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Fiabilitate si Durabilitate - Fiability & Durability No 1/ 2014 Editura “Academica Brâncuşi” , Târgu Jiu, ISSN 1844 – 640X
1
CONTENTS
Pag.
1. Iulian POPESCU, Ludmila SASS - MODELLING THE MOVEMENT OF MECHANISMS WITH
THREE DYADS OF RRT TYPE. GENERAL CASE
3
2. Ludmila SASS, Iulian POPESCU - MODELLING THE MOVEMENT OF MECHANISMS
WITH THREE DYADS OF RRT TYPE. PARTICULAR CASES
10
3. Liliana LUCA, Iulian POPESCU - KINEMATICS OF A SCISSORS MECHANISM 18
4. Ion TĂTARU, Cosmin-Mihai MIRIŢOIU, Dan ILINCIOIU - THE VALIDATION OF SOME
EXPERIMENTAL RESULTS USING A NUMERICAL METHOD WITH 3D MESHING ELEMENTS
27
5. Mariana PǍTRAŞCU, Doina TǍRǍBUŢǍ, Simona IONESCU, Constantin D. STǍNESCU -
RESEARCH ON EXTRACTION PIPES OF DEWAXING PROBES
33
6. Mariana PǍTRAŞCU, Doina TǍRǍBUŢǍ, Simona IONESCU, Constantin D. STǍNESCU -
RESEARCH ON EQUIPMENT FOR MINING EQUIPMENT, DEWAXING PROBES
43
7. Cristian PIRGHIE, Ana-Camelia PIRGHIE - CHARACTERIZING THE BEHAVIOR OF THE
LUBRICANT FILMS USING MOLECULAR DYNAMICS SIMULATIONS
49
8. Sebastian Marian ZAHARIA, Cristin Olimpiu MORARIU - STATISTICAL PROCESSING OF
CENSORED DATA UNDER ACCELERATED RELIABILITY TESTING FOR RADIAL BALL
BEARING
57
9. Marin NEACSA, George ADÎR, Victor ADÎR, Ancuta ADÎR - DYNAMIC STUDY OF THE R-RTT
MECHANISM ASSISTED BY AUTODESK INVENTOR
64
10. Stan Marius - THE FAILURE MODES AND THEIR REMEDIATION PROGRESSIVE CAVITY
PUMPS USED IN OIL PRODUCTION
71
11. Gheorghe MARC, Maria Loredana BOCA - USING LOGIC PROGRAMMING FOR IMPROVE
AND INCREASE THE RELIABILITY OF TOOLS AND EMBEDDED MACHINE TO AVOID SOME
“MISSION CRITICAL „ IN FLEXIBLE MANUFACTURING LINES
78
12. Anastase PRUIU, Traian FLOREA, Daniel MĂRĂȘESCU, Adriana SPORIȘ -
CONSIDERATIONS IN DETERMINING ANALYTIC GRAPHICS FUNCTIONAL PARAMETERS OF
MARINE PROPULSION ENGINES
84
13. Anastase PRUIU, Traian FLOREA, Daniel MĂRĂȘESCU,Adriana SPORIȘ - ABOUT ENGINE
ROOM VENTILATION ON MERCHANT VESSELS
91
14. Ion BULAC , MATHEMATICAL MODEL FOR DETERMINING KINEMATIC PARAMETERS OF
THE CARDAN JOINT MECHANISM WITH TECHNICAL (GEOMETRICAL) DEVIATIONS
97
15. Ion BULAC, THE NUMERICAL STUDY OF THE INFLUENCE OF TECHNICAL
(GEOMETRICAL) DEVIATIONS OVER THE KINEMATIC PARAMETERS OF THE CARDAN JOINT
MECHANISM
103
16. Răzvan Bogdan ITU, Iosif DUMITRESCU, Vilhelm ITU - CORRELATING 2K-52MU CUTTING
AND LOADING MACHINE WITH TR-5 SCRAPER CONVEYER
110
17. Răzvan Bogdan ITU, Iosif DUMITRESCU, Vilhelm ITU - STUDY OF STABILITY OF 2K-52MU
CUTTING-LOADING MACHINE ON TR-5 CONVEYER IN FACES WITH INDIVIDUAL SUPPORT
120
18. Mădălina DUMITRIU - INFLUENCE OF THE SUSPENSION PARAMETERS UPON THE
HUNTING MOVEMENT STABILITY OF THE RAILWAY VEHICLES
129
19. Mădălina DUMITRIU - THE DYNAMIC BEHAVIOUR OF THE RAILWAY VEHICLES IN
CROSSING AN ISOLATED NIVELMENT DEFECT
137
20. GEORGE Novac - CRANK WEB DEFLECTIONS OF MARINE DIESEL ENGINES 145
21. GEORGE Novac - EXHAUST VALVE WEARS OF MARINE DIESEL ENGINES 151
22. Traian FLOREA, Ligia-Adriana SPORIȘ, Corneliu MOROIANU, Traian Vasile FLOREA,
Anastase PRUIU - GRAPHO-ANALYTICAL METHOD FOR CALCULLATING IRREVERSIBILITY
PROCESSES WITH FINITE SPEED
157
Fiabilitate si Durabilitate - Fiability & Durability No 1/ 2014 Editura “Academica Brâncuşi” , Târgu Jiu, ISSN 1844 – 640X
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23. Traian FLOREA, Corneliu MOROIANU, Traian Vasile FLOREA , Ligia Adriana SPORIȘ,
Anastase PRUIU - THE COEFFICIENT OF REGENERATIVE LOSSES IN STIRLING MACHINES
165
24. Adina TĂTAR - GAUSSIAN MODEL 174
25. Corneliu MOROIANU, Ligia Adriana SPORIȘ, Traian FLOREA - THE DETERMINATION OF
THEORETICAL COMBUSTION TEMPERATURE OF HEAVY FUELS CONSIDERING THE
DISSOCIATION OF WATER VAPOURS FROM THE BURNING GASES
178
26. Corneliu MOROIANU, Traian FLOREA, Ligia Adriana SPORIȘ - MATHEMATICAL MODEL
FOR BURNING THE MARINE DIESEL FUEL DROP IN A HOT OXIDIZING ENVIRONMENT
183
27. Ligia-Adriana SPORIȘ, Traian FLOREA, Corneliu MOROIANU - ASUPRA UNUI SISTEM
KOROVKIN ÎNTR-UN CON DE FUNCŢII PONDERATE
190
28. Ligia-Adriana SPORIȘ, Corneliu MOROIANU, Traian FLOREA - ASUPRA UNOR ASPECTE
CALITATIVE ALE CONVERGENŢEI ÎN SPAŢII LINIARE ORDONATE TOPOLOGICE
193
29. Monica BÂLDEA, Mihaela ISTRATE - PROGRAM FOR THE CALCULATION OF GEOMETRIC
OPTIMIZATION OF PRIMARY SEALS
195
30. Iuliana Carmen BĂRBĂCIORU - A NOTE ON (α,β)-CUT IN INTUITIONISTIC FUZZY SETS
THEORY
200
31. Iuliana Carmen BĂRBĂCIORU , Viorica Mariela UNGUREANU - LYAPUNOV TYPE
OPERATORS ON ORDERED BANACH SPACES
207
32. Mădălina Roxana BUNECI - RANDOMLY GENERATED SUBGROUPOIDS OF X×Z×X 213
33. Mădălina Roxana BUNECI - USING MAPLE FOR VISUALIZATION OF TOPOLOGICAL
SUBGROUPOIDS OF X×Z×X
220
34. Elisabeta Mihaela CIORTEA, Mihaela ALDEA - ASPECTS OF A LINEAR PROGRAMMING
MODEL DEDICATED TO THE TRANSPORT SYSTEM 227
35. Miodrag IOVANOV - AN EXTREMAL PROBLEM FOR UNIVALENT FUNCTIONS 234
36. Constantin P. BOGDAN, Olimpia PECINGINA - BOOLEAN NORMED ALGEBRAS 240
37. Constantin P. BOGDAN, Olimpia PECINGINA - EXTENSION OF AN ADDITIVE FUNCTIONS
NUMARABILE
247
38. Olimpia PECINGINA Constantin P. BOGDAN, - ABN AND METRIC STRUCTURES SPACES OF
MEASURES
254
39. Cătălina IANĂŞI - INCREASING RESISTANCE OF STRUCTURAL ELEMENTS WITH CFRP
REINFORCEMENTS
261
Fiabilitate si Durabilitate - Fiability & Durability No 1/ 2014 Editura “Academica Brâncuşi” , Târgu Jiu, ISSN 1844 – 640X
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MODELLING THE MOVEMENT OF MECHANISMS
WITH THREE DYADS OF RRT TYPE. GENERAL CASE
Professor Iulian POPESCU,
University of Craiova, member of Romanian Academy of Technical Sciences,
Associate Professor PhD Ludmila SASS,
University of Craiova, Faculty of Mechanics, [email protected]
Abstract. The paper deals with the modeling of mechanisms with three dyads of type RRT and
rotating leading element. Generated trajectories are provided, along with the sliders’ laws of
motions. The mechanism’s operational angular range is limited to the subinterval 00…180
0
because the Grashof conditions are disobeyed. Diagrams depicting the variation of coordinates
corresponding to the points presenting practical interest are presented.
Keywords: mechanism with three RRT dyads, trajectories, movement laws
1. INTRODUCTION
The movement of one of the 1,234,620 possible mechanisms with three dyads dyads [2]
is modeled, in order to reveal its kinematics. It relies on three RRT dyads. As far as we know,
no specialty studies on this mechanism were issued. Instead, mechanisms with 5 and 7 bar
presented interest for scientists. For example [3] presents the structured synthesis of the afford
mentioned mechanism, based on orthogonal trajectories. Distortions and couplers‘ mobility
are considered. [1] includes studies on many mechanisms with rotation couplers and glides,
used for research dedicated spatial vehicles. Further on we will study a mechanism based on
three dyads of RRT type.
2. THE STUDIED MECHANISM
The movement of the mechanism depicted by Fig. 1 was modeled.
Fig. 1. The studied mechanism
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It consists of a leading element with a rotation movement AB, the first dyad BCD,
linked to the elements 1 and 0 (base), the second dyad EFG of type RRT connected to the 2-
nd and 3-rd element and the 3-rd RRT dyad HKL, connected to the 4-th and 5-th elements.
The mechanism‘s structural formula [2] is consequently: R-RRT-1+0- RRT-2+3-RRT-4+5.
The mobility degree is: M=3n – 2C5-C4=3.7-2.10=1.
Using the contours‘ method, the following equations can be written:
sin.
cos.
AByy
ABxx
AB
AB (1)
sin.sin.
cos.cos. 3
DCyBCyy
DCSBCxx
DBC
BC (2)
sin.
cos.
BEyy
BExx
BE
BE (3)
sin.sin.sin.
cos.cos.cos.
2
23
GFSyEFyy
GFSSEFxx
DEF
EF (4)
cos.cos.
sin.sin.
3 GFSEFx
GFyEFytg
E
DE
(5)
1 (6)
sin.
cos.
EHyy
EHxx
EH
EH (7)
2 (8)
sin.
cos.
2
23
Syy
SSx
DG
G (9)
sin.sin.sin.
cos.cos.cos.
5
5
LKSyHKyy
LKSxHKxx
GHK
GHK (10)
cos.cos.
sin.sin.
LKxHKx
LKyHKytg
GH
GH
(11)
3. RESULTS
The dimensions considered by our study are: Ax =18; Ay =22; AB=64; BC=81; DC=70;
EF=58; GF=90; HK=47; LK=38; yD=15; EH=26; BE=40; HM=24; 1 =75; 2 =115; =98;
1 .
Fig. 2 depicts the mechanism‘s position for =70o. Fig. 3 depicts the mechanism‘s
subsequent positions, considering that the element AB does not perform full rotations owing
to the adopted sizes which do not meet the Grashof conditions.
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Fig. 2. The mechanism’s position for =70
o
Fig. 3. The mechanism’s subsequent positions
Fig. 4, presenting the trajectories of points B and C, reveal that B describes only a part
from the circle and C‘s race is small.
Fig. 4. The trajectoris of points B and C
The trajectories of points E and D are given in Fig. 4. D moves along a line whilst the
trajectory followed by E is an open rod-type curve.
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Fig. 5. The trajectories of points E and D
The trajectories described by the points G (in the right side) and F (in the left side) are
depicted by Fig. 6. Both fall in the category of rod-type curves with loops.
Fig. 6. The trajectories described by the points G and F
Fig. 7 depicts the trajectories of points L, H and K. They are similar, but shifted.
Fig. 7. The trajectories of points L, H and K
Fig. 8 is used to reveal a comparison between the trajectories of the points K and M
from the element EF. They are similar, the one corresponding to M being left-shifted to that
corresponding to K.
Fig. 8. A comparison between the trajectories of the points K and M
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The variations of traces S3 and S2 are provided by Fig. 9. One can see that the
mechanism can operate only for angles within the range 0o…180
o. For angles >180
o
segments appear in the diagram. The program used for simulation joins the ranges‘ limits by
means of lines.
Fig. 9. The variations of traces S3 and S2
Fig. 10 present the variation of the trance S5 with respect to . Also is revealed that the
mechanism cannot operated for o180
Fig. 10. The variation of the trance S5 with respect to
The variations for the coordinates of points E and G, at the input of the 2nd
dyad, given
by Fig. 11, represent a new proof for the mechanism‘s blocking when >180o. The curves
are normal for the rest of the values.
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Fig. 11. The variations for the coordinates of points E and G, at the input of the 2nd dyad
Similarly in Fig. 12 one presents the variations corresponding to the coordinates of the
points H and L from the input of the 3-rd dyad. Conclusions identical to those from above can
be drawn.
Fig. 12. The variations corresponding to the coordinates of the points H and L
from the input of the 3-rd dyad
The diagrams for the coordinates of the points F, K and M (Fig. 13) reveal the already
mentioned blocking for >180o. An interesting aspect is related to the similarity of the
curves xi and yi respectively.
Fig. 13. The diagrams for the coordinates of the points F, K and M
0.0 100. 200. 300. 400.
Fi [ grd]
-50.
0.0
50.
100.
150.
200.
X EY EX GY G
0.0 100. 200. 300. 400.
Fi [ grd]
-50.
0.0
50.
100.
150.
X HY HX LY L
0.0 100. 200. 300. 400.
Fi [ grd]
-100.
-50.
0.0
50.
100.
150.
X FY FX KY KX MY M
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4. CONCLUSIONS
- Studies on the mechanism R-RRT-1+0- RRT-2+3-RRT-4+5 were performed.
- Owing to the disobeying of Grashof conditions, the mechanism can operate only for
=0o…180
o.
- The curves generated by the points of interest are open rod curves. Although being
characterized by a high degree, they are not spectacular.
- The variations of the glides‘ traces variations were also represented. Normal diagrams were
obtained.
REFERENCES
1. Brink Jeffrey S. – Reverse kinematic analysis and uncertainty analysis of the space suittle
aft propulsion system (APS) pod lifting fixtura. A thesis, University of Florida, 2005.
2. Popescu Iulian. – Mecanisme. Noi algoritmi şi programe, Reprografia Universităţii din
Craiova, 1997.
3. Shih -Hsi Tong - Design of High-Stiffness Five-Bar and Seven-Bar Linkage Structures by
Using the Concept of Orthogonal Paths. J. Mech. Des. 128(2), pp. 430-435, Jun. 23, 2005.
Fiabilitate si Durabilitate - Fiability & Durability No 1/ 2014 Editura “Academica Brâncuşi” , Târgu Jiu, ISSN 1844 – 640X
10
MODELLING THE MOVEMENT OF MECHANISMS
WITH THREE DYADS OF RRT TYPE. PARTICULAR CASES
Associate Professor PhD Ludmila SASS,
University of Craiova, Faculty of Mechanics, [email protected]
Professor Iulian POPESCU,
University of Craiova, member of Romanian Academy of Technical Sciences,
Abstract. The paper deals with the modeling of mechanisms with three dyads of type RRT and
rotating leading element. Generated trajectories are provided, along with the sliders’ laws of
motions. Diagrams depicting the variation of coordinates corresponding to the points presenting
practical interest are presented. Two particular cases related to certain sizes of some elements are
studied.
Keywords: mechanism with three RRT dyads, particular cases, trajectories, movement laws
1. INTRODUCTION
This paper deals with the general case of the mechanism with three RRT dyads. [2]
provides a study of a mechanism with 6 bars of a press with certain elements having
adjustable lengths. The kinematics of the mechanism obtained through re-sizing are studied.
[3] presents the structural synthesis of the mechanisms with 5 and 7 bars, based on orthogonal
trajectories, when distortions and couplers‘ mobility are considered. In order to know the
kinematics possibilities of certain variants of the mechanism with three RRT dyads (namely
when some elements are zero sized), the movements of certain particular cases are modeled.
2. STUDIED MECHANISM
The starting point consist in the general case of the studied R-RRT-1+0- RRT-2+3-RRT-
4+5 mechanism [1], depicted by Fig. 1.
Fig. 1. Studied mechanism
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Particular cases were obtained varying the sizes of certain elements.
3. RESULTS
The initial values for mechanism‘s sizes are: xA=18; yA=22; AB=64; BC=81; DC=70;
EF=58; GF=90; HK=47; LK=38, yD=15; EH=26; BE=40; HM=24; 1=75; 2=115; =98;
= + 1.
The first particular case corresponds to the case when AB is a rod. Repeated tests
yielded the following modifications: AB=30, DC=35. Fig. 2 depicts a mechanism obtained for
=700. One can see that the point G goes downward the rod from D.
Fig. 2. A mechanism obtained for =70
o
Fig. 3 depicts successive positions of the mechanism, revealing that the mechanism is
operational for the entire cycle.
Fig. 3. Successive positions of the mechanism
Fig. 4 reveals that B moves around a full circle and the trace of C is short.
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Fig. 4. B moves around a full circle and the trace of C is short
The curves from Fig. 5 present the variations of the coordinates of B specific to a circle.
xC has a nonlinear variation whilst yC is constant, its translation being imposed by the glide
from D. The trajectories of E and G, at the input of the 2- nd dyad, represent rod-type curves
and are given by Fig. 6.
Fig. 5. The variations of the coordinates of B specific to a circle
Fig. 6. The trajectories of E and G
The variations for the coordinates of these points are given by Fig. 7. The corresponding
curves are continuous, with symmetric features.
0.0 100. 200. 300. 400.
Fi [ grd]
-50.
0.0
50.
100.
150.
X BY BX CY C
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Fig. 7. The variations for the coordinates of the points E and G
The trajectories depicted by Fig. 8 correspond to the points H and L, from the input of
the 3-rd dyad, whilst Fig. 9 presents the variations corresponding to their coordinates.
Fig. 8. The trajectories described by the points H and L
The trajectory of L is a rod-type curve, egg-shaped, whilst the trajectory of H reveals
non-symmetric features and some disturbances in the up-right corner. The curves from Fig. 9
present symmetric features.
Fig. 9. The variations for the coordinates of the point L
0.0 100. 200. 300. 400.
Fi [ grd]
0.0
25.
50.
75.
100.
125.
X EY EX GY G
0.0 100. 200. 300. 400.
Fi [ grd]
-20.
0.0
20.
40.
60.
80.
X HY HX LY L
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The trajectories described by the points F, K and M are depicted by Fig. 10. The up
curve exhibits the same abnormal behavior as the above discussed case for the trajectory of K.
The curves have a high degree and their shape make them fall into the same category with
similar rod-type curves corresponding to other mechanisms.
Fig. 10. The trajectories described by the points F, K and M
Fig. 11 presents the variations for the coordinates of the points F, K and M. One can see
the partial overlapping of the curves xK and xM and a quasi-parallelism for the curves yK and
yM. It means that the points from the element HK have similar trajectories.
Fig. 11. The variations for the coordinates of the points F, K and M
The traces S3, S2 and S5 present the variations from Fig. 12. One can notice the trace S5
with some irregularities for =0o…170
0. Traces with similar shapes are sometimes
associated to simpler mechanisms.
0.0 100. 200. 300. 400.
Fi [ grd]
-50.
0.0
50.
100.
150.
X FY LX KY KX MY M
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Fig. 12. The traces S3, S2 and S5
Another particular case can be obtained when considering zero lengths for the elements
3, 5 and 7. Actually the sizing DC=0 cannot be accomplished because the sliding route of G
should vanish and a condition GF=0 should involve no guidance for L. The only possible
alternative is therefore KL=0. The rest of sizes are preserved.
Fig. 13 depicts the mechanism obtained for =700. Fig. 14 presents the subsequent
positions of this mechanism.
Fig. 13. The mechanism obtained for =70
o
Fig. 14. The subsequent positions of the mechanism
The trajectories for the points B, C, D, E, G, H and L will be identical to those presented
above, the only different trajectories corresponding to the points K and M. They are depicted
by Fig. 15 and are rod-type curves similar to other familiar ones.
0.0 100. 200. 300. 400.
Fi [ grd]
0.0
25.
50.
75.
100.
125.
150.
S3S2S5
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Fig. 15. The trajectories described by the points K and M
The variations of the coordinates of K and M are depicted by Fig. 16. Symmetries and
similarities are detected for the curves corresponding to xK and xM, whilst some non-
uniformities are included by the yK and yM curves.
Fig. 16. The variations of the coordinates of K and M
The shape for the trace S5 is depicted by Fig. 17. It has symmetries and a jump for
>1800. The movement low is interesting and very few mechanisms describe it.
Fig. 17. The shape for the trace S5
4. CONCLUSIONS
- Studies were made concerning the modeling of the movement corresponding to the R-RRT-
1+0- RRT-2+3-RRT-4+5 mechanism for particular cases;
- When searching for particular cases, two of the elements linked to glides cannot be reduced
to zero length, because other glides should remain without guides;
- The first particular case assumed the determination of mechanism‘s sizes such as to make
the leading element to describe full rotations;
- The second particular case involved a null length for an element;
0.0 100. 200. 300. 400.
Fi [ grd]
-25.
0.0
25.
50.
75.
100.
125.
X KY KX MY M
0.0 100. 200. 300. 400.
Fi [ grd]
20.
22.5
25.
27.5
30.
32.5
S5
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- Trajectories were build and variations for the couplings of interest were provided;
- The resulted trajectories are rod-type curves with high degree whose shape are common,
excepting two cases where some abnormal behaviors were detected;
REFERENCES
1. Popescu Iulian – Mecanisme. Noi algoritmi şi programe, Reprografia Universităţii din
Craiova, 1997.
2. Ren-Chung Soong – An adjustable six-barmechanism with variable input speed for
mechanical forming presses. Transactions of the CSMEIde fa SCGM Vol. 32, No. 3-4,2008.
3. Shih -Hsi Tong - Design of High-Stiffness Five-Bar and Seven-Bar Linkage Structures by
Using the Concept of Orthogonal Paths. J. Mech. Des. 128(2), pp. 430-435, Jun. 23, 2005.
Fiabilitate si Durabilitate - Fiability & Durability No 1/ 2014 Editura “Academica Brâncuşi” , Târgu Jiu, ISSN 1844 – 640X
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KINEMATICS OF A SCISSORS MECHANISM
Prof. PhD. Liliana LUCA, Constantin Brancusi University of Targu-Jiu,
Prof. PhD. Iulian POPESCU, University of Craiova,
Abstrac:. We study the kinematics of a scissors mechanism composed of two conductive elements with related
movements and a RTR type dyad. They are written the relations based on contours method and they are given
the results in tables and diagrams.
Keywords: mechanisms for scissors, kinematic analysis, two conductive elements.
1 . INTRODUCTION
The mechanisms from the scissors of debitting metals have been studied over time by
various methods. Many of them were built empirically, on summary calculations. Computers
and new analytical analysis methods allow more detailed studies, which led to improving the
performance of these mechanisms. In the literature, studies continue to show this theme .
Thus, in [1] it is studied the kinematics of a scissors mechanism with a triad, which is
intended for cutting of steel products. They are given the analytical relations based on
contours method and numerous resulted diagrams. In a doctoral thesis [2] they are studied in
detail the mechanisms that ensure shear cutting branches of trees in order to clean them. They
are studied different variants of mechanisms, by modeling them . A detailed dynamic study on
a shear mechanism is given in [3]. The mechanism consists of two dyads .They are calculated
the positions, velocities , accelerations and reactions of couplings .
2. INITIAL DATA
We left from the kinematic scheme of a mechanism given in [4] and shown in Fig. 1.
Items 1 and 4 are both leading, with movements linked by a gear, cog belts, chain
Galle chain or other system. In E and F points are the tips of two knives that run the shear,
point F being on the element 2 which is having a flat movement and point E belongs to
element 3, which also has a flat movement. The symmetry properties of the mechanism allow
for a position of the mechanism the knives to cut the blank (sheet) 5.
3. THE MECHANISM STRUCTURE
The structural diagram of the mechanism is given in Fig. 2. The mobility degree is:
M=3n-2C5-C4=3.4-2.5=2, the mechanism having two conductive elements and a BCC dyad of
RTR type.
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Fig. 1 Fig. 2
4. THE MECHANISM KINEMATICS
The correlation between angles and is obtained (Fig. 3), through the relations:
Fig. 3
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θ - α= 90 (1)
Ψ+ α= 270 (2)
Ψ+ θ - 90=270 (3)
Ψ=360- θ (4)
For the kinematic analyze, they are written the relations:
xB =xA+ABcosθ (5)
yB =yA+Absinθ (6)
xC =xD+CDcosψ (7)
YC =YD+CDsinψ (8)
S=yC-yB (9)
S2=yB + BF (10)
S3=yC-CE (11)
xF=xB-a (12)
yF=yB+BF (13)
xE=xC-a (14)
yE=yC-CE (15)
We have adopted the following initial values:
XA = 400: XD = 400: YD = 700: BF = 50: CE = BF: AB = 300 CD = AB: A = BF / 2.
5.THE OBTAINED RESULTS
In the FIG. 4 it is shown the mechanism for = 120 degrees. The image is similar to
that of FIG. 1, so the program is done correctly. The two points of the figure are the E and F
points, that is the tips of the knives for this position.
The successive positions of the mechanism are shown in Fig. 5 for .0...120
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Fig. 4 Fig. 5
It is noted that while element 1 rotates clockwise, item 4 rotates counterclockwise.
The figure also shows the trajectories of E and F points, thus the trajectories of knives peaks.
At a full rotation they result the successive positions of Fig. 6.
The trajectories of tops knives are circles and race S, meaning the distance between C
and B, is variable (fig. 7 for .0...120 ).
Fig. 6 Fig. 7
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The complete trajectories of E and F points are shown in Fig. 8, and they are circles
with centers that are different of A and D (Fig. 9), as E and F are located close to the C and B
but offset to their left. In the figure also appear and C and B circles.
Tangent circles of FIG. 9 are described by E and F.
Fig. 8 Fig. 9
The variations of S, S2 and S3 races to the position of the mechanism are shown in
Fig. 11. It is observed that the minimum S, S2 and S3 races are equal to 90 degrees.
0.0 100. 200. 300. 400.
Fi [ grd]
-500.0
0.0
500.
1000.
1500.
SS2S3
Fig. 10
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Referring to FIG. 11, it is shown that diagrams for coordinates variation of the F and B
points are very close, the shifts being determined by the fact that E and F are also staggered
relative to the BC element.
0.0 100. 200. 300. 400.
Fi [ grd]
-400.0
-200.0
0.0
200.
400.
600.
800.
X BY BX FY F
Fig. 11
The same observation applies to the E and C coordinates in Fig. 12.
0.0 100. 200. 300. 400.
Fi [ grd]
0.0
200.
400.
600.
800.
1000.
X CY CX EY E
Fig. 12
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For the drawer, it is interesting the contact area between the blade tips. To this, they
were plotted in FIG. 13 the coordinates of E and F points, observing that for of about 90
degrees, YE and YF curves are tangent, meaning the E and F points coincide, this is the
shearing time.
0.0 100. 200. 300. 400.
Fi [ grd]
-250.0
0.0
250.
500.
750.
1000.
X EY EX FY F
Fig. 13
In Table 1 they are also given the numerical results for this area of the operating cycle of the
mechanism.
Table 1
Fi XE YE XF YF
80 427.0933 354.5575 427.0948 345.4423
81 421.9293 353.6933 421.9307 346.3065
82 416.7509 352.9194 416.7523 347.0804
83 411.5598 352.236 411.5611 347.7638
84 406.3575 351.6433 406.3589 348.3565
85 401.1457 351.1415 401.1471 348.8584
86 395.926 350.7307 395.9273 349.2692
87 390.6999 350.4111 390.7012 349.5889
88 385.4688 350.1827 385.4702 349.8172
89 380.2347 350.0457 380.2361 349.9543
90 374.999 350 375.0003 350
91 369.7633 350.0457 369.7647 349.9544
92 364.5291 350.1828 364.5305 349.8173
93 359.2982 350.4112 359.2996 349.5889
94 354.072 350.7308 354.0734 349.2692
95 348.8523 351.1417 348.8537 348.8584
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96 343.6405 351.6436 343.6419 348.3566
97 338.4383 352.2363 338.4396 347.7639
98 333.2472 352.9197 333.2485 347.0805
99 328.0687 353.6937 328.0701 346.3066
100 322.9046 354.5578 322.9059 345.4424
It appears that indeed, at = 90, YE = YF.
It has been enlarged the diagram of FIG. 13 in the area of interest, finding fig. 14 and
15, where it is clear the tangency of the two circles and the equality of the two ordinates.
80. 85. 90. 95. 100.
Fi [ grd]
300.
325.
350.
375.
400.
425.
450.
X EY EX FY F
Fig. 14
80. 85. 90. 95. 100.
Fi [ grd]
340.
345.
350.
355.
X EY EX FY F
Fig. 15
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6. CONCLUSIONS
- The studied mechanism satisfies the condition of blank shear.
- Although blades are having a flat movement, they have trajectories that become tangent
when shearing.
- From constructive point of view, these knives can be even on BC element, without the
offset.
- The mechanism is cleverly designed.
REFERENCES
[1]. Berghian, A. B. , Vasiu, Th. , Kinetics study on laboratory model of the mechanisms of
parallel gang sheoars’ type assigned for cutting metallurgical products. Journal of
Engineering annals of Faculty of Engineering Hunedoara, tome V, 2007, fasc. 3.
[2]. Maglioni, C. ,Analysis of reciprocating single blade cutter bars. Tezi di Dottorato.
Universita di Bologna, 2009.
3]. Tyagi, R. K., Verma, M., Borah, S. , Dynamic analysis of a shaper machine cutting tool
and crank pin. Journal of Enviromental Science, Computer Science and Engineering &
Technology, sept.- nov. 2012, vol. 1 no.3, pp. 372-380.
[4]. Kojevnikov, S. N., Esipenko, Ia. I., Raskin, Ia. M. , Mehanizmî. Sparvocinâe posobie. Izd.
Maşinostroenie, Moskva, 1976.
[5] Popescu, I., Luca, L., Cherciu, M., Structura şi cinematica mecanismelor. Aplicaţii. Editura
Sitech, Craiova, 2013.
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THE VALIDATION OF SOME EXPERIMENTAL RESULTS USING A
NUMERICAL METHOD WITH 3D MESHING ELEMENTS
1Eng. Ion TĂTARU, University of Craiova, Faculty of Mechanics, Department of Applied
Mechanics and Civil Constructions, Calea Bucuresti Street, no. 107, Craiova,Code 200512,
Romania, [email protected] 2Assistant Phd. Eng. Cosmin-Mihai MIRIŢOIU, University of Craiova, Faculty of
Mechanics, Department of Vehicles, Transports and Industrial Engineering, Calea Bucuresti
Street, no. 107, Craiova,Code 200512, Romania, [email protected] 3Prof. phd. eng. Dan ILINCIOIU, University of Craiova, Faculty of Mechanics, Department
of Applied Mechanics and Civil Constructions, Calea Bucuresti Street, no. 107, Craiova,Code
200512, Romania, [email protected]
Abstract. In this paper we present the validation of some experimental results obtained in [1], where there was
presented a device for bars and plates bending which works with strain gauges attached, by using a numerical
method – the finite element analysis. There will be used the same loading variants as in [1]. The structure
analysis was made in Ansys with two types of meshing techniques: map mesh with Brick 8 Node 45 finite element
and auto mesh with Tet 10 Node 187. In the end, we will make comparisons between the used methods and
extract the errors that appear.
Keywords: metallic structure, finite element analysis, mesh, brick elements, tetrahedral elements
Contents:
1. Introduction
2. The previously studied problem
3. Finite element analysis. Meshing and loading cases
4. Conclusions
5. Acknowledgement
1. INTRODUCTION In this paper, starting from the experimental results determined in Miriţoiu (2012)[1],
we will present a finite element analysis validation method with three dimensional elements used for meshing: map mesh with Brick 8 Node 45 finite element and auto mesh with Tet 10 Node 187. In the end we will make comparisons between the results and determine the errors.
According to Călbureanu (2011)[2], the finite element method has appeared and rapidly developed because of the necessity to have a powerful, quick and simple method to solve the complex stress and displacement problems from various engineering areas, like: mechanics, aeronautics, civil engineering, nuclear engineering and marine engineering. This method can be successfully applied also for solving of some problems like: heat transfer, dynamic analysis, fluid mechanics, and so on.
In Quin (2010)[3] the finite element method was used for a complete modeling and calculation for steady state viscoelastic stress analysis. It was made an algorithm formulation of one-dimensional case and extended to a generalized one. The numerical examples were given for two cases: one-dimensional and two-dimensional. There are studied the effects of
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the load speed, material properties and pressure distributions at the contact surface. In Karunakaran (2011)[4] is presented a finite element procedure for thermal analysis in pulsed current gas tungsten arc welding (abbreviated PCGTAW) of Az 31B magnesium alloy sheets. The studied material can be used in aircraft, automobile and high-speed train components. The software Ansys was used for finite element analysis and the results obtained were compared with experimental ones. The conclusion of the study was that the finite element analysis using Ansys can be effectively used to model PCGTAW process for finding temperature distribution.
In El-Asfoury (2009)[5], the finite element analysis was used for a static and dynamic study of pelvic bone. The bone was subjected to quasi-static and dynamic loading conditions simulating the effect of both weight gain and impact.
The mechanism of damping in welded structures was studied in Singh (2010)[6]. The
study emphasized the theoretical investigation of slip damping in layered and jointed welded
cantilever structures using finite element approach. The developed finite element model
shows that the damping capacity of such structures is influenced by a number of vital
parameters, such as: pressure distribution, kinematical coefficient of friction and micro-slip at
the interfaces, amplitude, vibration frequency, specimen length and thickness.
2. THE PREVIOUSLY STUDIED PROBLEM In [1], a device for metallic structures (bars, plates) bending and stress measurement
was studied. The studied metallic structure is presented in fig. 1 and the used device is presented in fig. 2. According to [1], the device works with strain gauges (shown in fig. 3 and 4).
Fig. 2. The studied device [1]
Fig. 1. The studied metallic structure [1]
Fig. 3. The first half bridge [1]
Fig. 4. The second half bridge [1]
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Two loading variants were considered: variant 1- P= 701,55 daN, variant 2- F= 507,56 daN. The stresses obtained, for each loading case, are shown in fig. 5 and 6.
3. FINITE ELEMENT ANALYSIS. MESHING AND LOADING CASES For the first loading case, there was used a mapped mesh, with Brick 8 Node 45 finite
elements (fig. 7). The stress distribution for the whole structure is presented in fig. 7 and in fig. 8 the stress distribution in the area of the first half bridge is presented. From fig. 8 it can be seen that the stress distribution from the second half bridge area is almost 0. The stress distribution from the first half bridge is presented in fig. 9 for variant 1. The mesh type in variant 2 (with Tet 10 Node 187 meshing elements) is presented in fig. 10. In fig. 11 we have presented the stress distribution for the whole structure and in fig. 12 the stress distribution in the first half bridge area.
Fig. 5. The stress values in the first Fig. 6. The stress values in the second
loading case [1] loading case [1]
Fig. 7. Mesh type (variant 1) Fig. 8. Stress distribution (variant 1)
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Important remark: in the area of the second half bridge the stress values are very
small (according to fig. 8. and 11) and will be approximated being zero in the following parts of the paper (the real values are: for variant 1- 0,12∙10
-4 and for variant 2- 0,006736).
Fig. 9. Stress distribution (first half bridge) Fig. 10. Mesh type (variant 2)
Fig. 11. Stress distribution (variant 2) Fig. 12. Stress distribution (first half bridge)
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4. CONCLUSIONS In the table 1 we have listed the results obtained with the three-dimensional meshing
elements for the considered cases.
Table 1. The results obtained with the finite element analysis
Stress type Value [MPa]
Method Finite element analysis
Loading variants First loading variant Second loading variant
First half bridge 32,8125 69,125
Second half bridge 0,12∙10-4
0,006736
The results obtained with the experimental method from [1] are listed in table 2.
Table 2. Stress results from [1]
Experimental method
Stress type First half bridge Second half bridge First half bridge Second half bridge
Loading variant 1 2 1 2
Stress Value
[MPa] 34,269 0,0042094 72,871 0,0079752
We have determined the errors between the experimental and numerical method with
relation (1).
In (1) we have marked with: ε1 – the stress obtained with the experimental method, ε2
– the stress obtained with the numerical method and with εmax the maximul stress. The errors obtained are listed in table 3.
Table 3. Errors obtained between the experimental and numerical methods
Numerical method/ Experimental method Stress type First half bridge Second half
bridge First half bridge Second half
bridge Loading variant 1 1 2 2
Error [%] 4,25 0 5,141 0
From the table 3 we can extract the next conclusions: - the experimental method from [1] gives similar results like the numerical method, so
the strain gauges were glued well on the structure; - the errors are very small (under 6%); - the stress values obtained from the second half bridge are 0 (because the bars are not
loaded); - the stress values obtained from the first half bridge are different from zero, because
the area is loaded by the forces considered from the two loading variants;
100%max
21
(1)
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- both methods can be successfully used for metallic structures stress calculus; - the errors are higher when the tetrahedral elements are used, because this type of
elements insert higher errors than the hexahedral ones (used in the first loading variant), fact that was expected before using this type of elements.
4. ACKNOWLEDGEMENT
This work was supported by the strategic grant POSDRU/159/1.S/S/133255, Project
ID 133255 (2014), co-financed by the European Social Fund within the Sectorial Operational
Program Human Resources Development 2007-2013.
REFERENCES Miriţoiu, C., M., (2012) A Simple but Accurate Device and Method Used for Bending and Stress Measurement of Metallic Structures, IOSR Journal of Engineering (IOSRJEN), 2(6), 1334-1339 Călbureanu, M., (2011) Introduction to finite element analysis, Universitaria Publishing House Quin, F., Yu, Y., Rudolphi, T., (2010) Finite Element Modeling of Viscoelastic Stress Analysis under Moving Loads, International Journal of Mechanical and Materials Engineering, 4(1), 226-233 Karunakaran, N., Balasubramanian, V., (2011) Multipurpose Three Dimensional Finite Element Procedure for Thermal Analysis in Pulsed Current Gas Tungsten Arc Welding of AZ 31B Magnesium Alloy Sheets, International Journal of Aerospace and Mechanical Engineering, 5(4), 267- 274 El-Asfoury, El-Hadek, M., A., (2009) Static and Dynamic Three-Dimensional Finite Element Analysis of Pelvic Bone, International Journal of Engineering and Applied Sciences, 5 (5), 315-321 Singh, B., Nanda, B., K., (2010) Mechanism of Damping in Welded Structures using Finite Element Approach, International Journal of Information and Mathematical Sciences, 6(2), 138-142 Ajovalaist, A., Zucarello, B., (2005) Local Reinforcement Effect of a Strain Gauge Installation on Low Modulus Materials, The Journal of Strain Analysis for Engineering Design, 40 (7), 643-653 Atanackovic, T., (2000) Theory of Elasticity for Scientists and Engineers, Published by Birkhauser Boston Avalle, M., Goglio, L., (1997) Static lateral compression of aluminium tubes: Strain gauge measurements and discussion of theoretical models, The Journal of Strain Analysis for Engineering Design, 32 (5), 335-343 Huttelmaier, H., P., Glockner, P., G., (1985) Stresses and displacements due to underground mining using a finite element procedure, Geotechnical and Geological Engineering, 3(1), 49-63 Korayem, M., H., Heidari, A., Nikoobin, A., (2008) Maximum allowable dynamic load of flexible mobile manipulators using finite element approach, The International Journal of Advanced Manufacturing Technology, 36 (5,6), 606-617 Kulkarni, S., D., Kapuria, S., (2007) A new discrete Kirchhoff quadrilateral element based on the third-order theory for composite plates, Computational Mechanics, 39 (3), 237-246 Mao, S., Shi, Z., (2009) High accuracy analysis of two nonconforming plate elements, Numerische Mathematik, 111 (3), 407-443
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RESEARCH ON EXTRACTION PIPES OF DEWAXING PROBES
Drd. Eng Mariana PǍTRAŞCU (ANTONESCU); e-mail: [email protected]
Drd.Eng Doina TǍRǍBUŢǍ (ENE);e-mail: [email protected];
Matemat.drd.Simona IONESCU: e-mail: [email protected]
Prof.univ.Emerit. Dr.eng. Constantin D. STǍNESCU e-mail:[email protected]
Polytechnic University of Bucharest;
Abstract: In this paper I present dewaxing methods of extraction wells pipes. Dewaxing tubing of the
probes is done by mechanical, thermal, chemical Research undertaken on cleaning oil pipelines and networks as
for transport crude oil and petroleum products shows that within them is deposited drilling mud and paraffin
and cerezima which reduces pipe diameter and fluid flow velocity .In this context it is necessary, periods of
cleaning these pipes with solutions and special devices.
Keywords : dewaxing , pipeline, rehabilitation
1. INTRODUCTION
During operation of a hydrocarbon reservoir, and, in the probe and surface facilities is
submitted, a large amount of particles as a solid.
Paraffin wax or oil is the formula CnH2n +2 solid phase respectively C16H34 to
C64H130., Respectively, a mixture of liquid components, solid products (paraffin,
microcrystalline wax) as fine crystals, which add substance asphalt, resins sand, shale, clay.
After weight content of paraffin oils from Romania are divided into three categories:
- Waxy crude oils containing less than 2% paraffin;
- Semiparafinoase crude oils with a content of 1-2% paraffin;
- The wax crude oils containing less than 1% paraffin.
Separation of oil and paraffin deposition is greatly influenced by temperature and
pressure.
By lowering the temperature to reach a crystallization onset temperature of the wax,
and the lower part of pressure oil out of the solution, so that the dissolution capacity of the
solids falls.
Beginning of crystallization temperature is between 35 € - 38 ¤ C, as corresponds to
the paraffin deposition depths between 600 ... 1000 m as geothermal gradient and oil quality.
Paraffin oil is separated from the small crystals, which, due to movement of the fluid in
contact with each other, aglomerandu being around a nucleus, which may be a foreign body
such as sand, shale or fine metal particles resulted from the These clusters of corrosion
phenomena paraffin crystals are deposited on the walls of tubing, a phenomenon accentuated
tubing roughness.
Paraffin deposition is accentuated intermittently producing wells due to repeated oil
leaks on the interior walls of tubing.
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Areas where deposition occurs parafinii as conditions are:
- Layer pores - in the area immediately surrounding the hole made by the probe;
- The exit of the column operating layer of shallow wells
- Inside the column tubing the wells sucker for great depths;
- Inside the plant surface and the mixing pipe.
Paraffin deposits produce reducing production capacity wells, reducing fluid flow through
section tubing.
Methods to reduce and control paraffin deposition are:
- Prevention methods which prevent or delay the precipitation and deposition of paraffin;
- Methods for cleaning and removal of paraffin deposited in waxy crude equipment by
circulating
2. DEWAXING MECHANICAL TUBING WELLS ERUPTING
Dewaxing operation is performed using mobile winch and consists of the following
phases:
• Install the hard pole connector (which can attach a jar) and paraffin cleaner type A or
type B;
• insert the pipe assembly dewaxing;
• pressure mounts bronze rings and rubber seals;
• Install the downspout dewaxing glands, which is mounted above the last valve head
rash;
• Link to drain the casing;
Fig 1. Hydro hook
Fig 2. banana Guy
brake cleaner
Fig 3. brake cleaner
with variable
diameter and blade
furniture
Fig 4. brake cleaner with
furniture blade with straight
pins and brake cleaner with
spiral blades
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After the installation has been installed and controlled, open upper valve head slowly
eruption, noting if the hose is not leaking. Cleaner in the tubing down to the depth of paraffin
deposition.
After the cleaning tubing, pull the pipe cleaner, close the upper valve head eruption,
reduce pressure inside the casing, remove the stuffing and extracted cleaner.
To clean wax from the tubing walls or columns operation, use the lower scale and
other non-standard cleaners such as column hook dewaxing operation (Fig. 1) banana cleaner
(Fig. 2 ) with variable diameter and blade cleaner furniture (fig. 3), furniture cleaner blade and
guide pins, washers spiral blades (fig. 4)
3. DEWAXING MECHANICAL TUBING WELLS IN ARTIFICIAL
ERUPTION
Dewaxing column tubing wells operating in artificial eruption can use the same probes
used dewaxing natural eruption, but it can also use a special cleaner compressed acted
requiring installation of a special device at the head of eruption . Cleanser paraffin acted
compressed (Fig. 5) is made of two metal plates welded to the cross, which is welded a series
of fins arranged inclined. On top cleaner has a reducer fitted externally with radial notches to
be trapped and removed.
Equipment needed for the use of cleaner requires compressed, schematic in Fig. 5
consists of a launching tube made from a 3 1/2 in the upper part provided with a bumper
cover, the side with the connecting pipes 2, and a socket stop flap at the bottom and another A
lockable side of half the drain pressur.
Fig. 5. Diagram of dewaxing acted with cleaner compressed gas
1 separator, 2 spring detent 3-cap Silenced
In column tubing under parafining depth, a reduction seat mounts, fitted with silencer
to stop cleaner requires.
Dewaxing operation with this cleaner as follows:
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Release device is mounted on the upper valve head eruption. Remove its cap and
insert cleaner who sits on the flip stop.
It will stop the injection of gas through the annular space of the well by closing the
valve I, II then closes and valve through which fluid from the probe mixture. III then opens
valve at the top of the head of the eruption and acts on the throttle stops, allowing cleaner
requires the probe to descend through tubing under its own weight.
After the release pipe cleaner requires the injection of compressed gas begins by
opening the valve IV stick to push cleaner requires to seat reducer. In this time of scraped
cleaner wax deposited on the tubing wall.
It will stop the injection of gas through the tubing when the cleaner came in
termination point by closing the valve IV and will switch to normal injection gas through the
annular space by opening ventiluluui I.
- Evacuation probe mixture oil and gas and directing it to the separator by launching
device, opening the valve V.
Raising cleaner requires the device launch probe fluid. Cleanser flap switch lid damper stop
kicking, but can not return to the probe because the flap returns immediately closed position
under the action of a spring.
Open valve II to return oil to the normal route through arm rash head and close valves
III and V. To remove the head cleaners of dewaxing release gas will leak through the opening
below the 1/2 inch and then remove the lid of the launch.
4. DEWAXING MECHANICAL TUBING AND SUCKER RODS IN PUMPING
WELLS WITH PIPES
Dewaxing tubing in pumping wells with pipes is accomplished by means of coil
cleaners called scrapers (fig. 6).
A scraper has a cylindrical body of steel with a diameter of less than 4-5 mm than the
inside diameter of the tubing is inserted. On the body are processed three cutter wrapped by
the left propeller. Ends is properly threaded plugs that are inserted pole size.
Fig. 6. Cleaner helical
Cleaners are inserted between two poles socket instead of pumping the entire length of
the paraffin deposition zone.
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Cleaning paraffin column tubing, in this case, is made continuously by moving up and
down lining sucker for a length equal to the pumping stroke length during normal operation,
or periodically throughout the the paraffin deposition by executing a maneuver to seal pipes
of pumping over a distance greater than the distance between two cleaners.
Wells equipped with pumps that are included with sucker rods, not bobbing pump
mounting location during these maneuvers using a coupling device - called bayonet coupling
Dontov (Fig. 7.a), interlaced in the rod string at a depth greater than that which is deposited
paraffin.
The device consists of two parts:
- Barrel or bayonet scabbard fitted inside two parallel channels of special shape (Fig. 7
b);
- Hanging rod entering the bayonet scabbard and fix this with two wings, which engages
in the channels formed in the bayonet (Figure 7.c)
Fig 7 Bayonet Dontov
a-bayonet coupled device; b- bayonet scabbard; c-hanger rod with wings.
To leave a bayonet displacement of the weight of the ram pipes on the device rotates
gasket and then pull right up. To leave bayonet coupling down and automatically fins hanging
rod sliding on sloping channels and stop the clogged portion thereof.
In pumping wells equipped with pumps that are included with tubing not need this
device because of the pump piston can be lifted by sucker rods without leaking pipes.
A better cleaning tubing paraffin, along with cleaning rod pumping paraffin seal is
achieved by extracting sucker for changing pump P (R) or change piston pumps type T.
Dewaxing sucker is by direct scraping and extracting them from the probe.
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For scraping usually use a wire that wraps around the pipe and you stretched with two
rings (handles) of a probe while the probe is extracted from the pumping rod string. This
process is disadvantageous, presenting fire and some of the wax flows into the probe.
Instead use wire clippers dewaxing, which have two blades each provided with a
semicircular notch. When the blades are tight form an opening equal to the pipe section.
Were constructed and used sporadically site some special cleaners to clean wax from the
sucker rods.
Fig.8 Cleaner for pipes of pumping rubber wipers Fig.9 Tables of sucker rods with metal knife.
Figure 8 shows schematically a device for cleaning the wiper rubber mounts instead of
the polished rod stuffing box. This device has two semi-circular or helical rubber tiles that
sucker rubs during extraction of the probe. Grated paraffin flow through two side arms. Fins
pressed by a spring prevents penetration of wax scraped tubing. In Figure 9 is outlined wax
cleansing device on sucker rods with a metal knife.
5. THERMAL METHODS DEWAXING EXTRACTION PIPES FROM WELLS
This method is achieved by raising the temperature in the deposition of wax, that it
dissolve and be entrained in the upward fluid probe.
Heat to melt the wax is obtained by:
- Circulation of heat in the probe;
- Using an electric heating tubing.
Dewaxing tubing by circulating a heating using steam as heat, which is introduced into the
annular space and out through tubing with heated crude oil.
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Wells in artificial eruption, steam is introduced with the probe gas is injected in
ascension.
Pumping wells in leak pressure column and then steam generator is connected to the column.
Dewaxing pipes these probes are conducted in four phases:
1) steam is injected into the column, keeping the pump in operation for about 15
minutes;
2) is continuous steam injection, the probe stops for 15 minutes to heat the oil and
melt the wax resting on the walls of the pipes;
3) Replace the probe in use for 15 minutes, along with steam injection;
4) The new probe stops about. 15 minutes for heating oil at rest. Steam injection stops
and the probe is passed in continuous operation.
Probe can be inserted into another fluid heated by direct circulation or reverse.
Using the hot fluid has the advantage that it does not change the volume by giving
stored heat, condensation from steam, its volume shrinks more traffic. The heat used is crude
semiparafinos glazed or heated to 60-800 C. Water, although it has better thermal capacity is
not recommended as it can have a harmful influence on productivity layer exploited.
Dewaxing tubing with electrical heating is electrical energy conversion in heat energy.
Heaters are two types:
- Electric resistance heater;
- Electric heater induction.
Electric resistance heater (Fig. 10) consists of two conductors connected in series, with
different resistant. These conductors are column tubing equipped with plugs isolated column
operation.
Tubing heat from the electrical current will be higher than in column operation, due to
the difference of section (A Pipe > A column → then Rt> Rc) and the law Joule - Lenz result
Qt> Qc or:
where Q is the amount of heat that is released (in pipes Qt, Qc column);
I - the electric current;
R - the electrical resistance of the column tubing;
R - the electrical resistance of the column operation;
t - the amount of electrical current passing through the two conductors.
When using such an electric heater for dewaxing must ensure the necessary elements
insulation tubing from column exploitation insulating sleeves and a contact device at the
lower end of the pipe to close the electrical circuit between the pipes and columns.
Operated wells in pumping circuit consists of pipes and tubing, the focal point being the
piston pump shallow wells or springs contact device mounted on poles in depth parafining.
(1)
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Fig.10 Scheme dewaxing tubing with electric heater Fig.11 Scheme dewaxing tubing with induction heater
Induction heater (fig. 11) consists of a cylindrical body of metal (tubing), wearing
insulating material over which a coil is wound with copper wire, covered in turn with
insulating material and the entire assembly is locked in a shell.
The lower end of the coil are welded to the metal body, and the upper contact device
connects the column operation. The heater is mounted in the column pipe at a certain depth,
the power will be done through the column tubing and operating connected to a power source.
Warming is caused by induced AC.
6. CHEMICAL METHODS OF DEWAXING EXTRACTION PIPES
These methods consist in placing the tubing of a solvent, either pure or dissolved in a
liquid.
Type of solvent required for each probe, the amount required for treatment, the
proportion from transport agent, duration and frequency of treatment is determined
experimentally by taking samples of raw wax clean the tubing walls and reviewing the
corresponding solubility of different solvents in the same conditions.
To dissolve the wax can be used: carbon disulfide, carbon tetrachloride, methylene
chloride, chloroform, butane, either as a single component or as a mixture of several solvents.
For the transport of solvent into the wellbore may be used: gasoline, kerosene, diesel oil
glazed.
Dewaxing pipes eruptive wells following sequence:
- Insert the solvent extraction pipes, where allowed time of 3 - 4 o'clock maintaining probe
closed to dissolve the paraffin.
- Opens probe for a short time for cleaning.
- Close the probe and insert again solvent.
The operation is repeated several times in succession mentioned, then restore normal
function probe.
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Introducing the solvent with a higher density than the fluid in the probe is made by
The lubrication.
Pumping wells in traffic enforcement is indicated solvent.
It increases the flow probe increasing pumping elements so reduce submergenta.
Solvent is introduced into the annular space operating column - tubing is then sucked by the
pump with fluid discharged in the probe and tubing.
When the solvent reaches the pump head are directed into the annular space and
movement is mix oil - cleaning solvent to obtain paraffin deposition in production tubing.
Before reinserting the circuit oil mixture - solvent was removed from the probe will be a
separation of paraffin involved in the probe.
Dewaxing pipe mixture can be made about: mechanical, thermal, chemical.
Mechanical dewaxing paraffin pipeline is made using special cleaners called godevile.
Pig (Fig. 12) is a device composed of a central rod with one or more hinges, which is fixed to
a group of scraper wings, levers, having rollers at both ends needle for guide and some
supports for the fitting some of seals.
The joints allow Pig to pass easily through pipe bends. Seals made of leather or
synthetic rubber are designed to set in motion Pig in the fluid and push the wax scraped from
the pipe.
Gone are some blades scraping steel wax cleansing role. Gears, made of steel guides
cleaner and prevents its rotation. Launching and receiving godevilelor be done some special
connection pipes mixture, called the bypass pipe, fitted with valves to direct fluid required a
short insertion and removal of these cleaners.
Wheel steering:
Fig. 12. Godevil
Dewaxing about termicaa pipes is done by injecting superheated steam or hot oil.
Dewaxing chimica pipes are made with solvents that establish quantitative and
qualitative experimentally. Prevention of paraffin deposit pipe is cleaned by introducing
periodical liquid stream of pure solvent plugs.
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7. CONCLUSIONS
Research undertaken on cleaning oil pipelines and networks as for transport crude oil
and petroleum products shows that within them is deposited drilling mud and paraffin and
cerezima which reduces pipe diameter and fluid flow velocity. In this context it is necessary,
periods of cleaning these pipes with solutions and special devices.
REFERENCES
[1.] Branzan Ovidiu,Studiul prelungirii durabilitatii conductelor de transport produse
petroliere ,2007
[2.] Luerenich Sren-Untersuchun gen zur Bildung Korrosiver Belage inolge feuerten
Crasturbinen,Hachen 2009
[3.] Schutze,Michael-Conrosion and enviconmental degradation NewYork 2000
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RESEARCH ON EQUIPMENT FOR MINING EQUIPMENT,
DEWAXING PROBES
Drd. Eng Mariana PǍTRAŞCU (ANTONESCU); e-mail: [email protected]
Drd.Eng Doina TǍRǍBUŢǍ (ENE);e-mail: [email protected];
Matemat.drd.Simona IONESCU: e-mail: [email protected]
Prof.univ.Emerit. Dr.eng. Constantin D. STǍNESCU
e-mail:[email protected]
Polytechnic University of Bucharest;
Abstract :In thisprezentswouldrather on general aspects of the art equipment for dewaxingequipment
extraction wells Research undertaken on cleaning oil pipelines and networks as for transport crude oil and
petroleum products shows that within them is deposited drilling mud and paraffin and cerezima which reduces
pipe diameter and fluid flow velocity
In this context it is necessary, periods of cleaning these pipes with solutions and special devices
Keyworbs : dewaxing probe, pipe
1 INTRODUCTION
During operation of a hydrocarbon reservoir in the probe and the surface facilities is
submitted, a large amount of solid particles appropriate comb.
Paraffin wax oil or solid phase represents the formulaCnH2n+2respectivelyC16H34 up
toC64H130.,respectively, a mixture of liquid components, solid products (paraffin,
microcrystalline wax) as fine crystals, which add substance asphalt, resins, sand, shale, clay
After the weight content of paraffin naphthas in Romania is divided into three
categories:
- Paraffin oils containing less than 2% paraffin;
- Semiparafinoase oils with a content of 1-2% paraffin;
- Glazed oils containing less than 1% paraffin.
Separation and paraffin deposition in oil is much influenced by temperature and pressure.
The depression of the temperature reaching a crystallization onset temperature of the
wax, and the depression of a part of the pressure oil out of the solution, so that the dissolution
capacity of the solids falls.
Beginning of crystallization temperature is between 35 ¤ - 38
¤ C, corresponds to the
paraffin deposition depths between 600 ... 1000 m as geothermal gradient and quality of crude
oil.
Paraffin oil is separated from the small crystals, which, due to movement of the fluid
in contact with each other, making the being around a nucleus, which may be a foreign body
such as sand, shale or fine metal particles resulted from the corrosion phenomena paraffin
these clusters of crystals are deposited on the walls of tubing, a phenomenon accentuated
tubing roughness.
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Filing paraffin is sharp wells producing intermittent, due to repeated oil spills on the
inner walls of the tubing.
Areas where deposition occurs parafinii under the conditions specified are:
- The pores layer - the immediate area of hole made by Probe;
- The exit of the column operating layer of shallow wells
- Inside the column tubing wells sucker for great depths;
- The surface and inside of the mixing pipe.
Produce paraffin deposits decreasing production capacity wells, reducing fluid flow
through section tubing.
Methods for reducing and combating parafinǎ deposits are:
- Methods of prevention which prohibits evitǎ or paraffin precipitation and deposition;
- Clean and methods of paraffin removal of the equipment submitted that go paraffin oil.
2. PREVENT SETTLING PARAFFIN.
Keeping her training paraffin matter and appropriate comb crystals or agglomerates of
crystals on the surface and solubility in paraffin oil flow regime depends on the mixture and
thermodynamic regime of the probe .
For these reasons the following means to prevent shows of cellulose:
a) Maintenance of gas in solution by choosing a suitable operating rate higher
pressure and saturation pressure by providing the lowest possible pressure drop in the
tubing.
b) Avoid sudden pressure change by FOLLOWING measure by:
- Avoid using bottom nozzles;
- Avoid using columns telescopic tubing;
- Avoid possible to start using valves in the pipes parafining extraction;
- Carefully controlling the tightness of plugs and body tubing.
c) Influence of temperature conditions by:
- Loss prevention caldurǎ the path of the oil;
- Heating the oil before it reaches the foot of the probe with a paraffin deposit
temperaturǎ favorable views.
d) Avoiding flicker and pulsations in the operation of the probe.
e) The use of surface active agents such as paraffin retardants, working in meaning to
preventing accumulation of paraffin crystals by maintaining the suspension of
large amounts of fine crystals.
f) Ensure smooth movement by covering the inside of the tubing with special paints
or plastics to prevent adherence of paraffin crystals. In these lakes or plastic
coatings, even if not achieved total prevention of paraffin deposition, the
deposition of wax inside tubing is long overdue and it is relatively easy cleaning
due to poor adhesion of the wax film plastic.
g) The use of a pulsed ultrasound generator, the effect of the accumulation of gas
bubbles on the interior walls of the pipe, which change the structure of the
molecule will influence the shrinkage of the wax crystal formation temperature.
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Methods for removal of wax deposited on the inner walls of the column Probe tubing,
sucker rods and on the internal walls of the mixing pipes, consisting of:
cleaning about Mechanics;
Thermal cleaning;
chemical cleaning.
Each of these methods they differ depending on the operating system of the probes and
the nature of their equipment.
3. INSTALLATION DEWAXING MECHANICALLY.
Mechanical methods consist of scraping paraffin dewaxing to be submitted during the
operation of paraffinic hydrocarbons on metal surfaces through which they travel, using
special devices called knives.
Mechanical cleaning wax knives are inserted tubing periodically erupting wells
operated natural and artificial hives that are envisaged with special dewaxing plant.
Dewaxing assembly consists of the following elements:
dewaxing knife;
a heavy stick (or rod) mounted above the blade to ensure its descent producing
wells with high flow or bursts;
a special connection cable or wire;
cable or wire cutter launch and maneuver;
adewaxing pipe (head or head pistonaredewaxing);
a guide pulley cable or wire;
winch.
After the dimensions and construction components are three main types of dewaxing:
dewaxing heavy type;
dewaxing medium type;
dewaxing of light type;
Dewaxing of heavy type (Fig. 1) consists of: purifying tubular type A or type B
lamellar hard, heavy pole, fixed connection cable diameter 12-16 mm piston head and a winch
column intervention. Guidance cable is over crownblock tower production.
Dewaxing medium type (Fig. 2) consists of: Paraffin Cleaner easily laminated type C
or type D curǎţitor knives, heavy stick, removable connector, cable diameter 7 ... 8 mm, type
A head start for dewaxingdewaxing and mobile hoist.
Dewaxing easily type consists of: Cleaner easily laminated type C, heavy stick,
removable pipe, wire diameter 1.9 ... 2.2 mm, head wire B launch, over whose roll is guiding
wire and a hand winch type Yakovlev and Halliburton, which typically are used at different
probe measurements. Dewaxing mechanical eruption tubing wells is carried out using
standard paraffin cleaners which are schematically in Figure 3. and 4.
These knives have the upper thread with a pin which is screwed to a heavy pole.
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Heavy pole is a steel cylindrical Scheduled to a head pin and the other to jack the
thread sucker. Its role is to ensure the weight of the descending knife NECESSARY,
especially in wells with high pressure natural erupting respectively wells producing large
volumes or in bursts.
Fig. 1.Plant type dewaxing heavy
1 - Clean tubular or tubular type B, 2-pole heavy 3-
permanent connection, 4-wire 12 ... 16mm diameter., 5-
head piston column, 6 - winch intervention
Fig. 2 medium type dewaxing plant
1 Paraffin Cleaner easily laminated type C or type
D washers knives, 2 - heavy pole, 3-removable
connector, 4-wire with diameter 7 ... 8 mm, 5-head
type dewaxing launch, 6 - winch dewaxing phone.
a b c d
Fig. 3. Paraffin cleaners for wells in eruption
a) cleaners tubular type –A; b) cleaners hard lamellar type- B ; c.)cleaners easily slide type- C;
d.) cleaners with knives type- D.
-cleaner tube (sheath) - A (fig.3.a.) consists of a tubular body with a longitudinal cut,
with larger diameter at the bottom (a few mm less than the inside diameter of the pipe decǎt
which introduces ). The terminal body 450 is cut to provide the advancement easier, but also a
better scraping paraffin on the walls of the tubing.
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At the top is welded reducer for heavy pole now.
-cleaner hard lamellar type B (Fig. 3.b.) consists of a steel blade of 15 mm and length
of 1200 mm wind the strand in a sense the opposite upper and lower side, avoiding the
possibility rotation of the pipe cleaner.
-cleaners easily laminated type C (Figure 3.c) consists of a steel blade with a thickness
of 7 mm and a length of 500 mm. Body surface cleaners, twisted up and down in ways
contrary, are envisaged some windows that can easily switch from oil extraction pipe.
-D Cleanser knives (butterfly) (Figure 3.d) consists of a steel rod welded on three
floors of four knives with a special form. From one floor to another settlement knife is offset
by an angle of 300, so the knives to ensure the entire circumference, which provide a
complete cleaning wall tubing
Cleaner requires guidance is provided by four curved blades welded to the bottom of
the plunger body.
a ) b) c)
Fig. 4. Connectors, cables and wires
a)-fixed connection cable; b)- removable for cable connection; c)- removable connector for wire.
In Figure 4 presents the cable connections. From the point of view of the attachment of
the cable or wire is distinguished these types of connections:
a) fixed connection cable diameter 12 ... 18 mm (fig. 4 .. a). It is constructed from a piece
of steel pipe which is threaded for screwing the bottom heavy stick, and the upper and
lower diameter is provided on the outside with circular grooves to be caught in case
there Corunca probe . Inside the connector has a cylindrical hole that is half the length,
and the other half is conical. For this type of connection cable can not be removed
except by cutting;
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b) Connection removable cable diameter 7 ... 8 mm (fig. 4 .. b) does not require cutting
cable disassembly. Inside the steel body is fixed to a steel composed of two pieces and
a galvanized metal sheath, which assembles over the cable node.
c) Removable connection wires 1.7 ... 2.2 mm is shown in Figure 4.c. In this connection,
the head bends the wire around a pin having a diameter of 8 mm and a length of 20
mm. The free end of the wire head rotates several times around the wire. This knot
with a pin is retained until entering the coupling body.
Pistonare downspouts and dewaxing (Figure 5) is mounted at the head of the probe rash
introduction cleaners of paraffin. This casing has a diameter of 31/2 - 4 m and the length of
the downpipe 12, the upper part has a socket in which is screwed a particular sealing cap, and
the lower part has a thread in which is screwed a flange connecting the upper valve head
eruption. The body casing at the bottom of a pipe welding 23/8 which is mounted in the drain
pipe in the basement that serves the oil escaping from the well tubing by ferries, in the top of
the device casing.
Special head seal from the top of the casing is called oil removal. It consists of a lower
body, an intermediate body and a cap inside the bodies are aflǎ rubber gaskets for sealing
cable and pressing rings (two pieces) made of bronze.
Tighten the cable seals by rotating the cap with levers that is Scheduled.
Fig.5 Pipe dewaxing
1-cup, 2-lower body, 3 rubber seals, 4-socket 23/8 ", 5-ring compression,
6-body casing, 7-spacer, 8-body intermediate
4.CONCLUSIONS
Research undertaken on cleaning oil pipelines and networks as for transport crude oil
and petroleum products shows that within them is deposited drilling mud and paraffin and
cerezima which reduces pipe diameter and fluid flow velocity In this context it is necessary,
periods of cleaning these pipes with solutions and special devices
REFERENCES
[1.] BranzanOvidiu,Studiulprelungiriidurabilitatiiconductelor de transport
produsepetroliere ,2007
[2.] LuerenichSren-
UntersuchungenzurBildungKorrosiverBelageinolgefeuertenCrasturbinen,Hachen 2009
[3.] Schutze,Michael-Conrosion and enviconmental degradation NewYork 2000
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CHARACTERIZING THE BEHAVIOR OF THE LUBRICANT
FILMS USING MOLECULAR DYNAMICS SIMULATIONS
Lecturer Ph.D. Cristian PIRGHIE, Stefan cel Mare University of Suceava,
Department of Mechanics and Technology, [email protected]
Assistant lecturer Ph.D. Ana-Camelia PIRGHIE, Stefan cel Mare University of
Suceava, Department of Mechanics and Technology, [email protected]
Abstract. When large industries develop products, the size and complexity of it impose
major challenges. This is the case for nano-devices, which are widely present in engineering
applications. As we know, in nanotechnology the matter must be manipulated at this miniscule
scale, the nanotechnology playing by different rules. The laws we know for large systems do not
necessarily apply at the nanoscale. Doubtless, the nanotechnology developments are connected to
a correct understanding of micro- and nanotribological processes. The components used in micro-
and nanostructures are light and operate under loads, and generally lubricated with molecularly
thin films. The tribology field is evident interdisciplinary, involving scientists from many different
disciplines, including physicists, chemists, engineers, and biologists. Development of the
micro/nanotribology field has contributed to the fundamental understanding of friction and wear
processes, these being dependent on the surface interactions. The experiment results for lubricant
nanofilms have highlighted interesting properties, their comprehensive analysis being possible by
computer simulations, in the last decade an exponential increase in computing power simulation
techniques taking place. Giving the operating conditions lubricants are subjected to in practical
applications, in this paper the thin-film lubrication at sliding surfaces is considered. In this
respect, we are investigated confined nanofilms, between two walls, thin film lubrication being
simulated using non-equilibrium molecular dynamics. To impose shear on the fluid, the upper wall
is moved at different constant sliding velocities, in the same time supporting different constant
loads. Therefore, we provide a clearer understanding of the influence of molecular architecture on
lubricant viscous behavior.
Keywords: nanotribology, molecular dynamics, computer simulation, boundary lubrication
INTRODUCTION
In our days the requirements in engineering are continuously increasing, since the nano-
devices are present everywhere. We know that in magnetic storage systems,
microelectromechanical / nanoelectromechanical systems and other industrial applications,
the nanotribology is present. The magnetic storage industry continuously develops, since in
1956 the areal density was 2000 bit/in2, reaching in 2005, 1 Tbit/in
2. The present disk drives
use a lubricant film on magnetic hard disks, ensuring a longer durability, given that a relative
motion between magnetic medium and a read-write magnetic head is present.
In this situation, the tribology was replaced by micro and nanotribology, a research field
that enjoys the attention of increasingly more scientists around the world. As a consequence
of this, the traditional analysis methods are no longer valid, new and challenging one being
present. The results of experiments have revealed intriguing properties of the lubricant
nanofilms, but their analysis is not complete.
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The film lubricant properties are not the same at different scales. Viscosity is one of the
significant of these differences. Therefore, to gain a better fundamental understanding of the
involved phenomena, the molecular dynamic simulations are widely used to characterize the
lubricant film properties [1-3]. Thin film lubricants being subject to large shear rates, the
effect of shear thinning is significant. The shear rate is varied by maintaining constant film
thickness and changing the wall speed. But important is the fact that viscosity at a given shear
rate (for a film thickness and wall speed) may not be the same to the same shear rate, but for
other film thickness and wall speed. In this paper the viscosity, or better say, shear viscosity,
is calculated for seven wall speed and six pressures.
SIMULATION METHOD
In these days, searching into the molecular phenomena of confined thin lubricant films,
the molecular dynamics simulations has been proved to be an effective tool. Given the many
applications of the perfluoropolyether lubricants, our attention are focused on PFPE-Z, film
confined between two parallel solid gold walls, with an fcc lattice [4]. The system
temperature (300 K), the total number of particles and the total kinetic energy are
conservative.
In this paper, the molecular structure was obtained using the HyperChem software (Fig.
1) [5]. The analysis must be very carefully, because there are three types of atoms, carbon,
fluorine and oxygen. Consequently, we need to consider the bond bending component into
COC, CCO, OCF, FCF, and CCF terms, the bond stretching contribution into CC, CO, and
CF terms, and the bond torsional component into FCCO, OCCO, COCF, COCC, and FCCF
terms.
Fig. 1. The molecular model of PFPE-Z (C8F18O4).
Carbon atoms are gray, fluorine is white, and oxygen atoms are black.
The present simulations of thin film lubrication were run using non-equilibrium
molecular dynamics (NEMD). Molecular dynamics tracks the motion of atoms and molecules
as a function of time. For this motion we are using a set of coupled differential equation, this
being
2
2( ), 1, ,i i i tot i
dm r E r i n
dt (1)
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where im is mass, ir
is position of atom i, Etot is potential energy and n is the number of atoms
in system [6]. The potential energy gives the information about intermolecular and
intramolecular interactions. The interactions between the atoms of molecules are described by
the AMBER (Assisted Model Building and Energy Refinement) force field, namely [4]
2 2
0 0 0 12 6( ) ( ) [1 cos( )] .
2
ij ij i jntot r
bond angle dihedrals i j ij ij ij
A B q qVE K r r K n
R R R
(2)
The wall-molecule potential is given by Lorentz-Berthelot mixing rule [7]. The
molecular simulations were run with the Large Atomic/Molecular Massively Parallel
Simulator (LAMMPS) [8]. The simulation model of the thin lubricant film confined between
two solid walls is viewed in the Fig. 2.
Fig. 2. Snapshot of the simulation cell
The ―structure‖ of the walls is stratified. One wall contains three ―layers‖, the upper,
the middle and the upper layer. We apply the load on the upper layer, the lowest layer being
in contact with the thin lubricant film.
The layer between them (the middle one) is keep at constant temperature (Langevin
thermostat). Both walls, the upper and the lower one, exhibit the same structure. In order to
impose shear on the fluid, only the upper wall is moved at different constant velocity [9].
Seven different wall speeds were evaluated: 3, 4, 5, 6, 7, 8 and 9 m/s. So, the sliding
simulations are performed by keeping the lower wall fixed.
In order to investigate the both effects, of load and velocity respectively, on frictional
behavior of the thin lubricant film, the upper wall is supporting different constant loads (0.1,
0.5, 1.0, 1.5, 2.0, 2.5 GPa) for each mentioned velocity [10]. This constant pressure is applied
to the rigid part of the top wall in the z-direction (Fig. 2). The thicknesses of the investigated
films were 2.1 nm (50 PFPE-Z molecules) and 1.5 nm (25 PFPE-Z molecules).
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RESULTS AND DISCUSSION
Focusing on the velocity profiles of lubricant films (Fig. 3), we are able to say that
during shearing, the lubricant has different behaviors at the walls. First of all we encounter the
stick and slip phenomenon, which is determined by load and sliding velocity.
Fig. 3 Velocity profile: (a) 8 m/s sliding velocity, 1.5 nm lubricant film thickness;
(b) 4 m/s sliding velocity, 2.1 nm lubricant film thickness
For low load (L=0.1 GPa), the velocity profile (Fig. 3) show that the thin lubricant film
Fig. 3 Velocity profile: (a) 8 m/s sliding velocity, 1.5 nm lubricant film thickness;
(b) 4 m/s sliding velocity, 2.1 nm lubricant film thickness
For low load (L=0.1 GPa), the velocity profile (Fig. 3) show that the thin lubricant film
present two layers adsorbed on the walls. More precisely, the lubricant near the walls (3-4 Å)
became like a solid (frozen state), while the lubricant between these layers is fluid, with
Newtonian behavior.
This behavior is confirmed by the density profile (Fig. 4) where we can observe a
stratification of the film lubricant, confined between the walls. Increasing the load applied on
thin lubricant film, being now 1.0 GPa, we notice the same behavior for the lubricant film, in
addition occurring a strong slip near the walls (Fig. 3a). The velocity discontinuity between
the adjacent lubricant molecules and wall indicates that slip appear at this interface.
(a) (b)
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Fig. 4 Velocity profile: (a) 8 m/s sliding velocity, 1.5 nm lubricant film thickness;
(b) 8 m/s sliding velocity, 2.1 nm lubricant film thickness
By examining the radial distribution function (RDF), we obtain valuable information
about the state of the confined thin lubricant film whose thickness is 2.1 nm (Fig. 5). We
represent RDF of the lubricant at the beginning of the experiment and during the experiment.
We notice that in RDF pattern during the experiment appears a second peak, meaning that in
lubricant appear an ordinate structure, produced by the strong interaction between the
lubricant atoms and wall atoms. We suppose that the ordered structure of lubricant which
appears during the experiment is responsible for the viscosity changes.
Fig. 5 Radial function distribution for 1.5 GPa load and 6 m/s velocity profile
Information stated above is reinforced by the x-position of the lubricant atoms (Fig. 6),
confirming the stick and slip phenomena at the both wall.
(a) (b)
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Fig. 6. x-position of lubricant atoms as a function of time: (a) 2.1 nm, v=6 m/s, L=1.0 GPa; (b) 1.5 nm, v=6 m/s,
L=1.0 GPa
Going further, our attention is focused on shear viscosity [4], being evaluated as the
ratio of shear stress, xz , to effective shear rate, ,
xz .
(3)
In order to calculate the viscosity, the slope of linear part of velocity profile was used,
where we have a Newtonian behavior for the lubricant film.
Fig. 7 Shear viscosity as a function of pressure, 2.1 nm thickness
(a) (b)
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Fig. 8 Shear viscosity as a function of shear rate (shear thinning), 2.1 nm thickness
As we can see, on low load, the Barus low is respected, p
0e , while at high
pressure does not work properly (Fig. 7). The dependence of shear viscosity on shear rate is
given by power law, , where , generally lower than one, is a constant depending on
system, conditions and type of lubricant molecules (Fig. 8).
CONCLUSION
In this paper we investigated confined PFPE-Z thin film using molecular dynamics
simulations. The attention was focused on two nanometric thicknesses for the lubricant film,
only the upper wall being moved at constant shear velocity, while the bottom wall was fixed.
In the same time, the upper wall was supporting constant load (pressure). The simulations
were done for different shear velocity of the upper wall and different loads, but during one
simulation this parameters were constant. Our investigation reveals a film lubricant
stratification and appearance of a second peak during the experiment, meaning the presence of
an ordinate structure. Further, we evaluated shear viscosity, first, as a function of pressure
and then as a function shear rate.
ACKNOWLEDGMENT The authors would like to thanks to PrivDoz. Dr. rer. nat. Dipl. -Phys. András Vernes,
DI Dr. Stefan Eder, and Univ.-Prof. Dipl.-Ing. Dr. Friedrich Franek from Austrian Center of
Competence for Tribology (AC2T research GmbH), for their support and assistance.
REFERENCES
[1] A. Jabbarzadeh, P. Harrowell, R.I. Tanner, Very Low Friction State of a Dodecane
Film Confined between Mica Surface, Physical Review Letters, 94, 2005, 126103
[2] A. Martini, Y. Liu, R.Q. Snurr, Q.J. Wang, Molecular dynamics characterization of
thin film viscosity for EHL simulation, Tribology Letters, 21 (3), 2006, 217-225
[3] N.V. Priezjev, Shear rate threshold for the bou ndary slip in dense polymer films,
Physical Rewiew E, 80(3), 2009, 031608
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56
[4] C. Pirghie, A.C. Pirghie, S. Eder, F. Franek, PFPE-Z Lubricant Thin Films in
Molecular Dynamics Simulations – Shear thining and Friction law, Optoelectronics and
Advanced Materials – Rapid Communications, 7 (5-6), 2013, 434-438
[5] HyperChem is distributed by Hypercube, Inc.
[6] K. Tanaka, T. Kato, Y. Matsumoto, Molecular Dynamics Simulation of Vibrational
Friction Force Due to Molecular Deformation in Confined Lubricant Film, Journal of
Tribology, 125, 2003, 587-591
[7] A. R. Leach, Molecular Modeling Principles and Applications 2nd ed., Pearson
Education Limited, Harlow, 2001
[8] S. J. Plimpton, Journal of Computational Physics, 117, 1, 1995
[9] C. Pirghie, S. Eder, G. Vorlaufer, F. Franek, Viscosity oh Highly Confined PFPE-Z
Nanofilms with Molecular Dynamics, WTC 2013, 5th
World Tribology Congres, Torino,
Italy, 8-13 September 2013
[10] C. Pirghie, A.C. Pirghie, Investigations of Nanotribological Systems using
Molecular Dynamics Simulations, International Conference on EHD Lubrication and
Traction, 25-27 octombrie 2012, Proceedings of VAREHD, vol. 16, 2012, 53-60
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57
STATISTICAL PROCESSING OF CENSORED DATA
UNDER ACCELERATED RELIABILITY TESTING FOR RADIAL
BALL BEARING
Lect. PhD.Eng. Sebastian Marian ZAHARIA, Department of Manufacturing Engineering,
Technological Engineering and Industrial Management Faculty, Transilvania University of
Brasov, Romania, e-mail: [email protected]
Assoc. PhD.eng. Cristin Olimpiu MORARIU, Department of Manufacturing Engineering,
Technological Engineering and Industrial Management Faculty, Transilvania University of
Brasov, Romania, e-mail: c.morariu@unitbv. ro
Abstract: The organizing and the execution out of the reliability testing of the products represent complex
activities from an organizational standpoint and are also big resources consumers. Reliability test
elements, conditions and other factors are determined based on customer needs for reliability, by clarifying
the environmental and time conditions under which devices will be used and the failure definitions The
paper is targeted at the study of the reliability parameters and the lifetime of radial ball bearings using
reliability testing. For the case study it used ALTA 7 software what provides a complete array of analysis
tools for data from reliability tests. The case study is represented by a set of data from accelerated tests
using censored data type.
Keywords: reliability, ball bearings, life, reliability testing, censored data.
1. INTRODUCTION
Reliability test is the general term for reliability determination tests and reliability
compliance tests. In other words, reliability characteristics values (failure rate, reliability,
mean life, MTTF, etc.), which are scales representing the time-dependent quality of products,
are estimated and verified statistically from the test data. These tests also play an important
role in improving reliability by analyzing failures which occur during tests and clarifying
these failure mechanisms. Reliability tests provide the greatest effects when statistics and
failure physics function reciprocally [1].
The reliability tests have a great importance, aiming either to determine, either to check
the reliability characteristic of a product, if this is established in a predictive way. The
reliability tests are extremely necessary and they have a decisive role in improving the
technical solutions and in increasing the performances. The essential problem of reliability
tests is the testing duration, which is generally comparable with the product‘s useful life time
[2]. A too long testing duration renders the reliability test useless. These reliability tests help
us with: the determination of the statistical pattern of the operating time without failures; the
estimation of the pattern‘s parameters; the realization of predictions on the reliability of the
products. The reliability tests precisely analyze the phenomenon of failure, quantified either in
operating time, either in number of cycles. By reliability test we understand an experiment
organized in order to determine the reliability parameters for a well-defined product. The
organization of reliability tests represents a problem that requires on the specialist‘s part a
good theoretical background and a vast practical experience.
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In order to realize reliability tests we must take into account the following aspects:
a) A previously determined n number of products that will be subjected to testing
b) A testing plan that includes the following aspects: the selection of stress parameters,
which will determine the failure mechanisms specific to the product; the determination of
environmental conditions in which the experiment takes place, that has to take into account
the actual conditions in which the products will function in real operation
c) Instructions regarding the adequate type of test and the methods of calculation, in
order to estimate the reliability parameters
d) A test chart where the experimental data are recorded and the statistical calculations,
as well as the chronological recording of observations and interventions, are made
e) Testing stands, testing equipment, auxiliary materials and qualified staff in order to
realize the test.
The most used reliability tests are the following [3]:
Complete tests (type n out of n) - in these tests n products of the same kind, the
experiment being considered finished when all of the n products have failed. This
kind of tests can‘t be applied in all the situations, because in the case of expensive
products is uneconomical, and in the case of products that have a relatively long
life time by nature, the experiment will take too long. Nevertheless, this kind of
experiment has the advantage that the obtained information is complete, meaning
that at the end the failure times for all the products subjected to testing are
determined;
Censored tests (type r out of n) - are commonly used and they consist of subjection
to testing of n products of the same type, the experiment being considered finished
after the failure of r<n tested products; obviously, the r number is previously
determined, usually by technical, economical and statistical considerations. At this
type of experiments, the testing duration is random, because it‘s unknown when
the r-th product will fail; the information here is incomplete, because in the end we
will have only r, instead of n experimental data
Truncated tests (with a fixed testing time) - a n number of products are subjected
to testing, but the experiment doesn‘t stop according to the number of failed
elements, but according to a tr time, previously set, a period during which the
testing takes place. After this testing time (previously set) has passed, the
experiment is considered finished.
The testing methodology about to be used has a direct economical impact, because in
every test the following terms intervene: the cost of the tested product; the total cost of the
experiment; the time consumed for testing and for the statistical processing of the data
resulted from testing. Therefore, the selection of a specific type of test is a managerial
decision that has to be taken by a responsible authority. Also, in the follow-up of the results of
the statistical processing, we will propose certain corrective technical and economical actions,
aimed directly at the quality and reliability of the product in question [4].
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2. CASE STUDY
Single Row Radial Ball Bearings - 6004 2RS is a high quality bearing used in axial fans,
motors, drive axles, clutch, idler wheels, HVAC, snow mobiles and many other industrial
applications. Bearings are made of chrome steel, pre-lubricated with grease and have rubber
seals on both sides to protect the bearings from dust or any other types of possible
contamination. In the table 1 is described the geometric and constructive aspects of the radial
ball bearings type 6004, used for the accelerated reliability testing. The radial ball bearings
type 6004 is described in figure 1 [5,6,7].
Tab. 1. The parameters of the ball bearings type 6004
Fig. 1. The radial ball bearings type 6307
2.1. Experimental data
Using the testing stand of the ball bearings, we realized accelerated reliability tests with
the purpose of reducing the testing duration and the material costs associated with these tests.
The results obtained at the accelerated reliability testing (table 2) of the ball bearings for the 3
accelerated stress regimes are: for the first accelerated stress regime 8000 N; for the medium
accelerated stress level 9000 N and for the maximum accelerated stress level 10000 N. Tab. 2. Number of cycles until failure – bearing load
No. State
F or S
Time to
F or S
Bearing Load
[N]
1. F 1234 8000
2. F 1423 8000
3. F 1567 8000
4. F 1790 8000
5. S 2000 8000
6. S 2000 8000
7. F 789 9000
8. F 897 9000
9. S 1000 9000
10. S 1000 9000
11. F 456 10000
12. F 490 10000
13. F 543 10000
14. F 589 10000
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2.2. Statistical processing
Once you have selected an underlying life distribution (Weibull) and life-stress
relationship (inverse power law) model to fit your accelerated test data, the next step is to
select a method by which to perform parameter estimation. Simply put, parameter estimation
involves fitting a model to the data and solving for the parameters that describe that model. In
our case, the model is a combination of the life distribution and the life-stress relationship
(model). Available methods for estimating the parameters of a model include the graphical
method, the least squares method and the maximum likelihood estimation method. ReliaSoft ALTA 7 - www.ReliaSoft.com
Life vs Stress
Beta=6,861; K=3,603E-26; n=5,677
Bearing Load
Lif
e
7000 1400010000100
10000
1000
Life
Data 1Inverse Power LawWeibull7000F=10 | S=4
Eta L ine8000
Stress Level PointsEta PointImposed Pdf
9000Stress Level PointsEta PointImposed Pdf
10000Stress Level PointsEta PointImposed Pdf
sebastian zahariaUniversitatea Transilvania
Mean life of ball bearing
is 3846 hrs
ReliaSoft ALTA 7 - www.ReliaSoft.comFailure Rate vs Time
Beta=6,861; K=3,603E-26; n=5,677
Time
Fa
ilu
re
R
ate
0 200004000 8000 12000 160000
10
2
4
6
8
Failure Rate
Data 1Inverse Power LawWeibull7000F=10 | S=4
Failure Rate L ine
sebastian zahariaUniversitatea Transilvania Brasov
a) Life vs. Stress plot b) Failure rate vs. Time plot
Fig. 2. Reliability parameters
Once you have calculated the parameters to fit a life distribution and a life-stress
relationship to a particular data set, you can obtain the same plots and calculated results that
are available from standard life data analysis such as:
Reliability Given Time - the probability that a unit will operate successfully at a
particular point in time under normal use conditions;
Probability of Failure Given Time – the probability that a unit will be failed at a
particular point in time under normal use conditions. Probability of failure is also
known as "unreliability" and it is the reciprocal of the reliability;
Mean Life - The average time that the unit in the population are expected to operate at
a given stress level before failure (figure 2.a). This metric is often referred to as "mean
time to failure" (MTTF) or "mean time before failure" (MTBF). A variety of life
characteristics, such as B(10) life or eta, can be displayed on the plot. This plot
demonstrates the effect of a particular stress on the life of the product;
Failure Rate: The number of failures per unit time that can be expected to occur for the
product at a given stress level (figure 2.b);
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Warranty Time - the estimated time when the reliability will be equal to a specified
goal at a given stress level;
B(X) Life - the estimated time when the probability of failure will reach a specified
point (X%) at a given stress level (figure 3.a);
Acceleration Factor - a unit less number that relates a product's life at an accelerated
stress level to the life at the use stress level (figure 3.b);
Probability Plot - a plot of the probability of failure over time. This can display either
the probability at the use stress level or, for comparison purposes, the probability at
each test stress level;
ReliaSoft ALTA 7 - www.ReliaSoft.comAcceleration Factor vs Stress
Beta=6,861; K=3,603E-26; n=5,677
Bearing Load
Ac
ce
lera
tio
n F
ac
tor
7000 100007600 8200 8800 94000
10
2
4
6
8
Acceleration Factor
Data 1Inverse Power LawWeibull7000F=10 | S=4
AF L ine
sebastian zahariaUniversitatea Transilvania Brasov
a) BX Life b) Acceleration Factor vs. Bearing Load
Fig. 3. Reliability parameters
Reliability vs. Time Plot: A plot of the reliability over time at a given stress level. A
similar plot, unreliability vs. time, is also available (figure 4.a,b);
Probability density function plot - represents a plot of the probability density function
(pdf) at a given stress level. The pdf plot shows the probability density function of data
over time at the specified use stress level. This allows you to visualize the distribution
of the data set;
The Cox-Snell Residuals plot is similar to the standardized residuals plot, except the
line is plotted on an exponential probability plotting paper and is on the positive
domain (figure 5.a);
Residuals Plots - plots of the residual values that have been assigned, via regression
analysis, to each point in a data set. These plots provide a tool to assess the adequacy
of the model used to analyze the data set (figure 5.b).
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ReliaSoft ALTA 7 - www.ReliaSoft.comReliability vs Time
Beta=6,861; K=3,603E-26; n=5,677
Time
Re
lia
bil
ity
0 60001200 2400 3600 48000
1
0,2
0,4
0,6
0,8
Reliabil ity
Data 1Inverse Power LawWeibull7000F=10 | S=4
Data PointsReliabil ity L ine
sebastian zahariaUniversitatea Transilvania Brasov
ReliaSoft ALTA 7 - www.ReliaSoft.comUnreliability vs Time
Beta=6,861; K=3,603E-26; n=5,677
TimeU
nre
lia
bil
ity
0 60001200 2400 3600 48000
1
0,2
0,4
0,6
0,8
Unreliabil ity
Data 1Inverse Power LawWeibull7000F=10 | S=4
Data PointsUnreliabil ity L ine
sebastian zahariaUniversitatea Transilvania Brasov
a) Reliability function b) Unreliability function
Fig. 4. Reliability parameters
ReliaSoft ALTA 7 - www.ReliaSoft.com
Cox-Snell Residuals
Beta=6,861; K=3,603E-26; n=5,677
Residual
Pro
ba
bil
ity
0 102 4 6 81
99
50
90
95
Cox-Snell Residuals
Data 1Inverse Power LawWeibull
Residual L ine8000F=4 | S=2
Residuals9000F=2 | S=2
Residuals10000F=4 | S=0
Residuals
sebastian zahariaUniversitatea Transilvania Brasov
ReliaSoft ALTA 7 - www.ReliaSoft.com
Standardized vs Fitted Value
Beta=6,861; K=3,603E-26; n=5,677
Eta
Re
sid
ua
l
100 100001000-10
10
-6
-2
2
6
0
Standard - Fitted
Data 1Inverse Power LawWeibull8000F=4 | S=2
Residuals9000F=2 | S=2
Residuals10000F=4 | S=0
Residuals
sebastian zahariaUniversitatea Transilvania Brasov
a) Cox Snell Residuals b) Standardized vs. Fitted Value
Fig. 5. Reliability plots
3. CONCLUSION
In accelerated reliability testing, products are exposed to stress levels higher than
those at normal use in order to obtain information in a quickly time. In this paper we expand
the limits of performing the accelerated life tests on a product from the automotive field (ball
bearing). The implementation of accelerated reliability tests on the products from the
automotive field has produced a significant reduction of the testing time.
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We can observe that, by using the accelerated life tests, the testing time has been
reduced by 8 times. Given the fierce competition existing on the automotive industry market
and considering the reduction in testing time and therefore the optimizing of the products‘ life
cycle, many companies will implement and develop various methods of obtaining data as fast
as possible regarding the reliability and quality of the products.
4. REFERENCES
[1] Zaharia S.M, Martinescu I., Reliability tests, Transilvania University Press, Brasov,
2012.
[2] Nelson W. Accelerated Testing: Statistical Models, Test Plans, and Data Analysis, Wiley,
New Jersey, 2004.
[3] Klyatis L.M., Accelerated Reliability and Durability Testing Technology, Wiley, New
Jersey, 2012.
[4] Collins J.A., Busby H.R., Staab G.H., Mechanical Design of Machine Elements and
Machines, John Wiley & Sons, Wiley, 2010.
[5] Guangbin Y. Life Cycle Reliability Engineering, Wiley, New Jersey, 2007.
[6] Harris T.A., Kotzalas M.N., Advanced Concepts of Bearing Technology, Rolling Bearing
Analysis, CRC Press, New York, 2006.
[7] Bertsche B., Reliability in Automotive and Mechanical Engineering, Springer, 2008.
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DYNAMIC STUDY OF THE R-RTT MECHANISM
ASSISTED BY AUTODESK INVENTOR
Assoc. Prof. Dr. Marin NEACSA, University POLITEHNICA of Bucharest,
Assoc. Prof. Dr. George ADÎR, University POLITEHNICA of Bucharest,
Assoc. Prof. Dr. Victor ADÎR, University POLITEHNICA of Bucharest,
Eng. Ancuta ADÎR, Grigore Cerchez Technological College, Bucharest
Abstract: In this paper is introduced the way of using of the Dynamic Simulation Module from
Autodesk Inventor Professional, for the dynamic analysis of an R-RRT mechanism . As example, it
was chosen a mechanism used to operate refrigerators compressors.
Keywords: Dynamic study , mechanism, refrigerator compressor, Autodesk Inventor Professional.
STRUCTURE AND OPERATION OF THE MECHANISM STUDIED
In the manufacturing process of refrigerators there are used R-RTT mechanisms. The
piston has a translation motion inside the compressor‘s cylinder. The leading element (1) of
the mechanism, is the rotor of the electric motor that drives the compressor. This one is joined
to the engine‘s stator (this joint is marked by R, the first letter from the structural relationship
R – RTT). The rotor has (at one of the ends) a crank, as leading element, connected to dyad
RTT, made by 2 elements, namely the piston and a rock slide.
The rock slide is articulated on the crank an is gliding in a piston guide, positioned
perpendicular on its translation axle inside the compressor‘s cylinder. The flow of the cooler
agent in the compressor‘s cylinder is ordered by 2 valves, one for intake and the other for
discharge. The distance between the 2 joints of the crank is 0,0065 m. The translation axle of
the piston in cylinder is passing through the revolute axle of the crank, against the engine‘s
stator, against base and the chassis of the electric motor. In Fig. 1 is presented the most
important piece of the mechanism, namely the piston with the guiding system perpendicular
on the cylinder‘s axle.
The rotation speed of the driving element (motor‘s rotor) is considered as constant:
n1= 2690 rot/min.
The elements of the mechanism are made by steel and the masses and the mechanical
inertia moments of the elements are automatically established by AUTODESK INVENTOR.
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Fig. 1 The piston and the guiding system
The phases of the theoretical diagram, Vp , of the compressor are [1]:
1-2 polytropic compression;
2-3 discharge;
3-4 recoil of the fluid in the dead space;
4-1 aspiration
For the analysis of the mechanism R-RTT of a compressor with freon, there are
considered the following data:
- aspiration pressure in installation: 182805afp [N/m2 ];
- medium pressure loss for aspiration: afaf pp )1.005.0( ;
- discharge pressure in installation: 850050refp [N/m2 ];
- medium pressure loss for discharge: refref pp )15.01.0( ;
- polytropic exponent at rebound: 08.1dn ;
- polytropic exponent at compression: 1.1cn ;
- the technical compressor with piston has a dead space 0V ; the relative dead space ,
is:
05.0/0 sVV (1)
where sV is the aspiration volume (space volume necessary to the piston‘s displacement):
ABd
Vs
4
22
(2)
d - piston‘s diameter
AB - crank‘s radius
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66
0V , the volume of the dead space, is calculated with the relation:
ABd
VV S
4
22
0 (3)
- the discharge pressure in compressor is: refrefr ppp ; it is taken into
consideration refref pp 1.0 ;
- aspiration pressure in compressor: afafa ppp ; it is considered
afaf pp 05.0 ;
- Ecuation of the polytropic curve, at rebound:
dn
rx
AB
xpp
2
(4)
where x represents the piston‘s stroke from the upper dead point to the lower dead point;
- stroke x4, corresponding to the end of rebound, is established by the relation:
124 dn
a
r
p
pABx (5)
- Ecuation of the polytropic curve, at compression:
cn
ax
AB
xpp
2
1 (6)
- stroke x2, coresponding to the end of compression, is established by the relation:
cn
r
a
p
pABx )1(22 (7)
Displacements 321 , , xxx and 4x , necessary to establish the pressure variation diagram
against stroke, are:
ABx 21 (8)
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cn
r
a
p
pABx )1(22 (9)
03 x (10)
124 dn
a
r
p
pABx (11)
The corresponding pressures to each operating field are:
- for ],[ 43 xxx ,
dn
rx
AB
xpp
2
(12)
- for ],[ 14 xxx , ax pp (13)
- for ],[ 21 xxx ,
cn
ax
AB
xpp
2
1 (14)
- for ],[ 32 xxx , rx pp (15)
THE DYNAMIC STUDY OF THE MECHANISM ASSISTED BY AUTODESK
INVENTOR PROFESSIONAL
To study the dynamics of the R-RTT analyzed mechanism, it is necessary to follow
the stages:
1) Modeling in Inventor of the mobile elements of mechanism, namely: rotor of the
electric motor (with the crank fixed on it), piston and the rock slide. For these elements, is
important to know the mass and the mechanical inertia moments, automatically established by
Inventor. It is not relevant the rigorously modeling of the base, of the fixed part (the engine‘s
chassis, compressor‘s cylinder etc).
2) Modeling of the assembly of the elements of mechanism
3) Dynamic simulation of the mechanism with Dynamic Simulation Module from
Autodesk Inventor Professional.
Further on, we shall refer to the last stage, namely to the dynamic simulation of
mechanism. After modeling the assembly of elements, it is selected from Environments Tab
the icon Dynamic Simulation.
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So, it appears the window depicted in Fig. 2, in which it is selected the button marked
by 1, for editing the properties of couples. If the restrictions imposed when modeling the
assembly of the elements of mechanism were right, the mechanism‘s couples are
automatically and right modeled in Dynamic Simulation Module. To edit the properties of
the revolute couple between the leading element and the engine‘s stator, it is selected in
browser the respective couple and it is pushed the right button of the mouse, operation marked
by BdM further on [2].
Fig. 2 Window Simulation Player
It appears the window from Fig. 3. To specify the revolute speed, that in Inventor is
considered in deg / s, it is selected the button dof 1(R), marked by 1, then it is selected the
button 2 and then there are selected the buttons marked by 3 and 4 on the figure. After that, it
is possible to specify the revolute speed in the window marked by 5.
To edit the properties of the translation couple, between the piston and the
compressor‘s cylinder, it is selected in browser the respective couple and it is pushed the right
button of the mouse. It appears the window depicted in Fig. 4. To specify the necessary data
to calculate the forces in the translation couple between piston and cylinder, it is selected the
icon marked by 1, then is ticked the button marked by 2, it is specified the friction coefficient
in couple in the window marked by 3 ands then is pressed twice, succesively, the left button
of the mouse, with the prompter put on the window marked by 4.
As a result, it appears the window depicted in Fig. 5. It is selected the icon marked by
1, that allows to import the values of the pressure force against the piston, from a text file.
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The values of the pressure force picked up are present in the window marked by 2 and
the variation diagram of the pressure force against the piston‘s position is presented in the
window marked by 3.
Fig. 3 Specifying of the revolute speed Fig. 4 Editing of data for calculation forces
in the couple piston – cylinder
Fig. 5 Import of the values of the pressure force against piston
To obtain the variation of the balancing moment in the crank‘s joint at the base,
corresponding to the imposed rotation speed, it is selected from the menu Output Grapher. It
appears the window presented in Fig. 6; it is selected the revolute couple between the crank
and base, indicated in Fig. 1 and then it is ticked the button marked by 2,corresponding to the
balancing moment. The diagram obtained can be exported in MS Excel.
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70
Fig. 6 Selecting of the balancing moment
in the joint of the crank at the base
CONCLUSIONS
The dynamic modeling of mechanisms can be relatively easy studied by using the
Dynamic Simulation Module from Autodesk Inventor Professional. As a result, after this
modeling, it is posible to optimize the design of these mechanisms to increase their
competitiveness.
REFERENCES
1) Moise, V., ş.a., Analiza mecanismelor aplicate, Editura PRINTECH, 2007
2) Stăncescu, C., Modelare parametrică şi adaptivă cu Inventor, volumul 2, Editura FAST,
Bucureşti, 2010
3) http://knowledge.autodesk.com/support/inventor-products/learn-
explore/caas/CloudHelp/cloudhelp/ENU/123112/files/inventor-2014-tutorials-html.html
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THE FAILURE MODES AND THEIR REMEDIATION PROGRESSIVE
CAVITY PUMPS USED IN OIL PRODUCTION
Lecturer PhD STAN Marius , Petroleum - Gas University of Ploiesti
Abstract: The primary objective for this project was to design and select a suitable PC pumping system to
meet the applications production and lift requirements and proposing solutions to improve the operation of
the entire extraction system. Information contained in the “PC Pump Design Form” was used to develop a
simulated model with a specialized. The main difficulties that characterize the work of the probe are:
abrasion, corrosion, paraffin deposition, gas, oil viscosity, scale deposition and wellbore trajectory.
Keywords: analysis, elastomer, sustainability, modeling, reliability
1. INTRODUCTION
Today, primary heavy oil and bitumen applications are almost exclusively produced
with PC pumping systems.
Recent estimates characterize nearly 50% of the world's liquid hydrocarbon as having
a gravity of less than 20° API1 These reserves are generally referred to as bitumen and heavy
oil, and large deposits are abundant in Canada, Russia, Venezuela and China,
The most distinguishing characteristic of these fluids is their high viscosity which
typically ranges between 500 and 15,000 cp for heavy oil and may approach 100,000 cp for
bitumen,
These viscous crudes are commonly located in shallow reservoirs (300 to 600 depths)
and individual wells usually produce these fluids at low to moderates rates (I to 70 m3/day).
In order to achieve economic production rates, most wells must be pumped at low
bottom hole pressures which magnify the adverse effects of any produced gas, In addition,
heavy oil and bitumen are typically withdrawn from poorly consolidated reservoirs which are
prone to sand production that can exceed 30% by volume. The close well spacing required for
viable field development often leads to the preferential use of directional and horizontal wells.
One of the most important mining industry is the exploitation of deposits of
hydrocarbon fluids through wells.
The use of these natural resources as a source of energy, fuel, petrochemical
feedstock‘s or in the pharmaceutical industry has made a fluid hydrocarbon extraction
industry of prime importance.
Labor productivity growth in the oil industry called centralized monitoring wells in the
pumping operation, computer-aided data transmission to remote processes automation and
control devices adaptation of stopping and starting of electric motors, test probes, detection
and diagnosis of faults. Also in this area is remarkable development of complex computer
programs for optimization of the choice of equipment and operation of facilities.
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Oil and gas industry is characterized generally by conveying large amounts of fluids:
oil and gas accompanied by salt water and sometimes hard particles (sand) which are
extracted from the wells productive strata, then separated and stored installation surface. [12].
The material they are made of deep and surface equipment for extraction of oil wells are
subjected to wear caused by fluids inside and outside the vehicle. Often these processes are
produced with high intensity and leads to considerable difficulties such as:
• Premature wear and decommissioning of equipment before normal time;
• Sudden interruption of processes that lead to loss of production due to accidents or
technical, requiring large expenditures for remediation;
• Breakage of tubular material (tubing, oil pipelines and salt water) that generates high
production and investment losses supplementary. [8]
The main difficulties that characterize the work of the probe are: abrasion, corrosion,
paraffin deposition, gas, oil viscosity, scale deposition and the drill hole.
2. FORMULATIONS The chemical Eastover define the applications for which a PCP is suitable. Rubber.
The most cannon lassoers are rubber formulations. The term ―Rubber‖ is usually applied to
formulations based on the isoprene and/or butadiene polymer chains.
This discussion is confined to butadiene formulations Rubbers still offer the best
combinations of mechanical properties and resistance to chemical attack for most
applications.
The additives are mechanically mixed with a kneading action intothe plastic,
elastomeric butadiene compound. The mixture is then moulded and vulcanized Vulcanization
is the ―cedcing‖ process which speeds up the cross-linking of the additives with butadiene.
Usually there are a dozen or more additives to butadiene to make a rubber. Some are
iinstilcient research has been it and make it a science.
Acrylonitrile, oflen referred to as ‗nitrile‖, is also a carbon chain. It increases some of
the mechanical properdes of rubber while decreasing others. Within limits, the properties
which are decreased are still within the desirable range, which is why acrylonitrile is the most
used additive. In addition to its on mechanical properties, acrylo-nitrile greatly enhances the
resistance of rubber to aromatic solvents. It will be know that the acrylonitrile sdditive has a
triple bond. However, acrylottitrile rubbers will pump high water cut oil wells because
rubbers are oilwettable and attract a protective Iiirn of oil which prevents absorption of water
even in low oil cut production.
HNBR Hydrogenated acrylonitrile butadiene is another elastomer which is being
offkred by the suppliers of PCP ‗s.
To make HNBR, hydrogen is added to nitrile rubber to reduce or eliminate the
residual unsaturation. Research in the nuclear industry has shown that HNBR is better than
rubber at resisting H$. This elastomer has better resistance to temperature also. A problem
with HNBR is that there is not as large a body of knowledge of additives to make it as
resistant to the aromatic solvents as high acryIonitrile rubber. More research is required to
fmd additives which will provide the same aromatic solvent resistance as high nitrile rubber.
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73
Fluorocarbon and Perfluorocarbon. There are elastomers in the fluorocarbon and
perfluorocarbon groups which are excellent at resisting chemical attack and high
temperatures. However, the practical problem with these elastomers is that they have never
been successfully moulded in large quantities.
The moulding difficulty with fluorocarbon can be overcome by making a copolymer
with butadiene. This wmpromises the chemical resistance of tluomcwbm but results in an
elastomer with higher chemical and temperature resistance than rubber.
Polyethylene chlorosulphide is an elastomer with excellent abrasion resistance and
other mechanical properties similar to rubber. However, it has no resim to light hydrocarbon
liquids, although it does have good resistance to CO. Us resistance to water is superior to
rubber.
2. PROBLEMS ENCOUNTERED IN PUMPING HELICAL
Three most common pc pump failures in wells, [13]:
Overheating
Cause – Gas entering the pump causes the Elastover to swell and overheat. Pumping
the well off, or running dry.
Result - Can result in hardening, then shearing of the elastomer. Gas may also cause
blistering of the stator or surface cracking of the rotor. Any of these issues may cause damage
to the seal between the rotor and stator, even before failure.
Solids
Cause - High amounts of solids going through the pump or solids settling back
through the discharge or tubing.
Result - A plugged pump resulting in broken rods or rotors.
Incorrect operation of the pump
Cause - Due to the fluid, gas, and solids, it is critical to operate the pump within the
recommended parameters.
Result - Can cause additional stress to the system.
The presence of free gas at pump suction directly affects its efficiency by reducing the
volume of fluid pumped through the pump. [9,10]
Spiral pump can pump the fluid in limited quantities of product gas is taken to the
surface, thus overcoming the friction pressure loss.
The lack of adequate amounts of fluid gives rise to conditions of "dry run", which
results in burning of the surface of the elastomer and the occurrence of cracks, cracks, etc..
In Figure 1 is shown that one can suffer wear elastomer under "dry run".
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74
Fig.1 Wear elastomer.
Materials and combinations of materials given in Table II for . metal parts , such as
pump housing , rotor shafts , etc and Table I pt . stator are made of any metallic material by
conventional processes .
Table I Stator are made of any material and recomandations for use
Helical type pumps
BORNEMAN
Materials for helical screw pump
stators
(Facts)
Recommendations for use
Code Title Temp
max
adm. 2)
Possible to use the:3) Not be used to:
702 NR natural Rubber 70
Aqueous media, abrasive organic
acids, alcohols, cetane, aldehydes,
organic fertilizer, cement paste,
grape marc
Ozone concentrated acids, fats, oils,
hydrocarbons.
718/731
SBR/B
R
Buna (Buna S)
Styrene-
butadiene
80 Water, aqueous media,
water sanitation, liquid ammonia, li
quid manure, someinorganic acids.
Like natural rubber, in addition to
ketone and ester.
703/729
(NBR)
Perbunan N 1)
Rubber nitrile
90 Some hydrocarbons, hydraulic
fluids, weak acids and weak acid
solutions, gasoline, mineral, animal
and vegetable oils and fats.
Chlorinated aromatic hydrocarbons,
ester, aldehyde, ozone strong acids.
704 CR Neopren 1)
Rubber
cloroprenic
STAS 10297-
75
90 Ozone, grease, oils, paraffinic or
naphthenic, aliphatic
hydrocarbons, reducing agents,
aqueous salt solutions.
Strong oxidizing acids
732/705
11R/CJ-
11R
Rubber butilic 110 Animal and vegetable fats and oils,
ozone, strong oxidizing chemicals,
acids and acid solutions.
Oil
707
CSM
Hypalon 1)
Rubber sulfonil
polyethylene
100 Alcohols, salt solutions, ammonia,
hydrogen peroxide, oxidizing
chemicals, oils, water, pulp,
chromic acid.
Concentrated acids oxidants
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75
716
EPDM
Rubber EPDM
Rubber
ethylene-
propylene
110 Ozone hot water, sulfuric acid,
animal and vegetable oils and fats.
As butyl rubber 11 R
724
ACM
Rubber
polyacrylic
STAS 10577-
76
120 Oils at high temperatures, oils
edible animals, latex, PVC pastes.
Water, aromatic hydrocarbons,
ketones, alkaline solutions, acids.
708
FPM
Vitan
Rubber
fluorocarbon
180 Aliphatic, aromatic or halogen
groups, oils, grease, acids.
Almost all liquids!
Ketones, chlorinated hydrocarbons,
acids, oxidizers.
712
HDPE
Polyethylene
High density
(HDPE)
90 Water, inorganic salt solutions,
acids and weak acid solutions,
aliphatic oils, fats
Petrol, chlorinated hydrocarbons,
acids, oxidizers
720
PA
Polyamide
(Nylon)
90 Bentin, petrol, some solvents,
hydrocarbons, water, alcohols,
ester, ketones, oils and fats,
minerals, anorganic salt solutions.
Acids
715
PUR
(AU)
Polyurethane
NPR
HNPR
70 Ozonated oils and fats; strongly
abrasive environments
Neoprene
719
PTFE
Teflon 1)
Polytetrafluoro
ethylene
250 Almost all liquids! Fluorine
1) The name or trade name registered.
2) The maximum temperature of the working fluid (standard values)
3) Only indicative information. For carry fluids seek further details.
Materials and combinations of materials given in Table I for . metal parts , such as
pump housing , rotor shafts , etc and Table II pt . stator are made of any metallic material by
conventional processes .
• Apart from standard materials such as gray cast iron or stainless steel resistant to
oxidation and acid ( major CrNi 18-8 or 18-10 ) special materials specific properties can be
used , eg stainless steel with molybdenum , titanium , niobium or copper nickel alloys with
high purity , such as brass , alpacana , titanium, bronze or light alloys , etc. .
• It is possible to use plastic or hard rubber in the construction of the pump body and
intake chambers . Actionarepot impeller or shaft as hard chrome or covered with various
materials in the connection .
It should be borne in mind that the Cr -Ni steels resistant to corrosion and acid can not
be hardened . The rotors of these materials require a hard layer of chromium which protects
them if you carry abrasive or corrosive environments .
As materials for stator and protection shirts cardan links offer data in Table II. Stator
can be used more plastics or elastomers , you can use any material with specific properties
depending on the particular case of operation. Usually black elastomer used in the food
industry use white elastomers .
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76
Table II is basically a guide for the use of different materials . stator and offers only
informative data . A better choice can be made using tables of strength and experience. In
case of doubt, have sent a sample of our material testing laboratory .
Table II - Materials elicoidal eccentric rotor pumps ( data information )
1 )
standard
material
Pump body and
intake, exhaust
flange
Rotor Shafts Drive
housing
sub
assembly
Standard version 1) by
type
H L R S K
V
M V B V
B
1 IRON GGL 25 Steel
17% Cr
1.4122
Steel
13% Cr
1.4021
IRON
GGL 25
®
®
®
1A STEEL 1.0308 Otel
1.0308
®
®
®
4 IRON GGL 25 Steel Cr-Ni-Mo-Ti
1.4571
IRON
GGl 25
®
®
4A HDPE (polyethylene) SteelCr-Ni
1.4301
HDPE
(polyethyl
ene)
®
10 STEEL 1.0308 Steel
17% Cr
1.4122
Steel
Cr-Ni
1.4301
IRON
GGL 25
®
®
11 Cr-Ni 1.4301 Steel Cr-Ni-Mo-Ti
1.4571
®
®
®
®
12 Cr-Ni 1.4408
13 Cr-Ni 1.4308 Steel Cr-Ni
1.4301
®
®
®
15 Brass C 2.4602
18 STEEL Cr-Ni-Mo
1.4408
Brass 2.4602
19 G-Al si 7 Mg
3.2374.6
SteelCr-Ni 1.4301
®
1 ) standard material that is in every model sold . Using other materials than those tabulated
may be made to almost all models to the pump. Combinations of materials of different parts
are possible in most cases.
The presence of solid particles in the fluid pump products reduce the battery usage and
efficiency of the pump coil.
The rotation of the rotor inside the stator rough and smooth soft and elastic leads to a
very good tolerance to pump sand and abrasive particles. Solids are suspended in cavities and
forward through the pump once the fluid displaced. Any particle of sand trapped between the
rotor and stator is pressed within elastic elastomer without damaging the pump. Figure 3 are
the wear on careo data may suffer rotor abrasion conditions.
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CONCLUSIONS
The study presented aims to warn of problems encountered in practice. PCP pumps
shows the same type of loss of durability regardless of the company that produces them. It is
significant correlation between the factors and factors of influence exploatatre, materials,
manufacturing technology, speed drive.
PCP pumps are extensively applied in operation. The choice of materials is very
important to take into account compatibility with the fluid in the tube. It is necessary to know
the physical and chemical properties of petroleum vehicle. You know the content of sand and
elastomer compatibility of gases or water .. u poatearde and stator is necessary to choose the
correct speed drive. Gases can diffuse into the elastomer due to aromatics. Pentre rotor speed
is chosen depending on the viscosity of the oil and sand content.
BIBLIOGRAPHY
1.*** Catalog Geremia.
2.*** Catalog Griffin-Legrand.
3.*** Catalog PCM Moineau Oilfield.
4.***Catalog Weatherford Eastern Europe SRL.
5.*** Composite Catalog of Oil Field Equipment and Services 1998-1999, World Oil a Gulf
Publishing Company Publication.
6.***Documentaţie Premium Artificial Lift Systems Ltd.
7.*** Documentaţie Weatherford Eastern Europe SRL.
8.Dumitru V., "Contribuţii la tehnologia extracţiei petrolului prin sonde în pompaj de
adâncime cu pompe cu construcţie specială".
9.Gabor Takacs., "Modern Sucker-Rod Pumping", Penn Well Publishing Company, Tusla,
1993.
10.Nelik, L., Brennan, J., Progressing cavity pumps, downhole pumps and mudmotors, Gulf
Publishing Company, Houston, 2005.
11. Stan Marius, Fiabilitatea sistemelor si aplicatii, Editura Universităţii Petrol – Gaze din
Ploieşti, ISBN 978-973-719-249-3, 2010
12. Stan Marius, SUSTAINABILITY ASPECTS OF PROGRESSIVE CAVITY PUMPS
USED IN OIL PRODUCTION, Fiabilitate si Durabilitate - Fiability & Durability Supplement
no 1/ 2013, Editura ―Academica Brâncuşi‖ , Târgu Jiu, ISSN 1844 – 640X
13. ***http://blog.kudupump.com, Three Most Common Pcp Failures In A Cbm Well
Posted By Kerri Clarke On Tue, May 06, 2014 @ 02:14 Pm
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78
USING LOGIC PROGRAMMING FOR IMPROVE AND INCREASE
THE RELIABILITY OF TOOLS AND EMBEDDED MACHINE TO
AVOID SOME “MISSION CRITICAL „ IN FLEXIBLE
MANUFACTURING LINES
Lecturer PhD Gheorghe MARC, ―1 Decembrie 1918‖ University of Alba Iulia,
Asist PhD Maria Loredana BOCA, ―1 Decembrie 1918‖ University of Alba Iulia,
Abstract: The management of automation systems, including control system for tools machines can be
done in three ways:
-logical wired
-logic programming
-and mixed, both of them, wired and logical programming
Nowadays, we still use in manufacturing lines logical wired, automation made by using relays and
contactors. In this way the reliability is very low and leads to a high rate of defects and therefore breaks
the functionality of the entire manufacturing process, sometimes with significant losses in productions. This
entire possible problem can lead to “mission critical” situations in the manufacturing lines.
In this paper we try to design some solutions to grow the reliability of flexible manufacturing lines by using
microcontroller, PLC - Programmable Logic Controller and other embedded tools.
Keywords: Embedded, automation, manufacturing lines, mission critical
INTODUCTION
Nowadays, in the manufacturing lines still exist many machines whose command is made
in wired logic, automation being done with relays and contactors. Their low reliability leads
to a high rate of defects and therefore disruptions in operations, sometimes with significant
losses in production [1].
Re-designing of the power switchboards, control and plants automation by using PLC‘s,
microcontrollers, replacing of limitation and sensors with automation tools, usually without
switching tools, leads to a significant increase of working reliability.
In practice the aim is to maximize the effectiveness of equipment and technological lines
by maintenance works, respectively by proper maintenance with repairs at specify time, and
always using spare parts and maintenance materials of a good quality [3],[4].
Depending on the number of operating hours, the planned repairs are classifeid in the
following categories:
technical review (RT)
Current repairs I (RC1)
Current repairs II (RC2)
Total repairs (RK).
The main objectives of maintenance operations are:
Avoiding accidents and accidental disruptions of the production flow
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79
Reducing of production losses through accidental interruption of the technological
equipments
Avoiding wastage as result of disturbance and incorrect adjustments of
measurements
The possibility of estimations cost of repairs and maintenance[6]
As is already known, this type of preventive maintenance is done with certain costs,
which generally depend on the intervention tips, and the age of the machine.
DESCRIPTION OF TOOL MACHINE IN TECHNOLOGICAL FLOW
Aanalyzing of maintenance operations cost related to the repair cycle may cause a
decision to modernize equipments and technological lines, which lead to a more reliability of
the that equipments [7][8].
Driving classic electrical equipment of a tool is the most exposed to accidental falls that
can cause unexpected disruptions to the technological process. This can happened because of
a large number of switching elements, such as contactors, relays, pushbuttons, limit switches,
position sensors on the one hand, and on the other hand, operation conditions of the industrial
environment as dust, high humidity, etc [9],[10].
The aim of this paper is automation of a tool for protective foil of a pallet bagging line in
manufacturing of construction materials.
Figure 1 present a graphical panel of technological flow which shows the execution tool
where we make some interventions.
Fig. 1 - The graphical panel of the technological flow
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80
The next figure (figure 2) shows one part of electrical panel scheme of the manufacturing
tool.
Fig. 2 - Electrical panel scheme of the manufacturing tool
To achieve power and automation scheme we establish the placing bags operation
flowchart of the machine shown in Figure 3, from which we can obtain the wired logic
program with PLC [1],[2].
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81
Analyzing the complexity of operating scheme related to operation hours and the
matching of the tool in the current technological process, we chose to use a programmable
equipment from Moeller Easy PLC 700 series and replacing all position sensors and limit
switch with inductive and optical sensors.
Fig. 3 - The placing bags operation flowchart
Automation part is composing of sensors, PLC and control scheme achieved 719 AB
Easy. RC is a module of Easy700 series. Commander SK Inverter is a product of Emerson-
Control Techniques used to control AC motor. We used inverter to have effective control of
motor speed required in precise settlement of the film on the pallet, clamping system,
handling and fixing film.
This requires a high accuracy due to requirements imposed by the small size less than 1
mm foil and low stiffness.
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82
In this system we used small pneumatic components, filters, dispensers having extended
facilities in technologies of precision mechanics and robotics.
Following the automation of equipment and replacement of power panel we present in
Figure 4 automation and control scheme made using programmable tool PLC Easy719.
Fig.4 - Automation and control scheme made using programmable tool PLC Easy719
CONCLUSIONS
Using wired logic by introducing PLC and variable speed drives, in rehabilitating and
upgrading of control machine and machine tool drives, leading on the one hand to increase the
reliability in operation, on the other hand the performance and increased efficiency.
Following the practical research and implementation of the solution presented, machine has
been running for over a year without any failures to register.
FUTURE WORK
Encouraging results give us the idea to expand our research to the design of modular
and flexible automation systems to obtain complex control and actuation systems with
minimal cost and in a short time.
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83
These systems can be provided including self-diagnosis system for easy interventions
in case of failure, resulting in decreased time stationary and also with counting times of
running for a rigorous tracking of planning maintenance and repairs.
REFERENCES
[1] Allen-Bradlez , RON BLISS.Introducţion to IEC1131-3 Ladder Diagram
[2] Ardelean.I, Petrescu.L, Giuroiu.H, Circuite integrate CMOS, Editura Tehnica,
Bucuresti 1986,
[2] Balut Lucian , Circuite Electronice, Editura SIGMA TRADINGMETAFORA,
Constanta, 1999
[3] Balut Lucian, Componente si Dispozitive Electronic, EdituraLEDA, Constanta , 1997
[4] Festila L, Electronica digitala II , Circuite Logice Secventiale –LITO UTCN, 1994
[5] Haba C.G., Sisteme de comandă a maşinilor electrice, Ed.Gh.Asachi, Iaşi
[6] Hugh Jack. Automating Manufacturing Systems (with PLC,s), Ladder Logic,
Programing, PLC hardware, inputs and outputs, relays, logical sensors, OPTICAL
(Photoelectric) Sensors, pneumatics Components, 2005;
[7] Maghiar Teodor, Mircea Calugareanu, Constantin Stanescu, Karoly Bondor,
Electronica Industriala, Editura UNIVERSITATII DIN ORADEA, Oradea 2001
[8] Pasca S. , Tomescu N, Sztojanov I., Electronica Analogica si digitala (Vol I,II, III )
[9] ***, Comander SK- AC variable speed drive for 3 phase induction motors from 0,25 kw to
7,5 kw,0,33hp to 10 hp. Model sizes A,B,C, and D, 2008
[10] CONTROL TECHNIQUES WWW.controltechniques.com
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84
CONSIDERATIONS IN DETERMINING ANALYTIC GRAPHICS
FUNCTIONAL PARAMETERS OF MARINE PROPULSION ENGINES
Prof. univ. dr. ing. Anastase PRUIU, Academia Navală „Mircea cel Bătrân‖,
Prof. univ. dr. ing. Traian FLOREA, Academia Navală „Mircea cel Bătrân‖,
Instructor principal drd. ing. Daniel MĂRĂȘESCU, Academia Navală „Mircea cel Bătrân‖,
Lect. univ. dr. Adriana SPORIȘ, Academia Navală „Mircea cel Bătrân‖,
Abstract: In this paper the authors, present the main relationships between the functional parameters which
allow a correct interpretation of the functional parameters determined experimentally with their monitoring
programs.
Keywords: functional parameters, monitoring
1. RELATIONSHIP BETWEEN FUNCTIONAL AND GEOMETRICAL
PARAMETERS OF MARINE INTERNAL COMBUSTION ENGINES
Operation of machines and equipment in terms of naval safety is imposed by the
operating manual of the designer and manufacturer on and through compliance with the rules
of classification societies, these rules required by the IMO conventions and codes.
Mechanical engineers from the ship's complement, according to its competences, should
be on every day to determine the functional parameters of the propulsion engine to perform,
to make the necessary adjustments to reduce pollution of the marine environment and
efficient use of energy on the ship.
IMO certificates: Cargo Ship Safety Equipment Certificate; Certificates in compliance
with the International Safety Management Code for the Safe Operation of Ship and for
Pollution Prevention (ISM Code):
a) Document of Compliance (DOC)
b) Safety Management Certificate (SMC);
International Air Pollution Prevention Certificate;
International Energy Efficiency Certificate.
To maintain the validity of the statutory certificates issued by the Society, specified
surveys required conventions are to be conducted and endorsement by the society is to be
obtained.
The actual (effective) power of the engine:
kW60
12
4
2
e in
SD
pP mim
kW60
12
4
2
minen in
SD
pP nmn
rel.(1) Nominal
conditions
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85
kW60
12
4
2
eop in
SD
pPop
miopmn
Operating
conditions
where:
Nominal conditions Operating conditions
The mechanical efficiency of the engine mn mop
The mean indicated pressure
2min
m
kNp
2m
kNmiopp
The speed of rotation nn [rev/min] nop [rev/min]
The number of cycles per second 60
12
nn
60
12
opn
The number of cycles per minute
nn2
opn2
The number of cycles per hour 602
nn 60
2
opn
D [m]- cylinder diameter (bore); S [m] - piston stroke; η- the number of strokes of the piston
or racing in the motor cycle is performed : η = 2 for engines 2 strokes; η = 4 for engine in 4
strokes;
The actual power of the engine can be determined with the relationship:
The effective power of the engine Nominal conditions Operating conditions
kW3600
eih
e
QCP
kW
3600en
ihnen
QCP
(2) kW
3600eop
ihop
eop
QCP
where:
Nominal conditions Operating conditions
The effective efficiency of the engine en eop
The fuel consumption per hour
h
kgfuelhnC
h
kgfuelhopC
kgfuel
kJiQ - The power lower calorific value (LCV);
The air consumption for
combustion per hour Nominal conditions Operating conditions
h
airkg
minaerchac mCC
h
airkg
minaerchnhnacn mCC (3.1
)
h
airkg
minaerchophopacop mCC
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86
The air consumption per hour
for charger Nominal conditions Operating conditions
h
airkg
minaerchhach mCC
h
airkg
minaerchnhnachn mCC (3.2)
h
airkg
minaerchophopachop mCC
where:
Nominal conditions Operating conditions
The excess air coefficient for charger α ch α chn α chop
The excess air coefficient for combustion α c α cn α cop
α- The excess air coefficient; maermin
kgaer
kg cb
-the theoretical amount of air required to burn
one kilogram of fuel;
Results:
The fuel consumption per hour Nominal conditions Operating conditions
h
fuelkg
minaerc
ach
m
CC
h
fuelkg
minaercn
acnhn
m
CC
(4)
h
fuelkg
minaercop
acop
hopm
CC
The relationship (2) becomes:
The effective power of the engine
kW3600
min
ei
aerc
ace
Q
m
CP
kW3600
min
eni
aercn
acnen
Q
m
CP
(5) Nominal
conditions
kW3600
min
eopi
aercop
acop
eop
Q
m
CP
Operating
conditions
or:
The air consumption per hour for combustion
h
airkg3600min
ei
aerc
eacQ
mPC
h
airkg3600min
eni
aercn
enacnQ
mPC
(6) Nominal
conditions
h
airkg3600min
eopi
aercop
eopacopQ
mPC
Operating
conditions
The mean indicated pressure
S
aerc
iiVmi
m
Qp
min
2m
kN
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Sn
aercn
iinVn
m
Qp
min
min
2m
kN
(7) Nominal
conditions
Sop
aercop
iiopVopmiop
m
Qp
min
2m
kN
Operating
conditions
where:
ηV - the coefficient of filling of the cylinder with air; ηi - the indicated efficiency; S
kgaer
m3
-
the air density for supercharger;
The compression of supercharging air is done after a trial polytrophic with exponent
polytrophic nc.
Either (po; To) the environmental parameters that determine air density.
Nominal conditions Operating conditions
3m
airkg
o
oo
TR
p
3m
airkg
n
nn
TR
p
(8)
3m
airkg
op
op
opTR
p
where:
2m
kNop - the ambient air pressure; R
kJ
kg K
- the constant air; To K - the ambient air
temperature.
Either (ps ; Ts) the air compressor parameters.
The air supercharger density: Nominal conditions Operating conditions
3m
airkg
s
ss
TR
p
3m
airkg
sn
snsn
TR
p (9)
3m
airkg
sop
sop
sopTR
p
Results:
p po on
s snc c v v (10) or p po
on
s
snc c
(11) and cn
o
sos
p
p1
(12)
Taking into account the relationship (12), relationship (7) becomes:
The mean indicated pressure
cn
o
so
aerc
iiVmi
p
p
m
Qp
1
min
2m
kN
cn
n
snn
aercn
iinVn
p
p
m
Qp
1
min
min
2m
kN
(13) Nominal
conditions
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88
cn
op
sop
op
aercop
iiopVopmiop
p
p
m
Qp
1
min
2m
kN
Operating
conditions
By entering the relationship (13) in the relationship (1) is obtained:
The effective power
kW60
12
4
2
1
min
e in
SD
p
p
m
QP
cn
o
so
aerc
iiVm
kW60
12
4
2
1
min
en in
SD
p
p
m
QP n
n
n
snn
aercn
iinVnmn
c
(14) Nominal
conditions
kW60
12
4
2
1
min
eop in
SD
p
p
m
QP
opn
op
sop
op
aercop
iiopVopmop
c
Operating
conditions
2. SHIP PROPULSION POWERS [6]
For propulsion, the effective power of main engine is transmitted through an axial line
shaft and Stern propeller at hull of ship, at the movement speed Vs.
PeME –the effective power for main engine; PD –the power delivered to propeller; PT –
The thrust power; Ptow –the towing power;
PeME sh = PD; sh - the shaft efficiency
PD PR = PT; PR - the propeller and propulsive efficiency
PT H =Ptow;H - the hull efficiency
PeME HPRSH = Ptow
3. REFERENCE AMBIENT CONDITIONS
Functional parameters defined in certain circumstances prevail with the effective
nominal power at nominal speed nominal parameters are functional. It uses index \"n\".
REFERENCE CONDITIONS
1 2 3 4 5 6 7 8 9
Ambient air temperature (0C) 45 25 25 10 15.6 20 25 15 15
Ambient air pressure (bar) 1 1 1 1 1.01325 1.01325 1.01325 1.01325 1.01325
Sea water temperature (0C) 32 25 25 10 - - - - -
Relative humidity (%) 60 60 30 60 - - - 0 -
1 - IACS M28 (1978); Tropical conditions at sea level; 2 - ISO 3046-1-2002; 3 - ISO 3046-
1-2002(E); ISO 15550- 2002E; 4 - Winter ambient reference conditions; 5 - STP - Standard
Temperature and Pressure (USA); 6 - NTP- Normal Temperature and Pressure; 7 - SATP –
Standard Ambient Temperature and pressure; 8 - ISA- International standard Atmosphere; 9 -
ICAO-Standard Atmosphere International Civil Aviation Organization
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89
For 1;2;3;4; on use the fuel with a power lower calorific value (LCV) equal to 42,70
kJ/kg. For specific fuel consumption values refer to brake power.
For propulsion engines, by contract, determine the functional parameters from the
manufacturer (manufacturer) or in the shipyard where the engine compartment mounting
follow the cars with the participation and under the supervision of designer companies for
classification of IACS (International Association of Classification Societies).
Ambient environmental conditions will be those of the inspections, and fuel-diesel fuel
supplied from analyses elementary and lower calorific corresponding rules for fabrication of
refineries.
Follows, according to the contract, the conditions for recalculation of the functional
parameters of reference.
The functional operating parameters are functional parameters other than nominal ones.
It uses the index: \"exp\" or \"op\".
Functional parameters defined in cylinder engine are called functional parameters
specify. (subscript\"i\"). Define the functional parameters of the coupling flanges of the motor
with an axial line are called actual functional parameters (index \"e\")
4. PERFORMANCE CHARACTERISTICS OF THE ENGINE
Performance characteristics of the MAN B&W L60MC-
C8engine. Performance curves without VIT [7]
Performance characteristics of the MAN B&W
L60MC-C8 engine. Performance curves with VIT [7]
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90
5. CONCLUSIONS
1. The relationship (14) in order to determine the engine power allows to analyses the
influence of bands such as: quality of supercharger air route: The pipe of supercharger air
quality, quality of processes in engine cylinder, fuel quality, Elementary analysis of fuel, air-
fuel mixture, environmental parameters, turbocharger air pressure, compression ratio, load
indicator and use marine heavy fuel oil economy.
REFERENCES
[1] - Anastase PRUIU - Instalaţii energetice navale, Editura Muntenia, Constanţa, 2000
[2] - Alexandru DRAGALINA - Motoare cu ardere internă. Vol I şi II, Ed. Academia
Navală, 2003
[3] - Gh. DUMITRU – Motoare cu ardere interna, Universitatea din Galati
[4] - Nicolae BERECHET – Teza de doctorat, Academia Tehnică Militară 2007
[5] - Anastase PRUIU – MAI- Procese, caracteristici si supraalimentare, Universitatea
Maritima Constanta
[6] -Basic Principles of Ship Propulsion MAN diesel & Turbo
[7] -MAN B&W L60MC-C8 Project Guide
[8] - Marine Engine IMO Tier II Programme 2013
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91
ABOUT ENGINE ROOM VENTILATION ON MERCHANT VESSELS
Prof. univ. dr. ing. Anastase PRUIU, Academia Navală „Mircea cel Bătrân‖,
Prof. univ. dr. ing. Traian FLOREA, Academia Navală „Mircea cel Bătrân‖,
Instructor principal drd. ing. Daniel MĂRĂȘESCU, Academia Navală „Mircea cel
Bătrân‖, [email protected]
Lect. univ. dr. Adriana SPORIȘ, Academia Navală „Mircea cel Bătrân‖,
Abstract: Engine room ventilation must ensure the quality and quantity of air for breathing, as well as the
amount of air necessary machines and thermal installations and for heat flow transmitted through the warm
surfaces of machines and naval installations. Through the assumptions and calculations, the authors allow those
interested in a quick and correct interpretation of the flow and temperature for supercharger of marine diesel
engines in all navigation conditions.
Keywords: engine room, ventilations
1. ATMOSPHERE OF EARTH
The earth's atmosphere has a mass of about 4,9 · 10e18 kg and the population
7 · 10e9 persons, so that each person has the a mass of air per person 7 · 10e8 kg/person.
Air composition Table 1
Nitrogen (N2) 78,0842% Helium (He) 0,000524%
Oxygen (O2) 20,9463% Methane (CH4) 0,0001745%
Argon (Ar) 0,93422% Krypton (Kr) 0,000114%
Carbon dioxide (CO2) 0,03811% Hydrogen (H) 0,000055%
Water vapor ≈ 1% Neon (Ne) 0,001818%
Air requirement and production CO2 Table 2
Consumer Power mc/day kg/day Kg CO2/day
MAN (0,1-0,5) kW/man 15 18 0,8
The population
of earth 2450000000 1.05E+11 1.26E+11 5600000000
Marine diesel
4T i=1-28V
(50-3000)
kW/cil 17 200 000 20 640 000 1 362 240
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92
Marine diesel
2T i=1-14L
(200-7000)
kW/cil 20 000 000 24 000 000 1 584 000
Marine boilers
i=1-12
(200-50000)
kW/unit 24 000 000 28 800 000 5 184 000
Marine steam
turbines
i=1-4
(1000-70000)
kW/unit 28 500 000 34 200 000 6 155 000
Marine gas
turbines
i=1-6
(1000-80000)
kW/unit 195 000 000 234 000 000 10 530 000
Table 3
Ambient air
temperature
(0C)
Relative
humidity
(%)
Pressure of
scavenge air
(bar)
Temperat
ure after
the
scavenge
air (0C)
Water
content
(kgwater/
kg dry air)
Water
content
(kgwater/
kg dry
moist)
The flow of
water from the
humid air motor
consumption
Kg water/h
10 60% 3.5 16 0.009 0.00892 8920
25 40% 3.5 30 0.008 0.007937 7937
30 60% 3.5 40 0.015 0.014778 14778
35 60% 3.5 50 0.022 0.021526 21526
45 60% 3.5 59 0.035 0.033816 33816
Numerical application are made to environmental parameters in reference conditions,
engineers task is to make adjustments for ambient conditions in operations conditions.
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93
The cooling occurs condensation of water vapor in the air, maximum water production is
reflected in the table above. It is necessary to periodically purging of air coolers (1-4 times on
watch = 4 hours), therefore is necessary automatic purging.
Health effects from lack of oxygen
Table 4
Health effects from lack oxygen
O2 level Effects
22% Oxygen enriched atmosphere
20.8% Normal level – Safe for Entry (±0.2%)
19.5% Oxygen deficient atmosphere
16% Impaired judgment and breathing
14% Rapid fatigue and faulty judgment
11% Difficult breathing and death in a few minutes
Low pressure fan p =60-100 mmcw; p =0.588- 0.98 kN/ m2
Table 5
Marine
Equipment Power Kg/day mc/day
Flow of fan
Ventilation
kg/day
Flow of fan
Ventilation
mc/day
Marine
diesel 4T
i=1-28V
(50-3000)
kW/cil 20640000 17200000
30960000
41280000
25 800 000
34 400 000
Marine
diesel 2T
i=1-14L
(200-7000)
kW/cil 24000000 20000000
36000000
48000000
30 000 000
40 000 000
Marine
boilers
i=1-12
(200-50000)
kW/unit 28800000 24000000
42000000
56000000
36 000 000
48 000 000
Marine
steam
turbines
i=1-4
(1000-70000)
kW/unit 34200000 28500000
51300000
64400000
42 750 000
57 000 000
Marine gas
turbines
i=1-6
(1000-80000)
kW/unit 234000000 195000000
351000000
468000000
292 500 000
390 000 000
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Table 6
Marine
Equipment Power
Flow of
fan m3/s
Power el.motor
of fan kW
f =0.8; p =60
mmcw
p =0.588 kN/
m2
Power el.motor of
fan kW
f =0.8; p =100
mmcw
p =0.980 kN/ m2
Number
of fan
Marine diesel
4T i=1-28V
(50-3000)
kW/cil
298.6111
398.1481
216.4931
288.6574
365.7986
487.7315
6 – 8
Marine diesel
2T i=1-14L
(200-7000)
kW/cil
347.2222
462.963
251.7361
335.6481
425.3472
567.1296
6 – 8
Marine
boilers
i=1-12
(200-50000)
kW/unit
416.6667
555.5556
302.0833
402.7778
510.4167
680.5556
8 – 10
Marine
steam
turbines
i=1-4
(1000-70000)
kW/unit
494.7917
659.7222
358.724
478.2986
606.1198
808.1597
8 – 10
Marine gas
turbines
i=1-6
(1000-80000)
kW/unit
3385.417
4513.889
2454.427
3272.569
4147.135
5529.514
12 – 16
Where:
Power shaft of fan f
p
antF
FP
[kW]; (1)
Massic flow of fan
s
KgairCF ach)2..5.1(1 (2)
Flow of fan
s
mFF
air
3
1
(3)
Flow air of thermal machinery
s
Kgairm
CC airch
hf
ach min3600
(4)
The excess air coefficient for charger - αch; the theoretical amount of air required to burn one
kilogram of fuel -
f
airmkg
kg air
min; Efficiency of fan f = 0.7-0.85; Air density –
3m
kgair ; Fuel consumption of thermal machinery -
h
kgC
f
hf ; Pressure fan
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95
p =0.588- 0.98 [kN/ m2];
Engine room temperature TER and difference ΔT
The engine room temperature TER and the engine room/ambient air temperature
difference ΔT are shown as functions of the ambient air temperature Tamb [1]
ISOSMCRscsc pp /. Bypass opens when scp exceeds offsetsomeISOSMCRscp /.
ISOscsc pp . Bypass opens when scp exceeds offsetsomeISOscp . [1]
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Reference ambient conditions
Tabel 7
1 2 3 4
Ambient air temperature (0C) 45 25 25 10
Ambient air pressure (bar) 1 1 1 1
Sea water temperature (0C) 32 25 25 10
Relative humidity (%) 60 60 30 60
1 - IACS M28 (1978); Tropical conditions at sea level; 2 - ISO 3046-1-2002;
3 - ISO 3046-1-2002(E); ISO 15550- 2002E; 4 - Winter ambient reference conditions;
BIBLIOGRAPHY
[1] - Influence of Ambient Temperature Conditions on Main Engine Operation
of MAN B&W Two-stroke Engines
[2] - Caterpillar Marine Engines Application and Installation Guide
[3] - Engine Selection Guide Two-stroke MC/MC-C Engines
[4] - Marine and Machinery Systems and Equipment OCTOBER 2013
[5] - Wartsila Engines - Project Guide
[6] - INTERNATIONAL ASSOCIATION OF CLASSIFICATION SOCIETIES –
Requirements concerning MACHINERY INSTALLATIONS
[7] - MAN B&W L60MC-C8 Project Guide
[8] - Marine Engine IMO Tier II Programme 2013
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97
MATHEMATICAL MODEL FOR DETERMINING KINEMATIC
PARAMETERS OF THE CARDAN JOINT MECHANISM WITH
TECHNICAL (GEOMETRICAL) DEVIATIONS
Ion BULAC
Doctor, University of Pitești, email: [email protected]
Abstract: The cardan joint mechanism is derived from the 4R spherical quqdrilateral mechanism
and a particular case of spatial quadrilateral mechanism RCCC where by C, R was noted the
cylindrical kinematic pair respectively the rotation kinematic pair. In this paper are deducted the
calculation relations , is established the mathematical model for determining the the kinematic
parameters of the cardan joint mechanism with technical (geometrical) deviations.
Keywords: cardan joint, kinematic pair, quadrilateral mechanism, cardan transmission .
1. INTRODUCTION
The technical (geometrical) deviations lead to the changine of kinematic parameters
of the cardan joint mechanism. This deviations is established in paper [3].
For determining the influence of both angular and axis deviations [1]., over the
kinematic parameters of the cardan joint mechanism, it is necessary to consider the cardan
joint, not as a spherical quadrilateral but as a particular case of RCCC mechanism. where by
C, R was noted the cylindrical kinematic pair respectively the rotation kinematic pair.
In this paper are deducted the calculation relations , is established the mathematical
model for determining the kinematic parameters of the cardan joint mechanism with technical
(geometrical) deviations.
2. THE POSITIONAL ANALYSIS OF THE RCCC MECHANISM
The RCCC mechanism (see Figure 1) is made of four elements noted with 1, 2, 3 and
4, the forth element (the base) being fixed and the elements being connected through the
kinematic pairs 321 ,, OOO , and 4O , the 1O being the rotation kinematic pair and 32 ,OO ,and
4O being the cylindrical kinematic pairs.
The axes of the kinematic pairs are noted with ,...2,1, izO ii and the following
perpendiculars are noted with 4,3,2,1,1 iOO ii ,point 5O being identical with point 1O .
One notates with i , i , 4,3,2,1i the length of the axes and the angle between them.
So it is chosen a local reference system iiii zyxO , 4,3,2,1i so that the axes ii xO to be
situated on the shared perpendicular of the axes ii zO , 11 ii zO . It is noted with is the
distances iiOO and with i the angle between the axes 11 ii xO , ii xO , 4,3,2,1i .
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98
Fig. 1. RCCC Spatial Mechanism
In these conditions, the geometrical parameters 4,3,2,1,,, is iii being known, the
positional analysis for determining 432432 ,,,,, sss is based on the angle 1 .
From the equation of rotations closing, using the diagram ‖„ [7] and the order
3,4,1 and 2 is obtained the following equation:
0)()()( 13413413 CcBsA (1)
where :
2143114313
4114313
11313
)(
()(
)(
ccccscscC
cssccsB
sssA
( 2)
The trigonometrically functions cos, sin being noted with c, s. Through the
conventional derivate D of the relations (1), (2) having as basis the relations [7].
iiiiii cssDsscD )(;)( ( 3)
csDscD iiiii )(;)( ( 4)
is obtained the equation:
0433323131343 KHGFsFsD ( 5)
where :
The angle 4 is determined by solving the equation (1) and through the equation (5) is
known the parameter 4s .
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99
With circular permutations the relations follows:
0)()()( 42342342 CcBsA ( 6)
0)()()( 31231231 CcBsA ( 7)
from where are determined, in order, the angles 3 and 2 and also the equations:
0322212424232 KHGFsEsD ( 8)
0211141313121 KHGFsEsD (9)
from which are determined the parameters 23, ss .
The expression of the coefficients iiiiiiiii KHGFEDCBA ,,,,,,,, , i=3,2,1 ,are given
in TABLE 1 from the paper [2].
In the initial position , 00 i the expressions are obtained
2413341333 )(),(,0 cccCssBA (10)
and it results that:
)(
)(
413
241304
ss
cccc (11)
3. THE TECHNICAL (GEOMETRICAL) DEVIATIONS OF CARDAN JOINT
The cardanic joint enables the transmission of the rotation movement from the shaft 3
through the cardanic cross 2.
The cardanic cross is tied to the brackets of the shafts 1 and 2 through the cinematic
rotation couples A , A and also B , B .
Fig. 2. Cardan joint mechanism
In the papers [1], [3] is established the technical (geometrical) deviations of cardan
joint mechanism.
A kinematic diagram that represents a mechanism with one cardan joint, with all
geometrical deviations possible [1], [3]., is presented in Figure. 3.
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100
Fig. 3. Geometrical deviations.
These deviations are small and fulfill the condition:
iiii
ii
OOiOO
i
441
4
,2,1,
,3,2,1,2
(12)
The angularly deviation of the main shaft bracket is defined by the parameter 1 and
the smoothness deviations for the same bracket is given by the parameter 1 .
The angularly deviation of the cardanic cross 2 is given by the parameter 2 and also
the deviation from smoothness is given by the parameter 2 .
The angularly deviation of the driven shaft bracket 3 is given by the parameter 3
and the smoothness deviation is given by the parameter 3 .
The angularly deviation of the driven shaft 3 depending on the driving shaft 1 is given
by the parameter 4 .
As shown in the papers [1], [3] in default of shafts 1 and 3 are known the points
43322114 ,,,,,,, OOOOOOOO are overlaid with point O (see Figure. 3.) and the kinematic
cylindrical couples A , B and D (see Figure. 1.) become rotation kinematic couples (there are
no displacements 432 ,, sss along the axes 432 ,, OzOzOz .
The existence of technical deviations conducts to the displacements 4,3,2,1, isi and.
In order to determine these displacements it is first necessary to calculate the angularly
parameters 432 ,, variation depending on the angle 1 .
4. THE DETERMINING PARAMETERS 432 ,,
The angularly parameters 432 ,, is derermined from the system of equations
.3,2,1,0111 iCcBsA iiii (13)
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101
To this purpose, one uses the Newton method [10], [11]. and with the notations
.,
4
3
2
4
3
2
(14)
.3,2,1,11 iCcBsA iiiiii (15)
.
3
2
1
(16)
.23211
33211
3311
ssscC
sscsB
cssA
(17)
.44322
44322
4422
ssscC
sscsB
cssA
(18)
4343
232323232
121212121
00
0
0
sBcA
CcBsAsBcA
CcBsAsBcA
J (19)
is obtained the matric equation
1
J (20)
from which results the variation { } for the known values of angles 4321 ,,, .
After the determining the angularly parameters 432 ,, variation depending on the angle 1
.is determined the parameters 432 ,, sss with the relations
)(1
43332313133
4 KHGFsED
s (21)
)(1
32221242422
3 KHGFsED
s (22)
)(1
21114131311
2 KHGFsED
s (23)
where the coefficients .3,2,1,,,,, iKHGFE iiiii are calculated from the TABLE 1. from
the paper [2].
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102
5. CONCLUSIONS
The mathematical model presented in this paper, makes possible the study of technological
deviations influence over the kinematic parameters of the cardan joint mechanism.
Using this mathematical model, made possible the elaboration an calculation algorithm that
by numerical simulation can highlight the influence of different technical deviations that
appear in the mechanism elements.
REFERENCES
1. BULAC, I,. Contributions to the study of technical deviations over the dynamic response of
policardan transmissions, Doctoral Thesis, University of Piteşti, 2014.
2. BULAC, I,. Mathematical model for determining kinematic parameters of the spatial quadrilateral
mechanism RCCC (Submitted for publication), SISOM 2014, Bucharest, May 22-23, 2014.
3. BULAC, I,. The technical (geometrical) deviations of cardan joint mechanism (Submitted for
publication), Annals of the Oradea University, 2014.
4. DUDIŢĂ, FL., Cardan shafting, Technical Publishing House, Bucharest, 1966.
5. DUDIŢĂ, FL., FL., DIACONESCU, D., BOHN, CR., NEAGOE, M., SĂULESCU, R., Cardan
shafting, Transilvania Expres Publishing House, Brașov, 2003 .
6. DUMITRU, N., NANU, GH., VINTILĂ, DANIELA, Mechanisms and mechanic shafting, Didactic
and Pedagogical PublishingHouse, Bucharest, 2008.
7. PANDREA, N., Solid mechanics plucheriane coordinates, Romanian Academy Publishing House,
Bucharest, 2000.
8. PANDREA, N., POPA, D., Mechanism, Technical Publishing House, Bucharest, 2000.
9. RIPIANU, A., CRĂCIUN, I., Mechanism, Technical Publishing House, Bucharest, 2000.
10.STĂNESCU, D., PANDREA, N.,, Numerical methods, Didactic and Pedagocical Publishing
House, Bucharest, 2007.
11. TEODORESCU, P., STANESCU, D,. PANDREA, N., Numerical analysis with applications in
Mechanics and Engineering, Wiley, 2013.
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THE NUMERICAL STUDY OF THE INFLUENCE OF TECHNICAL
(GEOMETRICAL) DEVIATIONS OVER THE KINEMATIC
PARAMETERS OF THE CARDAN JOINT MECHANISM
Ion BULAC
Doctor, University of Pitești, email: [email protected]
Abstract: The cardan joint mechanism is derived from the 4R spherical quqdrilateral mechanism
and a particular case of spatial quadrilateral mechanism RCCC where by C, R was noted the
cylindrical kinematic pair respectively the rotation kinematic pair. In the present paper are
established the connection relations between the technical (geometrical) deviationsl and of the
kinematic parameters of this mechanism .The results of the numerical solving of this problem will
be presented under the form of a diagram and will be commented.
Keywords: cardan joint, kinematic pair, quadrilateral mechanism, technical deviations .
1. INTRODUCTION
For determining the influence of both angular and axis deviations, over the kinematic
parameters of the cardan joint mechanism, it is necessary to consider the cardan joint, not as a
spherical quadrilateral but as a particular case of RCCC mechanism where by C, R was noted
the cylindrical kinematic pair respectively the rotation kinematic pair
In the previous papers [1], [2], [3]., there was elaborated a mathematical model and the
calculation algorithm for the kinematic parameters of the cardan joint mechanism with
technical (geomeyrical) deviations.
In the present paper are established the connection relations between the technical
(geometrical) deviationsl and of the kinematic parameters of this mechanism.
2. THEORETICAL ASPECTS
The RCCC mechanism (see Figure 1) is made of four elements noted with 1, 2, 3 and 4, the
forth element (the base) being fixed and the elements being connected through the kinematic
pairs 321 ,, OOO , and 4O , the 1O being the rotation kinematic pair and 32 ,OO ,and 4O being
the cylindrical kinematic pairs.
From the equation of rotations closing, using the diagram ‖„ [7] and the order
3,4,1 and 2 is obtained the following equation:
0)()()( 13413413 CcBsA (1)
and with circular permutations the relations follows:
0)()()( 42342342 CcBsA ( 2)
0)()()( 31231231 CcBsA ( 3)
the trigonometrically functions cos, sin being noted with c, s.
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Fig. 1. RCCC Spatial Mechanism
Through the conventional derivate D of the relations (1),(2),(3) and of coefficients
3,2,1.,,, iCBA iii having as basis the relations [7].
iiiiii cssDsscD )(;)( ( 4)
csDscD iiiii )(;)( ( 5)
is obtained the equation:
0433323131343 KHGFsFsD ( 6)
0322212424232 KHGFsEsD ( 7)
0211141313121 KHGFsEsD (8)
The angle 4 is determined by solving the equation (1) and in order, the angles 3 and
2 by solving the equations (2),(3).
From ecuation (6) is determined the parameter 4s and also the equations (7), (8) is
determined the parameters 23, ss .
The expression of the coefficients iiiiiiiii KHGFEDCBA ,,,,,,,, , i=3,2,1 ,are given
in TABLE 1 from the paper [1].
In the paper [2], is established the technical (geometrical) deviations of cardan joint
mechanism.
A kinematic diagram that represents a mechanism with one cardan joint, with all
geometrical deviations possible [2]., is presented in Figure. 2
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Fig. 2. Geometrical deviations.
These deviations are small and fulfill the condition:
iiii
ii
OOiOO
i
441
4
,2,1,
,3,2,1,2
(9)
The angularly deviation of the main shaft bracket is defined by the parameter 1 and
the smoothness deviations for the same bracket is given by the parameter 1 .
The angularly deviation of the cardanic cross 2 is given by the parameter 2 and also
the deviation from smoothness is given by the parameter 2 .
The angularly deviation of the driven shaft bracket 3 is given by the parameter 3
and the smoothness deviation is given by the parameter 3 .
The angularly deviation of the driven shaft 3 depending on the driving shaft 1 is given
by the parameter 4 .
3. NUMERICAL APLICATION
One considers a cardanic joint (see Figure 3) for which:
.4,3,2,1,0,0,0,001,0,0 1312 israd i (10)
Fig. 3. The cardan joint mechanism
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On the basis of a calculation program realized in Excel with the mathematical model
presentea in the paper [4], and the algorithm presented in the paper [3], where obtained, in
the case where 0 , for the parameters 432 ,, the results from diagram from Figure. 4.,
Figure. 5., and Figure. 6.
Fig. 4.The variation of rotation angle θ3 Fig.5.The variation of rotation angle θ4
Fig. 6. The variation of rotation angle θ2
For a cardanic joint for which:
4,3,2,1,0,001,0,001,0,0 1 israd ii (11)
The variation graphs are presented in the Figures 7,8,9,10,11,12
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Fig. 7.The variation of rotation angle θ4 Fig.8.The variation of rotation angle θ3
Fig. 9. The variation of rotation angle θ2 Fig. 10. The variation of displacement s4
Fig. 11. The variation of displacement s3 Fig. 12. The variation of displacement s2
For a cardanic joint for which:
4,3,2,1,001,0,001,0,001,0,0 1 israd ii (12)
The variation graphs are presented in the Figures 13,14,15,16,17,18
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Fig. 13. The variation of rotation angle θ4 Fig. 14. The variation of rotation angle θ3
Fig. 15. The variation of rotation angle θ2 Fig. 16. The variation of displacement s4
Fig. 17. The variation of displacement s3 Fig. 18. The variation of displacement s2
4. CONCLUSIONS
For the normal cardan join with technical deviations with 0 and radi 001,0 ,
when 1 covers the interval 3600
the angle 4 varies between 45090 ;
the angle 3 varies between 27088,269 ;
the angle 2 varies between 06,9090 .
The influence of i and 1s deviations over the angles 234 ;; are insignificant in value.
The variation of angles i i=1,2,3 does no influence the displacements is , i=2,3,4.
The displacements is , i=2,3,4. are influenced only by the value of the i and 1s
parameters.
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For 0 , the variation curves form of the kinematic parameters are alike.
REFERENCES 1. BULAC, I,. Mathematical model for determining kinematic parameters of the spatial quadrilateral
mechanism RCCC (Submitted for publication), SISOM 2014, Bucharest, May 22-23, 2014.
2. BULAC, I,. The technical (geometrical) deviations of cardan joint mechanism (Submitted for
publication), Annals of the Oradea University, 2014.
3. BULAC, I,. Calculation algorithm for determining kinematic parameters of the cardan joint
mechanism with technical (geometrical) deviations (Submitted for publication),
Annalsof the Oradea University, 2014.
4. BULAC, I,. Calculation algorithm for determining kinematic parameters of the cardan joint
mechanism with technical (geometrical) deviations (Submitted for publication),7tth
,Durability and Reliability of Mechanical Systems``,Târgu-Jiu, Romania, 23-24 May, 2014.
5. DUDIŢĂ, FL., Cardan shafting, Technical Publishing House, Bucharest, 1966.
6. DUDIŢĂ, FL., FL., DIACONESCU, D., BOHN, CR., NEAGOE, M., SĂULESCU, R., Cardan
shafting, Transilvania Expres Publishing House, Brașov, 2003 .
7. PANDREA, N., Solid mechanics plucheriane coordinates, Romanian Academy Publishing House,
Bucharest, 2000.
8. PANDREA, N., POPA, D., Mechanism, Technical Publishing House, Bucharest, 2000.
9. STĂNESCU, D., PANDREA, N.,, Numerical methods, Didactic and Pedagocical Publishing
House, Bucharest, 2007.
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110
CORRELATING 2K-52MU CUTTING AND LOADING MACHINE
WITH TR-5 SCRAPER CONVEYER
PhD, Eng., Consulting Teaching Staff, Răzvan Bogdan ITU, Department of Industrial
Mechanical Engineering and Transport, University of Petrosani, [email protected]
PhD, Associate Prof. Eng., Iosif DUMITRESCU, Department of Industrial Mechanical
Engineering and Transport, University of Petroşani, [email protected]
PhD, Lecturer, Eng., Vilhelm ITU, Department of Industrial Mechanical Engineering and
Transport, University of Petroşani, [email protected]
Abstract: The necessity of mechanization of coal extraction in Jiu Valley mines, in the conditions
of the present economic crisis, involved the adaptation of the existing equipments to the new
conditions of reequipping of certain faces. Thus, within the program of reequipping of a longwall
in Lonea Mining Plant, the adaptation of 2K-52MU cutting and loading machine to TR-5 scraper
conveyer was required. The main problem of adaptation of the two equipments was in the design
and development of systems for affixing the ends of the feeding gear chain of the machine to the
driving and returning stations of the TR-5 scraper conveyer. In solving this problem, the focus was
on ensuring for all the elements of the attaching system of the ends of the machine chain to resist
to the machine’s maximum haulage force of 250 kN, and this strain not to be transmitted to the
metal structure of the stations and be taken over by the hydraulic prop of anchorage of the
conveyer station.
Keywords: correlating, cutting and loading machine, scraper conveyer
INTRODUCTION
To adapt the existing equipments in view of reequipping the faces, one should be deeply
familiar with the structure and technical characteristics of the equipments that are used and of
the way they are correlated with the mining method, the geological-mining conditions specific
to the layer exploited, and with observing the occupational health and safety norms.
By the implementation of a longwall reequipping program in Lonea Mining Plant in the
fourth trimester 2013, the classical method of extraction with a productivity of 6,8 ton/job was
abandoned in favor of longwall extraction method with individual support and cut with a
machine with an estimated productivity of 12 ton/job. A technical documentation was
required to be drawn up in this sense, regarding the adaptation of the affixing program for
the2K-52MU machine to TR-5 scraper conveyer stations. In order to see the correlation of the
equipments, an analysis of the framework extraction method was made for longwalls with
cutting and loading machines. Fig. 1 shows the working stages for a maximum 3,2 m high
longwall and 1,8 m high cut with the machine, as it follows: I – machine in the bay; II –
cutting the first strip; II – manual fixing of the place for mounting the articulated beam; IV –
machine advance in the bay and mounting of the fourth prop; V – cutting the second strip; VI
– manual cleaning up of the face and machine advance in the bay; VII – moving the back prop
under the first beam; VIII – ripping of the back prop and beam.
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From the above, it results that an analysis of economic efficiency should be made,
regarding the correlation of the longwall height with the cutting height of the machine, with
the geological mining conditions and the occupational health and safety norms. The price of
the 2K-52MU machine, recovered from cassation should be considered, scrap iron – 2500
Euro, rehabilitated and put to operate with maximum 5000 Euro.
Fig. 1. Longwall extraction method with
individual support and machine cutting
The technical characteristics of the 2K-52MU machine were not correlated with those of
the TR-5 scraper conveyer, especially considering that the latter had not been designed for
faces, and they had been manufactured by different companies in different countries. The two
equipments are nevertheless compatible, at least from the following points of view:
- More than half of the theoretical cutting capacity of the machine, which is not achieved
in practice due to the correlation of the advance speed with the geological-mining conditions,
can be handled by the scraper conveyer;
- Size-wise, the machine can be mounted on the conveyer by adopting suitable
modifications, adapting TR-5 stations to chutes, TR-6 with the use of TR-7 laterals, and
modification of machine shoes without diminishing the characteristics of their resistance;
- The conveyer‘s robust design supports the approx. 12 …14 ton mass of the machine;
The design of the scraper conveyer allows coal to be loaded in good conditions by the
auger drums.
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The main lack of correlation between the two equipments consists in the fact that the
actuating and return stations for the TR-5 conveyer are not foreseen with attaching
hangers/plates of the affixing device of the machine haulage chain end.
AFFIXING SYSTEM TO THE ACTUATING STATION
Fig. 2. Movement of the affixing system on
he actuating station [3]
Fig. 3. Design solution for the affixing system
of the chain end to the TR-5 actuating station[3]
Fig. 2 shows the design solution for the positioning of the Fig. 3. Design solution for the
affixing system of the chain end to the TR-5 actuating station[3] attachment system of the end of
the chain calibrated with 26x92 links of the 2K-52MU machine advance mechanism,
reference point 2, in the metal construction of the actuating station, reference point 1.
The design solution of the affixing system is shown in Fig. 3, which is made up of 1 –
hanger fixed on the station; 2 – lateral connecting plate; 3 – lateral blocking plate; 4 –
blocking bolt Φ50; 5 – blocking bolt Φ60; 6 – articulation bolt Φ60; 7 – device hanger; 8 –
haulage rod; 9 – wear ring; 10 – wear ring support; 11 – chain fixing strap; 12 – centering pin;
13 – chain calibrate with 26x92 links; 14 – M20x100 screw; 15 – M10 screw for greasing; 16
– distance ring; 17 – M42 low washer; 18 – M42 washer; 19 – M24x100 screw.
The affixing system for the chain end to the TR-5 actuating station shows the following
design improvements:
- the hanger fixed to the station, instead of the lifting hanger, leans on the framework of
the station by two distanced shoes and has its own support for the SVJ station anchoring
hydraulic prop, which improves stability of hanger and the way forces are transmitted to the
station;
- overlapping the prop supports avoids the error possibility in placing the anchoring prop
and allows interchangeability of the actuating station;
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- parallel positioning of the lateral linking plate, reference point 2 (Fig. 3), and rigid
fixing on the hanger through the three bolts Φ50, reference point 4, and Φ60, reference point
5, made a movement outward the chain axis by 120 mm, which improved the movement of
the machine on the conveyer in the area of the actuation station;
- the distance between the wings of the device hanger, reference point 7, by inside
welding of the of two 20 mm thick attachments plates, which improved the strain on the
articulation bolt, reference point 6;
- axial rolling contact bearing with balls 51112 was replaced with a wear ring of cast
iron or bronze, reference point 9, its part being to take over the twist of the chain, and a screw
was provided, reference point 15, for greasing the contact area between the wear ring and the
ring support, reference point 10;
- transversal pins were provided, reference point 12, to center the two bridles in view of
improving the haulage force transmission between the haulage rod, reference point 8, and the
chain link, reference point 13;
- only 20 mm and 60 mm thick sheets were used, which were in stock in Lonea Mining
Plant;
Fig. 4. Calculation model for the connection system
at the actuation station[3]
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Based on the design solution in Fig. 3, the calculation model was drawn up, with constructive
dimensions in view of dimensional verification of its elements given in Fig. 4, where: 1 –
partition of actuation station; 2 – hanger fixed to the station; 3 – device hanger; 4 –
articulation bolt Φ60x270; 5 – distance ring; 6 – wear ring; 8 – haulage rod Φ57x200; 9 –
bridle; 10 - M20x100 screw; 11 – centering pin Φ20x45; 12 - M24x100 screw; 13 – lateral
connecting plate; 14 – blocking bolt Φ60; 15 – blocking bolt Φ50.
Figure 5. Variation of safety coefficients
of connection system to the anchoring station[3]
Based on the calculation model in Fig. 4, a calculation breviary was drawn up in Math
CAD for the variation of the machine‘s haulage force Ftc between 160 and 250 kN, and the
value of safety coefficients are graphically shown in Fig. 5 for the following constructive
elements [1], [2], [3]:
- lateral connecting plate(Fig. 5a);
- hanger fixed to the station, 2, (Fig. 5b);
-hanger of the connecting device, 3,(Fig. 5c);
- articulation bolt Φ60x245, 4, (Fig. 5d);
- haulage rod Φ57x200, 8, (Fig. 5e);
- attachment bridle for the chain link, 9, (Fig. 5f).
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Safety coefficients resulted by relating to mechanical characteristics of OL 37, 210
N/mm2 flow limit for sheets and improved OLC 45, 500 N/mm
2 flow limit for bolts. The
lowest values are with bending for bolts, reference point 4, Csib=1,28, and with shear of the
fixing bridle hanger of the chain, reference point 9, Csfub=1,29, these values can be amplified
1,7 times, if the relating is made at tear resistance.
Based on the documentation of execution the system of connection of the machine chain
to the actuating station was carried out in Lonea Mining Plant, Fig. 6.
Fig. 6. Chain connecting system to the actuating station carried out in Lonea Mine[3]
CONNECTING SYSTEM TO THE RETURN STATION
Fig. 7 shows the constructive positioning solution of the connecting system of the chain
end calibrated with 26x92 links of the advance mechanism of the 2K-52MY machine,
reference point 2, to the metal structure of the return station, reference point 1.
Fig. 8 shows the constructive solution of the connecting syste, made up of: 1 – hanger
fixed to the station; 2 – articulation bolt Φ60; 3 – chain connecting device; 4 - M30x100
screw; 5 –M30x200 screw.
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Fig. 7. Connecting system positioning to
the return station[3]
Fig. 8. Design solution of the chain end
connecting system to the TR-5return station [3]
The chain end connecting system to the TR-5 return station shows the following
design improvements:
- the hanger fixed to the station, to the lifting bolt by a bolt Φ50 and four screws M30, has in
front a rigid threshold by two bolts Φ50, blocking the turning of the hanger against the station
partition;
- on the outside of the hanger the support for the station anchoring hydraulic prop SVJ
was placed, in a welded structure, solider than the one on the return station;
-by overlapping the prop supports, the error of wrong positioning of the anchoring prop
can be avoided;
- in case of changing the return station, part of the gussets for hardening the prop support
should be discharged with oxyacetylene flame, on the return station, on the hanger‘s
mounting part, and the two holes for screws M30x100 should be made in the lifting hanger.
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Fig. 9. Calculation model for connecting system to return station[3]
Based on the design solution in Fig. 8, the calculation model with constructive
dimensions in view of dimensional verification of its elements, shown in Fig. 9, was drawn
up, where: 1 – station lifting hanger ; 2 – connecting system hanger; 3 – bolt Φ50x100; 4 -
bolt Φ50x120; 5 - screw M30x100; 6 – chain connecting device.
Based on the calculation model in Fig. 9, a calculation breviary in MathCAD was drawn up
for Ftc haulage force variation of the machine, between 160 and 250 kN, and the values of the
safety coefficients are graphically shown in Fig. 10 for the following design elements:
assembling by bolt Φ50x80, 4, and screws M30x100, 5, of the hanger on the station partition,
(Fig. 10a); station lifting hanger, 1, (fig. 10b). Since the values of sliding safety coefficient
Csai are low, an additional blocking of the hanger was carried out against the return station
lifting hanger by bolts Φ50x120, reference point 4, and a vertical rule.
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Fig. 10. Safety coefficients variation of the connecting system to the return station[3]
Based on the execution documents, a connecting system of the machine chain to the
return station was carried out in Lonea Mine.
Fig. 11. Connecting system of the chain tothe return
station carried out in Lonea Mine[3]
Fig. 12. Mouting the machine
to the conveyer[3]
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Fig. 11.To check the way of positioning and movement of the 2K-52MU machine on the
conveyer carried out of TR-5 stations, TR-5 chutes and lateral of TR-7A , the assembly in
Fig. 12 was carried out in Lonea Mine Shops, with new systems of connecting the chain ends
to the machines‘ advance mechanism.
CONCLUSIONS
Even if the cutting height of the machine is not correlated with the height of the face,
an improvement of work conditions results for a minimum reequipping of the face. By
adapting the 2K-52MU machine to a hybrid scraper conveyer, TR-5 stations, TR-6 chutes and
TR-7A laterals, experience was gained in the use of these equipments in the exploitation of
longwalls of individual support ant machine cut. In an endeavor to move the machine on the
conveyer, the connecting systems of the chain ends of the advance mechanism to the
conveyer stations were checked. The information obtained as a result of face reequipping in
Lonea Mine, with the advantages and disadvantages of the method application, will allow in
the future to achieve an optimization of the equipments correlation in a shortwall working.
REFERENCES
[1] Dalban, C., ş.a. – Construcţii metalice, Editura Didactică şi Pedagogică, Bucureşti, 1983.
[2] Găfiţeanu, M. şa - Organe de maşini, vol. I şi II, Editura Tehnică, Bucureşti, 1981 şi 1983.
[3] * * * - Documentaţie tehnică privind adaptarea sistemului de legare a combinei 2K-52
MY de staţiile transportorului tip TR-5 şi verificarea stabilităţii combinei pe transportor,
contract 713/ 26.08.2013, E.M. Lonea
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STUDY OF STABILITY OF 2K-52MU CUTTING-LOADING MACHINE
ON TR-5 CONVEYER IN FACES WITH INDIVIDUAL SUPPORT
PhD, Eng., Consulting Teaching Staff, Răzvan Bogdan ITU, Department of Industrial
Mechanical Engineering and Transport, University of Petrosani, [email protected]
PhD, Associate Prof. Eng., Iosif DUMITRESCU, Department of Industrial Mechanical
Engineering and Transport, University of Petroşani, [email protected]
PhD, Lecturer, Eng., Vilhelm ITU, Department of Industrial Mechanical Engineering and
Transport, University of Petroşani, [email protected]
Abstract: Besides the problem of adapting 2K-52MU machine to la TR-5 scraper conveyer, the
study of stability of the machine on conveyer was required, in faces with individual supports. To
this end stability coefficients of the machine were determined in cutting and loading coal on the
conveyer, and even in blocking the drum at the face. The study was made for maximum 250 kN
traction force and variation of the inclination of the face in the range of 0 and 300 for three cases
of machine movement towards the face.
Keywords: correlating, cutting and loading machine, scraper conveyer
INTRODUCTION
To adapt the existing equipments in view of refurnishing the faces, we should be
familiar with the construction and characteristics of the equipments used and how to correlate
those with the coal extraction mining method, the geological-mining conditions specific to the
exploited layer and with respecting the occupational health and safety standards.
Fig. 1. Extraction method of the longwall with individual support and machine cut
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121
By the implementation of a refurnishing program of a longwall in Lonea Mine during
the fourth trimester of the year 2013, the classical extraction method with a productivity of
6,8 ton/job, was replaced with longwall method with individual support and cut with the
machine with an estimated productivity of 12 tons/job.
CORRELATION OF THE EQUIPMENTS
To see how the equipments were correlated, an analysis of the framework method of
longwall method with cutting the coal with the machine was performed [5]. Fig. 1 shows the
work stages for a face of maximum 3,2m high and 1,8 high cut with the machine, thus: I –
machine in the butt pocket; II –cutting the first slice; III – manual execution of the seat to
mount the articulated beam; IV – advance of the machine in the butt pocket and mounting the
fourth prop; V – cutting the second slice. VI – manual clearing of the face and advance of the
machine in the pocket butt; VII – moving the back prop under the first beam; VIII – ripping
the prop and the back beam.
From the above, it results that an economic efficiency analysis should be made
regarding the correlation of the longwall height with the cutting height of the machine, with
the geological-mining conditions and the occupational safety standards. In this analysis, the
price of the machine should be taken into consideration, which was recovered from cassation,
scrap iron – Euro 2500, rehabilitated and put to use with maximum Euro 5000. The technical
characteristics of the 2K-52MU machine were not correlated with those of the TR-5 scraper
conveyer, especially considering that the latter had not been devised for longwalls, and they
were designed and manufactured by different companies in different countries. The two
equipments are however compatible, at least from the following points of view [1], [5]:
- more than half of the theoretical capacity of cutting of the machine, which is not
reached in practice due to the correlation of the heading speed with the geological-mining
conditions, can be supported by the scraper conveyer;
- dimensionally, the machine can be mounted on the conveyer by adopting suitable
modifications, adapting the TR-5 stations to TR-6 chutes by using TR-7A laterals and by
modifying the machine shoes, without diminishing their resistance characteristics;
- the conveyer‘s robust construction withstands the machine weight of approximately 12
…14 ton;
- the design of the scraper conveyer allows the coal loading by the auger drum in good
conditions;
The main non-correlation of the of the two equipments lies in the fact that the driving
and turning stations of the TR-5 scraper conveyers re not provided with fixing plates/hooks
for the linking device of the end of the traction chain end of the machine.
STUDY OF MACHINE STABILITY ON THE CONVEYE
Starting from the maximum transportation capacity of the TR-5 scraper conveyer of
4,1 ton/min, and knowing the width of the slice that has been cut of 0,63m and its thickness of
1,9 m, the maximum heading speed of 2,45 m/min was determined.
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Knowing the design characteristics of the machine‘s auger drum (diameter, number of
cutting lines, number of bits per face and corner on a cutting line, the width of the cutting
edge of a CMR3 bit) and the 42,7 rpm rotation of the drum, the average depth of the cut was
determined, made by a 0,029 m face bit, and maximum 0,045 m [2], [4].
Fig. 2. Variation of the machine’s heading force and the motor power function
of the inclination angle of the longwall.
With the help of these data, the cutting forces on the auger drum of the machine were
calculated, of 18,9 kN for the drum cutting on the roof and in compact seam, and 10,78 kN for
the drum cutting the floor for 0,7 m high.
The variation of the machine‘s heading force, in kN, and the power required at the
electric driving motor, in kW, function of the inclination angle of the longwall, when it is
inclined towards the main gallery where the driving station ins found, is shown in Fig. 2,
where [5]: Facq – heading force in cutting towards the turning station, in the range of 84,1 -
161,6 kN; Facaq – advance force in cutting towards the driving station, in the range of 84,1 şi
-4,5 kN; Pmotq – necessary force at the electric driving motor in cutting towards the turning
station, in the range of 125,76 - 130,15 kW; Pmsaq – necessary power at the electric driving
motor in cutting towards the driving station, in the range of 125,76 - 120,75 kW.
Facq – heading force in cutting towards the turning station, in the range of 84,1 -161,6 kN;
Facaq – advance force in cutting towards the driving station, in the range of 84,1 şi -4,5 kN;
Pmotq – necessary force at the electric driving motor in cutting towards the turning station, in
the range of 125,76 - 130,15 kW; Pmsaq – necessary power at the electric driving motor in
cutting towards the driving station, in the range of 125,76 - 120,75 kW.
Knowing the technological forces acting on the machine, its design dimensions and how it is
positioned on the conveyer, shown in Fig. 3, the stability of the 2K-52MY machine was
verified, by developing a simplified calculation model for stability, shown in Fig. 4. In Fig. 1
it is noticed that in cutting towards the main gallery, towards the driving station, at angles
larger than 25°, the heading force is compensated by the component of the machine‘s weight,
which was 118,66 kN and a machine-conveyer friction coefficient of 0,25.
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Fig. 3. Design dimensions of 2K-52MY machine and
its position of the conveyer.
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Fig. 4. Simplified calculation model of 2K-52MY machine
stability on the conveyer
It results that for the machine‘s heading, 4 … 7% of the motor power is consumed,
and the greatest part, 90 … 95%, for cutting the coal. The motor power was estimated for a
spare coefficient of 1,25. In the case of the simplified calculation model of the 2K-52MY
machine stability on the conveyer, Fig. 4, points 1 and 2 represent the center of the support
skid of the machine on the longwall side lateral of the conveyer, and points 3 and 4 represent
the captive guiding of the machine on the back lateral of the conveyer [5]. The technological
forces on the auger drum of the machine are represented for two cases, noted with index 1
when it moves towards the driving station, and with index 2, when moving towards the
returning station, with:
Fts, Ftj – cutting force on the upper drum, at the roof, or down, on the floor;
Fas, Faj – force opposing to the machine movement up on the drum, at the roof, and
down on the floor;
Frs, Frj – machine‘s rejection force by the face on the upper drum, at the roof, or down on
the floor.
To determine the weight centre of the machine, 3D modeling of the machine‘s
component parts and their assembling was performed, shown in Fig. 5 [3].
Thus, for a 12095,82 kg weight of the machine, the coordinates of the weight centre
were determined, and the reference system is found in the assembling plan of the feeding
mechanism with the motor, in the horizontal central plane of the motor and on the outside of
the feeding mechanism on the longwall side, for three possible working cases, when the front
drum cuts up on the roof:
a) when the machine moves towards the driving station, the position shown;
b) when the machine moves towards the returning station;
c) when the machine moves with both drums down to clear the longwall.
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Fig. 5. 3D model of 2K-52MY machine with positions
of the weight centre for three working cases
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With the help of these data, the reactions in the leaning points of the machine on the
empty running conveyer were determined, thus in the trials performed in the Mechanical
Workshop in Lonea Mining Plant, the results were, per total for the three cases, high values
on the skids on the longwall side, 90,4 kN and 28,4 kN on the back guides, and the repartition
difference on the skids is 40,8 kN in point 1 and 49,6 kN in point 2, and 17,6 kN in point 3
and 10,6 kN in point 4, respectively. These differences between the reactions on the longwall
side and back are not more than 25%, as it is recommended in the literature of specialty. The
greater load on the skids on the face side, which was highlighted at the machine movement on
the conveyer at the functioning trials at the surface, are lower during the cutting of coal, due
to the technological forces acting on the machine. The maximum contact pressure between the
skid and the conveyer lateral is 3,76 N/mm2, very near the admissible pressure at the guides of
machine-tools, of 4 N/mm2.
Figure 6. Variation of stability coefficients
function of the longwall inclination angle, case 1
Figure 7. Variation module of stability coefficients
function of the longwall inclination angle, case 2
Variation module of stability coefficients function of the longwall inclination angle, case 2
four lines determined by the support points, whose variation depending on the angle of the
longwall inclination is shown in Fig. 6, where:
Cs14q – stability coefficient according to line 1-4, with values in the range of 2,95 and 2,48;
Cs23q – stability coefficient according to line 2-3, with values in the range of 4,61 and 6,95;
Cs12q – stability coefficient according to line 1-2, with values in the range of 5,98 and 5,5;
Cs34q – stability coefficient according to line 3-4, with values in the range 2,95 and 2,62;
Cs14bq – stability coefficient according to line 1-4 when the upper drum is blocked and the
traction force reaches maximum 250 kN, with values in the range of 1,53 and 1,51;
Cs23bq – stability coefficient according to line 2-3 when the lower drum is blocked and the
traction force reaches maximum 250 kN, with value in the range of 1,67 and 1,24.
Verification of the stability of 2K-52MY machine on the conveyer, during cutting
towards the return station, case 2, was made by calculation of the stability coefficients
according to the four lines determined by the support points, whose variation, depending on
the longwall inclination angle, is shown in Fig. 7, where:
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Cs14q – stability coefficient according to line 1-4, with values in the range of 3,0 and 2,12;
Cs23q – stability coefficient according to line 2-3, with values in the range of 5,27 and 3,34;
Cs12q –stability coefficient according to line 1-2, with values in the range of 5,98 şi 5,5;
Cs34q – stability coefficient according to line 3-4, with values in the range of 2,95 şi 2,62;
Cs14bq – stability coefficient according to line 1-4, when the lower drum is blocked and the
traction force reaches maximum 250 kN, with values in the range of 1,24 and 1,22;
Cs23bq – stability coefficient according to line 2-3 when the upper drum is blocked and the
traction force reaches maximum 250 kN, with values in the range of 1,21 and 1,0.
Fig. 8. Variation of stability coefficients depending on the longwall inclination, case 3
Verification of the 2K-52MY machine stability on the conveyer during loading the coal
that has been cut towards the returning station, case 3, was made by the calculation of the
stability coefficients according to the four lines determined by the leaning points, whose
variation, depending on the longwall inclination angle is shown in Fig. 8, where:
Cs14q – stability coefficient according to line 1-4, with values in the range of 2,94 and 1,93;
Cs23q – stability coefficient according to line 2-3, with values in the range of 36,7 and 7,56;
Cs12q – stability coefficient according to line 1-2, with values in the range of 12,64 and 11,03;
Cs34q – stability coefficient according to line 3-4, with values in the range of 19,2 and 16,78;
Cs14bq – stability coefficient according to line 1-4 when the lower drum is blocked and the
traction force reaches maximum 250 kN, with values in the range of 1,25 and 1,2; Cs23bq –
stability coefficient according to line 2-3 when the lower drum is blocked and the traction
force reaches maximum 250 kN, with values in the range of 50 - 14,34.
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CONCLUSIONS
The study of 2K-52MY machine stabilityon the conveyer showed that all the stability
coefficients have values higher than 1,2 as it is limited in the literature of specialty, even in
the case of blocking of a drum in the longwall, due to sterile intercalation and haulage of the
machine with maximum force of 250 kN, except for the movement during cutting towards the
return station, case 2, when in the event of the upper drum being blocked, the stability
coefficient according to line 2-3, has smaller values than 1,2 [5]. It is seen that in the two
cases of machine movement during cutting, case 1 and 2, when a drum is blocked due to
sterile intercalations, or due to other causes (wear or lack of bits for the cutting part) the
stability coefficients values reduce greatly, and great reactions result horizontally on the
machine‘s captive guides, of up to 100 kN, in case 1, much greater than the friction force
between the conveyer and the longwall floor, leading to tear of the conveyer and even to
breaking the articulations between the chutes and the back laterals, since the conveyer chutes
are not supported in the longwall as in the case of mechanized support. To avoid the situations
presented above, of conveyer tear horizontally, the following measures of exploitation for the
equipments are recommended:
- at the beginning of each shift or whenever required, the sterile intercalations should be
visually checked and localized, all along the longwall, and their derocking should be done
with the hammer; after cutting a slice with the machine, the condition of the bits is checked of
the cutting parts and the worn and broken ones are replaced and the missing ones are
completed;
- cutting a slice with the machine in the longwall is made by moving the machine
towards the turning station of the conveyer, case 2, when the reactions on the machine‘s
captive guides are not greater than 50 kN, this value being half of the one in case 1;
- reduction of the pressure value of the advance mechanism from 160 bar to 120 bar,
which reduces the maximum traction force from 250 kN to 187, kN, and the reactions
horizontally from 50 kN to 37,5 kN, by 25%, respectively.
REFERENCES
[1] Hirian, M., Kovacs, I., - Maşini miniere, Institutul de Mine Petroşani, Petroşani 1987;
[2] Iliaş, N., Zamfir, V., Kovacs, I., ş.a. - Maşini miniere. Exemple de calcul, Editura Tehnică,
Bucureşti, 1993.
[3] Muscă G. – Proiectarea asistată folosind Solid Edge, Editura Junimea, Iaşi, 2006.
[4] Posea, N., ş.a. – Rezistenţa materialelor, Probleme, Editura Ştiinţifică şi Enciclopedică,
Bucureşti, 1986.
[5] * * * - Documentaţie tehnică privind adaptarea sistemului de legare a combinei 2K-52
MY de staţiile transportorului tip TR-5 şi verificarea stabilităţii combinei pe transportor,
contract 713/ 26.08.2013, E.M. Lonea.
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INFLUENCE OF THE SUSPENSION PARAMETERS UPON THE
HUNTING MOVEMENT STABILITY OF THE RAILWAY VEHICLES
Mădălina DUMITRIU
Department of Railway Vehicles, University Politehnica of Bucharest
Abstract: The hunting movement of the railway vehicles is essential for the safety, the comfort of
the passengers and the integrity of the transported goods. The dynamic performance of a railway
vehicle can be seriously damaged, due to the phenomenon of instability of the hunting motion that
occurs when a certain speed is exceeded – the critical one. An important role is played by the
suspension parameters in the extension of the stability interval during hunting motion at high
velocities. And this is what the paper draws attention to, based on the analysis of how the elasticity
and damping suspension characteristics influence the critical speed.
Keywords: railway vehicle, hunting, critical speed, suspension
1. INTRODUCTION
The hunting motion is specific for railway vehicles, as a result of the fact that the rolling
surfaces of the wheels have a reversed conicity, provided that they are rigidly fixed on the
axle. The hunting of the wheelsets is conveyed via the suspension elements to the entire
vehicle, thus generating vibrations that can affect the safety, comfort of the passengers or the
integrity of the transported goods [1, 2].
What is particular about the hunting movement is the dependence of its nature on the
velocity, whether it is stable or unstable. For relatively low velocities, the vehicle has a stable
hunting motion. Its movement occurs in the vicinity of the balance position and is maintained
by the geometrical irregularities of the track. Starting from a certain speed, called critical
speed, the hunting movement of the vehicle becomes unstable. The loss of stability is
manifest in the increase of the amplitude in the movements of wheelsets, which will reach to
hit the interior flanges of the rails. From a practical perspective, the phenomenon of the
instability in the hunting motion is essential, since it restricts the maximum velocity of the
vehicles.
The extension of the stability range of the hunting depends on a series of parameters of
the vehicle– the equivalent conicity of the wheel rolling surface, the wheelset mass and inertia
momentum, the bogie axle base, the bogie inertia momentum [3, 4, 5]. An important role is
also played by the vehicle suspension by its stiffness and damping characteristics [5, 6, 7].
This paper focuses on the influence of stiffness and damping on the transversal and
longitudinal direction of the suspension upon the stability of the hunting motion during the
vehicle running on the alignment.
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To this purpose, the vehicle is modelled via a 21-degree-of-freedom system, which
includes all its basic components – the carbody, the suspended masses of the bogies and the
wheelsets, as well as the elastic and damping elements of the two levels of suspension.
Solving the issue of stability is based on the analysis of the system‘s matrix eigenvalues,
comprising the movement equations describing the free vibrations of the vehicle and resulting
into the establishment of the critical speed. The possibilities of an increase in the vehicle‘s
critical speed is pointed out at, via a better choice of the suspension parameters.
2. THE VEHICLE MECHANICAL MODEL AND MOVEMENT EQUATIONS
The mechanical model to study the horizontal-transversal vibrations of a 4-axle vehicle,
two levels of suspension, travelling at a constant speed V on a tangent track is shown in
figures 1 and 2. This contains 7 rigid bodies representing the carbody, the suspended masses
of the bogies and the 4 wheelsets, connected among them through Kelvin-Voigt systems, by
which the two levels of suspension are modelled.
The vehicle carbody is assimilated to a three-degree-of-freedom rigid, with the following
movements: lateral displacement yc, rolling c and yaw c. This is supported in four points by
the elements of the secondary suspension that have the transversal basis 2bc. It is about the
secondary suspension‘s springs of the vehicles, which can deform themselves in three
directions and whose rigidities are noted with kxc, kyc and kzc. Every bogie has a system with
an anti-rolling torsion bar, whose stiffness is kc. In the vertical direction, the secondary
suspension of a bogie has two dampers with the damping constant czc, and in the horizontal
direction, there is one damper whose damping constant is cyc. Similarly, there will be
considered the antiyawing dampers that are mounted on the lateral sides of the bogies, with
the damping constant cxc. The following carbody parameters are to be mentioned: mass mc
and the inertia moments around the longitudinal axis Jxc and the vertical axis Jzc, respectively.
The height of the carbody centre of mass compared to the secondary suspension plan is hc,
and the vehicle axlebase is 2ac.
The bogie carriage (the bogie suspended mass) is also considered a three-degree-of-
freedom rigid, namely lateral displacemeent ybi, rolling bi and yaw bi, with i = 1 or 2, as it
regards the front or the rear bogie. This carriage supports the elements of the secondary
suspension and is resting in four points on the wheelsets, via the elements of the primary
suspension. The main parameters of the bogie carriage are its mass mb, the inertia moment in
respect to the longitudinal axis Jxb, and the inertia moment in respect to the vertical axis Jzb.
The bogie mass center is located at the distance of hb1 from the primary suspension plan and
at hb2 from the secondary suspension plan. It should be mentioned that the bogie has the
axlebase of 2ab.
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Fig. 1. The mechanical model of the vehicle – frontal view.
Fig. 2. The mechanical model of the vehicle – top view.
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The elements of the primary suspension also operate after three directions and they have
the rigidities kxb, kyb, kzb and the damping constants cxb, cyb and czb. The Kelvin-Voigt systems
placed in the plan of the axles, at the distance hb1 from the mass center of the bogie suspended
side, model their elastic driving. The transversal basis of the primary suspension is 2bb.
In terms of the wheelsets, they are considered to be able to perform the following
independent movements: one movement of lateral translation, yoj,(j+1), and a rotation
movement – yaw, oj,(j+1), where j = 2i – 1, with i = 1 or 2, mentioning that the bogie i has the
axles j and j + 1. Similarly, the wheelset makes a rotation movement around its own axis, at
the angle speed oj,(j+1) = V/ro + oj,(j+1), where oj,(j+1) is the angle sliding velocity of the axle
compared to V/ro, and ro is the radius of the rolling circle when the axle takes the median
position on the track. The following parameters will be considered: mass mo and the inertia
moments Jyo and Jzo.
The movement equations of the vehicle are as below:
- the carbody movement equations (lateral displacement, rolling, yaw)
.0)()(22
)()()(2
21221
21221
bbbbbcccyc
bbbbbcccyccc
hyyhyk
hyyhycym (1)
0
)()()(22)(2)2(
)()()(2)(22
21221212
21221212
ccc
bbbbbccccycbbcczcc
bbbbbccccycbbcczccxc
ghm
hyyhyhkbkk
hyyhyhcbcJ
(2)
.0)()(22)](2[2
)()(2)](2[2
21221212
21221212
bbbbbcccycbbccxc
bbbbbcccycbbccxcczc
hyyaakbk
hyyaacbcJ (3)
- the bogie movement equations (lateral displacement, rolling, yaw), for i = 1, 2 and j = 2i – 1
0)()(22))1((2
)()(22))1((
)1(11
2
)1(11
12
joojbjbbjybcci
cccbibbiyc
joojbibbiybcci
cccbbbiycbib
yyhykahyhyk
yyhycahyhycym
(4)
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02
4
)()(22))1((2
))(2(4)()(22
))1(()(2
1122
)1(111
22
22)1(11
122
2
bibbc
bzb
joojbibibbybcci
cccbibibbyc
cbiczccbibzbjoojbibibbyb
cci
cccbibibbyccbiczcbixb
mhm
hgbk
yyyhhkahyyhhk
bkkbcyyyhhc
ahyyhhcbcJ
(5)
.0)](2[2)](2[2
)(2)](2[2
)](2[2)(2
)1()1(2
2)1(
)1(22
joojbibbybjoojbibxb
cbicxcjoojbibbyb
joojbibxbcbicxcbizb
yyaakbk
bkyyaac
bcbcJ
(6)
- the axle movement equations (lateral displacement, yaw, rotation around its own axis), for
i = 1, 2 and j = 2i – 1
211)1(,
1)1(,)1(,
2
2
jjbibbibbijojyb
bibbibbijojybjojo
YYahyyk
ahyycym
(7)
).(
)(2)(2
2)1(,1)1(,
)1(,2
)1(,2
)1(,
jjjjoojo
yo
bijojbxbbijojbxbjojzo
XXer
VJ
bkbcJ
(8)
)( 2)1(,1)1(,)1(, jjjjojojyo XXrJ , (9)
where Xj,(j+1)1,2 represent the longitudinal forces, and Yj,(j+1)1,2 – the guiding forces acting upon
the axle j and (j+1) respectively, at the contact points of the wheels 1 or 2 with the rails.
Based on the analysis of the system matrix eigenvalues derived from the equations (1 -
9) turned into first-order differential equations, a quality-based evaluation can be done for the
stability in the vehicle movement, with the calculation of the critical speed during hunting as a
result.
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3. NUMERICAL APPLICATION
This section deals with the influence of the elasticity and damping characteristics in the
longitudinal and transversal direction of the suspension upon the critical speed while hunting.
During the numerical simulations, the parameters have been appropriately adapted to a Y 32R
bogie-fitted passenger railway vehicle, with a maximum velocity of 200 km/h. For the
reference values of the vehicle, the critical speed of 261.56 km/h has been calculated.
Fig. 3. Influence of the secondary suspension upon the critical speed:
(a) influence of the elasticity characteristics; (b) influence of the damping characteristics.
(b)
Fig. 4. Influence of the primary suspension upon the critical speed:
(a) influence of the elasticity characteristics; (b) influence of the damping characteristics.
Figure 3 shows the critical speeds calculated for values of the secondary suspension
rigidities within the range of 104 N/m and 10
6 N/m and dampings between 10
3 Ns/m and 10
5
Ns/m.
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In diagram (a), the high value of the critical speed is visible (374.89 km/h) for high
rigidities of the secondary suspension (kxc = kyc= 106 N/m). The increase of the critical speed
compared to the reference value is still possible should only one of the two suspension
parameters is modified. While the reference value (kyc= 1.7105 N/m) is maintained in the
transversal direction and the value of 106 N/m is adopted for kxc, the result is the critical speed
of 302.34 km/h. Upon considering the reference value kxc= 1.7105 N/m and increasing the
transversal stiffness of the suspension up to 106 N/m, the critical speed of 314.43 km/h is
obtained. The diagram (b) shows, on the one hand, the increase of the critical speed during the
raising of the secondary suspension damping in the transversal direction. Should the situation
corresponding to the damping reference value in the longitudinal direction cxc = 6.46104
is
looked at and the transversal damping is increased to 105 Ns/m, the critical speed of 319.22
km/h will be the result. On the other hand, the rise in the critical speed can be also obtained
by the increase in the secondary suspension damping in the longitudinal direction. Thus, if the
reference value of cyc = 1.52104 Ns/m is maintained and only the suspension longitudinal
damping is increased (cxc = 105 Ns/m), the critical speed can be raised up to 269 km/h. Finally,
should cxc = cyc = 105 Ns/m is adopted, the critical speed can be 320 km/h.
The diagram (a) in figure 4 shows the results concerning the critical speed for various
values of the primary suspension rigidities within the interval of (105 ... 10
8) N/m, and in
diagram (b) the critical speed is calculated for dampings that can have values from 103 Ns/m
to 105 Ns/m. The diagram (a) points out at a series of interesting aspects related to the way in
which the stiffness in the longitudinal and transversal directions of the primary suspension
affects the value of the critical speed. It is about the fact that an increase in the longitudinal
stiffness leads to a higher critical speed, but this only occurs for certain values of the stiffness
in the transversal direction. Should this range is exceeded, an opposite effect will result, i.e. a
decrease in the critical speed. Further, the diagram (b) of the figure 4 shows that a slightly less
increase of the critical speed is possible by lowering the damping in the primary suspension.
As an example, for cxb = cyb = 103 Ns/m, the critical speed rises from the reference value of
261 km/h to 269 km/h.
4. CONCLUSIONS The dynamic performance of the railway vehicles, defined in terms of safety, comfort of
the passenger and the integrity of the transported merchandise, can be seriously damaged, due
to the phenomenon of instability of the hunting motion that occurs at higher speed than the
critical one. The stability interval for the hunting can be extended at high velocities by
adopting certain parameters of the vehicle, among which the stiffness and the suspension
damping are essential.
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This paper examines the possibilities to increase the critical speed by adopting the best
values of the vehicle suspension parameters. It has been proved that an increase of the
stiffness and damping in the longitudinal and transversal directions of the secondary
suspension, the critical speed of the vehicle can be higher. Likewise, it is demonstrated that
higher critical speeds can result from the correlation of the values of longitudinal and
transversal stiffness of the primary suspension. A less increase in the critical speed turns into
a lower damping in the primary suspension of the vehicle.
REFERENCES
[1] Sebeşan, I., Dinamica vehiculelor feroviare, Ed. MatrixRom, Bucureşti, 2011.
[2] Sebeşan, I., Mazilu, T., Vibraţiile vehiculelor feroviare¸ Ed. MatrixRom, Bucureşti,
2010.
[3] Polach, O., Influence of wheel/rail contact geometry on the behaviour of a railway vehicle
at stability limit, ENOC – 2005, Eindhoven, Netherlands, 7 – 12 aug. 2005, pp. 2203 –
2210.
[4] Dabin, C., Li, L., Jin, X., Xiao, X., Ding, J., Influence of vehicle parameters on critical
hunting speed based on Ruzicka model, Chinese Journal of Mechanical Engineering,
Jan., 2012, pp. 1-7.
[5] Serajian,R., Parameters’ changing influence with different lateral stiffnesses on
nonlinear analysis of hunting behavior of a bogie, Vibroengineering. Journal of
Measurements in Engineering, Vol. 1, Iss. 4, 2013, pp. 195-206.
[7] Yabuno, H., Okamoto T., Aoshima, N., Effect of lateral linear stiffness on nonlinear
characteristics of hunting motion of a railway wheelset, Meccanica, Vol. 37, 2002, pp.
555–568.
[8] Huang, C., Zeng, J., Liang, S., Carbody hunting investigation of a high speed passenger
car, Journal of Mechanical Science and Technology, Vol. 27, No. 8, 2013, pp. 2283-
2292.
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THE DYNAMIC BEHAVIOUR OF THE RAILWAY VEHICLES IN
CROSSING AN ISOLATED NIVELMENT DEFECT
Mădălina DUMITRIU
Department of Railway Vehicles, University Politehnica of Bucharest
Abstract: The vibrations in the vertical plan of the railway vehicles are mainly initiated by the
interaction with the track that can have nivelment defects due to its construction. The maximum
values of such defects correspond to the isolated defects that lead to a higher intensity of the
vibrations behaviour of the vehicle while crossing them and, hence, this situation needs to be
considered when evaluating the dynamic behaviour of the railway vehicle. The paper focuses on
the movements of the running gear and the maximum accelerations at the carbody level when
crossing an isolated nivelment defect, derived from numerical simulations.
Keywords: railway vehicle, dynamic behaviour, isolated defect, vertical vibrations
1. INTRODUCTION
The quality of the track can be affected by a series of deviations from the ideal
geometry, which come in the shape of certain defects of longitudinal or transversal nivelment,
alignment defects or gauge defects, plus the track torsion [1]. The quality levels of the track
are established in dependence on the extent of such defects [2, 3]. To evaluate the dynamic
behavior of the railway vehicles in terms of the safety, ride quality and the track fatigue
attention should be paid to the values of the standard deviations of the defects of longitudinal
nivelment and of the alignment of track, as well as the maximum values of the isolated
defects of this type [2].
The nivelment defects represent the main cause of the vertical vibrations in the vehicle
[4], for which the bouncing, pitch vibrations are essential for its dynamic behaviour, along
with the carbody bending vibrations [5 - 9]. During certain running conditions – the crossing
of an isolated defect in the nivelment at a high speed – the vibration behaviour of the vehicle
is much more amplified and the vertical accelerations at the carbody level can reach values to
damage the ride quality.
This paper examines the dynamic behavior in a railyway vehicle during a crossing at
speed of 200 km/h over an isolated defect of nivelment with the maximum amplitude
admitted for a track with a QN2 quality level. The movements of the running gear and the
accelerations at the carbody level in three reference points – at the centre and above the two
bogies – are being analyzed. In this context, the accelerations are shown to be lower at the
centre of the carbody and higher above the bogies, and maximum above the rear bogie.
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The numerical simulations are based on a mechanical model of the vehicle, of a
discrete-continuous type, where the carbody is modelled via an Euler-Bernoulli beam and the
wheelsets and the suspended masses are assimilated to rigid bodies [8, 9]. This model allows
to take into consideration both the rigid vibration modes of the carbody and the bogies –
bounce and pitch, as well as the complex vibration modes of the carbody – the symmetrical
and antisymmetrical bending.
2. THE VEHICLE MECHANICAL MODEL AND MOVEMENT EQUATIONS
The mechanical model to study the dynamic behaviour of a two-level suspension railway
vehicle while crossing over an isolated defect of nivelment is shown in figure 1. It is about a
discrete-continuous model, where the vehicle carbody is modelled via an Euler-Bernoulli
beam of constant section and mass of uniform distribution, and the suspended masses of the
bogies and those four wheelsets are assimilated to rigid bodies. The two levels of suspension
of the vehicle are modelled by means of Kelvin-Voigt systems [8, 9].
Fig. 1. The mechanical model of the vehicle.
For the vehicle carbody, the first two natural modes of bending in the vertical plan
(symmetrical and antisymmetrical) are considered, as well as the rigid vibration modes,
namely the bounce zc and pitch c.
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The following carbody parameters are mentioned: mc – the carbody mass; 2ac – the
carbody wheelbase; Jc – the inertia moment for the pitch movement; L – the carbody length;
EI – the bending module; - the coefficient of structural damping. The suspended masses of
the bogies can carry out bounce movements zbi, and pitch bi, with i = 1, 2. The mass of a
bogie is mb, its wheelbase is - 2ab, and the inertia moment for the pitch movement is Jb. The
characteristics of the secondary suspension elements pertinent to a bogie are represented by
the elastic and the damping constants 2kzc and 2czc; at the primary suspension level,
corresponding to a suspension, the elastic and the damping constants are noted with 2kzb and
2czb.
Should consider that the stiffness of the track is much higher than the stiffness of the
suspension levels, and the natural frequencies of the wheelsets are higher than the ones for the
vehicle, the hypothesis of the rigid track will be adopted.
As a result, the vertical movements of the wheelsets j (where j = 1...4) are equal with
the dimension of the isolated nivelment defect (xj) against them, and they can be calculated
from the below equations
0)( jj x , for xj < 0; )()( jjj xx , for xj ≥ 0, (1)
where xj represents the x-coordinate along the track and is given by the axle position in the
vehicle, as such
xx 1 ; baxx 2 ; caxx 23 ; cb aaxx 224 , where x = Vt. (2)
Upon applying the method of the modal analysis, the movement equations of the vehicle
can be written as follows:
- for the carbody bounce
; 0)()]()([22
)()]()([22
2122122
2122122
bbczc
bbczccc
zzlXlXTzk
zzlXlXTzczm (3)
- the carbody pitch
; 0)()]()([)]()([22
)()]()([)]()([22
211323312222
211323312222
bbccczc
bbccczccc
zzlXlXTlXlXTaak
zzlXlXTlXlXTaacJ (4)
- the carbody symmetrical bending
; 0)]()([)]()([)]()([2
)]()([)]()([)]()([2
2221212221
2222212
2221212221
2222212
222222
lXzlXzlXlXTlXlXzk
lXzlXzlXlXTlXlXzc
TkTcTm
bbczc
bbczc
mmm
(5)
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- the carbody antisymmetrical bending
; 0)]()([)]()([)]()([2
)]()([)]()([)]()([2
2321312231
2331323
2321312231
2331323
333333
lXzlXzlXlXTlXlXak
lXzlXzlXlXTlXlXac
TkTcTm
bbcczc
bbcczc
mmm
(6)
- for the bounce of the bogies
; 0)()(2
)()(2
)2(2)2(2
32,1322,122,1
32,1322,122,1
4,23,12,14,23,12,12,1
TlXTlXazzk
TlXTlXazzc
zkzczm
cccbzc
cccbzc
bzbbzbbb
(7)
- for the pitch of the bogies
0)2(2)2(2 4,23,12,14,23,12,12,1 bbbzbbbbzbbb aakaacJ , (8)
where l1 and l2 are the positions of the leaning points of the carbody on the secondary
suspension, Tn is the time coordinate of the natural bending mode n (n = 2, 3), and
)cosh(coscoshcos
sinhsinsinhsin)( 2,12,12,12,12,1 ll
LL
LLlllX nn
nn
nnnnn
(9)
are the natural functions of the first two modes of the carbody vertical bending, where
EILmcnn /2 , n is the natural pulsation of the vibration mode n.
It is also mentioned that mm2,3, cm2,3 and km2,3 represent the masses, dampings and the
modal stiffnesses of the carbody symmetrical and antisymmetrical bending modes [8].
The solution of the movement equations in (1-8) is in the application of the Runge-Kutta
algorhythm.
3. NUMERICAL APPLICATION This section deals with the results of the numerical simulation of the dynamic behaviour
of the railway vehicle during crossing over an isolated nivelment defect of an amplitude o
and length whose analytical form is given by the equations below
)/(sin)( 2 xx o , for 0 ≤ x ≤
0)( x , for x < 0 or x > .
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The maximum amplitude of the defect admitted by UIC leaflet 518 [2] for a track with
QN2 quality level and o = 9 mm will be considered and the defect length is established based
on the regulations concerning the track construction and maintenance, = 10.8 m [10]. The
parameters of the vehicle model are presented in table 1. Table 1
Carbody mass mc = 34320 kg
Bending module EI = 3.2109 Nm
2
Carbody length L = 26.4 m
Carbody wheelbase 2ac = 19 m
Carbody pitch inertia moment Jc = 7.6 kgm2
Carbody damping ratio m2,3 = 0.015
Vertical stiffness of the secondary suspension 4kzc = 2.4 MN/m
Vertical damping of the secondary suspension 4czc = 68.88 kNs/m
Bogie mass mb = 3200 kg
Bogie pitch inertia moment Jb = 2048 kgm2
Bogie wheelbase 2ab = 2.56 m
Vertical stiffness of the primary suspension 4kzb = 4.4 MN/m
Vertical damping of the primary suspension 4czb = 52.21 kNs/m
The figures 2 and 3 show the travelling of the running gear of the vehicle while crossing
the isolated nivelment defect at the speed of 200 km/h. There are also included the
movements of the wheelsets, of the bogie frames against the axles and of the centre of each
bogie. Generally speaking, the time history of the components in the two bogies are similar,
which proves that there is weak coupling among them. The rear bogie has a certain delay in
crossing the isolated defect, of 0.35 s, corresponding with the travelling of the distance
between the bogies at a given speed. Similarly, the second axle of each bogie crosses over the
track defect with a delay of circa 0.046 s behind the first axle. The moment the first axle
passes over the isolated defect, the bogie frame makes a combined movement between pitch
and bounce. The bounce comes from the movement of the bogie centre, which has a similar
path with the defect‘s. The pitch movement makes the point on the bogie frame above the rear
axle rise, while the point on the corresponding frame of the front axle come down.
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Fig. 2. The movements of the axles and of the first bogie frame:
──, axle 1; ──, bogie frame above the axle 1; ──, axle 2;
──, bogie frame above axle 2; ──, bogie centre.
Fig. 3. The movements of the axles and of the second bogie frame:
──, axle 3; ──, bogie frame above the axle 3; ──, axle 4;
──, bogie frame above axle 4; ──, bogie centre.
Fig. 4. The carbody acceleration; : ──, at the centre; ──, over the front bogie;
──, over the rear bogie.
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The presence of the two movements, pitch and bounce, are made also visible by the
paths of the three points on the bogie that are shifted. The bogie pitch movement is quickly
damped after crossing the defect, and so will tend the bounce to do. This aspect is clearly seen
in the fact that all three bogie points, at the centre and above the two wheelsets, practically
have the same movements.
Figure 4 shows the carbody acceleration at its centre and above the two bogies. The
excitation of the two movements, bounce and pitch, is visible here. The pitch movement can
be noticed in which the carbody is engaged when the front bogie touches the track irregularity
– the point above the rear bogie rises, while the point against the front bogie goes down. This
movement has a slow damping, which is obvious from the fact that the points above the
bogies vibrate in anti-phase, as it can be seen in the second part of the movement, after the
front bogie has also crossed over the defect area. On the other hand, the carbody bounce
damps more quickly, as noticed in the acceleration of the carbody centre.
Similarly, the influence of the carbody symmetrical bending can be identified in the
modulations imposed to the acceleration, more at the carbody centre and less above the
bogies. The maximum acceleration is recorded above the bogies, namely 0.66 m/s2 - above
the front bogie and 0.82 m/s2 – above the rear bogie.
4. CONCLUSIONS To have a numerical simulation of the dynamic behaviour of the four-axle railway
vehicle during crossing an isolated nivelment defect, this needs to be mechanically modelled
by a 8-degree-of-freedom system of a discrete-continuous nature. The model includes the
basic elements of the vehicle, such as the carbody – modelled by an Euler-Bernoulli beam, the
wheelsets and the suspended massed of the bogies – considered as rigid bodies, as well as the
elements of the suspension, modelled via Kelvin-Voigt systems.
The analysis of the movements in the vehicle running gear highlights the pitch and
bounce movements that are excited during the crossing over the isolated nivelment defect.
These movements are conveyed from the bogies farther to the vehicle carbody via the
elements of the secondary suspension, visible in the accelerations calculated at its level.
Likewise, the carbody symmetrical bending movement is identified, and it is stronger at its
centre and weaker above the two bogies.
The accelerations are also noticed to be lower at the carbody center and higher above the
bogies, where the maximum acceleration is recorded above the rear bogie.
REFERENCES [1] Mazilu, T., Dumitriu, M., Metode şi proceduri de cercetare experimentală şi încercare a
vehiculelor feroviare, Editura MatrixRom, Bucureşti, 2012.
[2] UIC Leaflet 518, Testing and approval of railway vehicles from the point of view of their dynamic
behaviour – Safety – Track fatigue – Running behaviour, 2009.
[3] EN 13848-1, Railway applications. Track geometry quality. Part 1. Characterization of track
geometry, 2006.
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[4] Sebeşan, I., Mazilu, T., Vibraţiile vehiculelor feroviare¸ Editura MatrixRom, Bucureşti, 2010.
[5] Zhou, J., Goodall, R., Ren, L., Influences of car body vertical flexibility on ride quality of
passenger railway vehicles, Journal of Rail and Rapid Transit, Vol. 223, 2009, pp. 461-471.
[6] Cheli, F., Corradi, R., On rail vehicle vibrations induced by track unevenness: Analysis of the
excitation mechanism, Journal of Sound and Vibration, Vol. 330, 2011, pp. 3744–3765.
[7] Diana, G., Cheli, F., Collina, A., Corradi, R., Melzi, S., The development of a numerical model
for railway vehicles comfort assessment through comparison with experimental measurements,
Vehicle System Dynamics, Vol. 38, no. 3, 2002, pp. 165- 183.
[8] Dumitriu, M., Influence of the suspension damping on ride comfort of passenger railway vehicles,
UPB Scientific Bulletin, Series D: Mechanical Engineering, iss. 4, vol. 74, 2012, pp. 75-90.
[9] Dumitriu, M., Influence of damping suspension on the vibration eigenmodes of railway vehicles,
Mechanical Journal Fiability and Durability, Issue 1, 2013, pp. 109 – 115.
[10] Instrucţia de norme şi toleranţe pentru construcţia şi întreţinerea căii, nr. 314, MTTc, 1989.
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CRANK WEB DEFLECTIONS OF MARINE DIESEL ENGINES
Eng. PhD. Candidate, NOVAC GEORGE
―Mircea cel Batran‖ Naval Academy, Constanta
Abstract: In order to establish the proper functioning of a marine diesel engine, respectively the
crankshaft bearing condition and uniformity of thermal processes taking place in each cylinder, a
study was made over the crankshaft of a MAN B&W 7K80 MC-C engine, over a period of about
four years by measuring the crank web deflections during overhauls or various repairing
operations on board. The study includes measurements made by the crew of the ship and related
graphics recording the crank web deflections evolution depending on the number of engine
operation hours.
Keywords: deflections, marine, crankshaft, engine, measurements.
1. INTRODUCTION
The entire chemical process that takes place inside the cylinder of the internal
combustion marine diesel engine is materialized by transforming into mechanical
work on crankshaft and further on the propulsin plant‘s propeller.
The translational motion of the piston is converted through the crank mechanism into
rotating motion of the crankshaft. The gas pressure forces produced in the combustion
chamber are thus discharged through intermediate components - piston, connecting
rod, cross head – in loads of journals and crankpin bearings.
Because of this, crankshaft deflections are measured periodically, ensuring that
journals and crankpin bearings are performing their lubrication role efficiently.
The crankshaft components are illustrated in Figure 2.3.
2. MEASUREMENTS
Overhaul and control operations of crankshaft deflection are performed by the
embarked crew on the merchant vessel during the performed international voyages.
Indications of making these deflection measurements are provided by engine
documentation manual [1], and shown in Figures 2.1, 2.2 [2].
The marine diesel engine included in this study is a MAN B&W 7K80 MC-C model,
and measurements are extended over a period of approximately four years.
Values to be taken into consideration for the final evaluation of the crankshaft
deflection are actually the ―V‖ (deflection of vertical misalignment) and ―H‖
(deflection of horizontal misalignment) values, where ―V‖ and ―H‖ are the differences
between the deflections measured in two of the five areas shown in Figure 2.2. More
specifically: V = T-B, and H=C-E [2].
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Fig. 2.3. Crankshaft components:
1 – flange; 2,4 – screw; 3,11 – crankshaft; 5,6 – guard; 7 – nut; 8 – fitted bolt; 9 – split
pin; 10 – chain wheel; 12 – gasket; 13 – cover, 14 – screw; 15 – locking wire. [1]
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Fig. 2.1
Fig. 2.2. Measurement indications
This study includes six measurements (M1, M2, M3, M4, M5, M6)
performed on the crankshaft, depending on the number of engine operating hours,
the crankcase temperature, date and place of the ship during measurements and
also ship‘s trim (Table 2.1) – [2].
Table 2.1. Measurements values [2]
Date: Crankcase
temp.:
Runing
hours: Place: Trim:
M1 30.05.2006 48⁰C 698 Road to Shanghai Fwd.-7,7m/Aft.-9.3m
M2 02.09.2008 40⁰C 16071 Yokohama (drifting) Fwd.9,0m/Aft.10.0m
M3 02.04.2009 39⁰C 20191 Hong-Kong
(anchored) Fwd.9,05m/Aft.9,5m
M4 23.02.2010 45⁰C 26250 Manzanillo Fwd.8,6m/Aft.10,55m
M5 25.11.2010 45⁰C 31255 Hong-Kong
(anchored) Fwd.5,2m/Aft.5,8m
M6 01.02.2010 45⁰C 31256 Hong-Kong
(anchored) Fwd.5,2m/Aft.5,8m
The following charts (Figures 2.4, 2.5) shows the evolution of the ―V‖ and
―H‖ values between 30.05.2006 and 01.12.2010.
At the top of each chart is schematically represented the crankshaft but only
for illustrative purposes in order to highlight the individual measurement value for
each of the seven crankshaft journals.
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Fig. 2.4. Deflections evolution of vertical misalignment (“V”) [2]
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Fig. 2.5. Deflections evolution of horizontal misalignment (“H”) [2]
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3. CONCLUSIONS
The graphs above, correlated with other measures for each cylinder-piston
group in part, may reveal information relating to the proper functioning of the
internal combustion marine diesel engine.
Deflection measurements and checks have an important role in determining
the correct functioning of bearings that provide crankshaft lubrication, and thus
obtaining a maximum output by converting the fuel combustion energy into
mechanical work transmitted to the propulsion plant of the ship.
4. REFERENCES
[1]. MAN B&W Diesel 46-98 MC Edition 40F – Engine No. 16, 2006;
[2]. Ship‘s engine overhauls condition reports (on board official papers).
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EXHAUST VALVE WEARS OF MARINE DIESEL ENGINES
Eng. PhD. Candidate, NOVAC GEORGE,
―Mircea cel Batran‖ Naval Academy, Constanta,
Abstract: Exhaust valve overhauls and wear registrations reveal information about the quality and efficiency of
thermal processes occurring in the combustion chamber,the fuel quality, the compression pressure inside the
cylinder or combustion gas leakages. The measurements included in this study are targeting the bottom piece,
the spindle and the housing of the exhaust valves, for a period of four years and aims the MAN B&W 7K80 MC-
C marine diesel engine. By correlating with other associated wears for each cylinder, these studies can help
improve engine thermal efficiency of processes, and therefore marine diesel engine reliability.
Keywords: exhaust, valve, marine, engine, wears.
1. INTRODUCTION
This paper studies the exhaust valves wears, of internal combustion marine diesel engine
SULZER 7K80MC-C model and the tabulated measurements extends over a period of about
three years (2007-2010).
The condition and wearing of exhaust valves, provide important information about the
quality and efficiency of the combustion process inside the combustion chamber.
A study over a long period would highlight any operational problems of each cylinder,
but also can generate a range of values within the dimensional and functional characteristics
of the valve will fit, during normal functioning wear depending on the operation hours of each
valve.
2. EXHAUST VALVE
The exhaust valve is presented in Figure 2.1.
Each cylinder is equipped with an exhaust valve, mounted in the center of the cylinder
head. The bottom of the casing is provided with tapered seat for the valve head made from a
heat-treated material.
The valve spindle bore is also equipped with a reinforced duct and the whole assembly is
water cooled. At the top of the spindle valve, are mounted two pistons: an air piston used to
close the exhaust valve and a hydraulic piston used to open the exhaust valve.
The exhaust valve is operated by a cam on the camshaft via a hydraulic transmission.
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Figure 2.1. The exhaust valve:
1. lifting eye bolt; 2. screw; 3. lifting attachment; 4. gasket; 5. orifice; 6. disc; 7. oil cylinder; 8. stud; 9. nut; 10.
safety strap; 11. disc; 12. screw; 13. lock washer; 14. air cylinder; 15. valve housing; 16. cover; 17. gasket; 18.
surub; 19. valve spindle; 20. surub; 21. flange; 22. gasket; 23. stop screw; 24. O-ring; 25. valve seat; 26. O-
ring; 27. piston, complete; 28. piston; 29. sealing ring; 30. damper piston; 31. piston; 32. spring; 33. disc;
34. plug screw; 35. sealing ring; 36. sealing ring; 37. sealing ring; 38. spindle guide; 39. plug screw; 40.
gasket; 41. flange; 42. O-ring 43. screw; 44. cooling water connection; 45. gasket.
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3. MEASUREMENTS
Measurements included in this study were taken by the embarked crew on the
commercial ship during overhauls or other operations involving disassembling the exhaust
valve.
Measurements are targeting the following dimensional characteristics of the valve
bottom piece:
- deposits quantity in chamber, extented on circumference (in mm);
- angular position of maximum deposit (in degrees – Figure 3.1);
- maximum deposit thickness in duc (in mm).
For the valve spindle the following dimensional characteristics will be inspected (Figure 3.3):
- number of dent marks larger than 7 mm in diameter;
- stem diameter above sealing area - d0 (in mm);
- minimun stem diameter - dmin (in mm);
- wear of stem sealing ring (%).
For the valve housing the following dimensional characteristics will be inspected (Figure 3.2):
- minimum spindle guide diameter;
- maximum spindle guide diameter;
Below are tabulated (Table 2.1) the measurements performed on six of the seven
engine‘s valves, in order of their functioning hours [2].
Indications concerning the measurement areas are provided by the marine diesel engine
documentation manual [1], and are shown in figures 3.1, 3.2, 3.3 [2].
Fig. 3.1. Angular position of maximum deposit (0⁰ =
port side) [2]
Fig. 3.2. Measuring of spindle guide diameter [2]
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Table 2.1. Measurements results [2]
Valve no. 4 5 1 9 3 2
Valve hours: 10422 10620 17529 17529 18694 25547
Hours total: 29071 26252 17529 23036 29144 25547
Engine hours (total): 29249 26475 23359 24832 29144 29379
Valve dismount date:
09.0
8.2
010
11.0
3.2
010
09.0
8.2
008
09.1
2.2
007
01.0
8.2
010
21.0
8.2
010
Hours since last
overhaul: 18629 15632 16372 17569 18694 18563
Bottom piece
Amgular position of
max. deposit [0⁰]: 120 140 120 140 180 120
Spindle
No. of dent marks
larger than 7 mm: 3 3 5 4 6 5
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Valve no. 4 5 1 9 3 2
Valve hours: 10422 10620 17529 17529 18694 25547
Hours total: 29071 26475 23359 24832 29144 29379
Engine hours (total): 29249 26475 23359 24832 29144 29379
Valve dismount date:
09.0
8.2
010
11.0
3.2
010
09.0
8.2
008
09.1
2.2
007
01.0
8.2
010
21.0
8.2
010
Spindle
Housing
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Fig. 3.3. Stem diameter at sealing (dmin), and above sealing (d0) [1]
4. CONCLUSIONS
Traces of wear retrieved by these valve checks, reveals important information about the
quality and chemical content of the combustion fuel used, and other information related to the
combustion process, injection, combustion mixture formation or the gases exhaust efficiency.
So appropriate measures can be taken to minimize components wear of marine diesel
engine, to increase engine efficiency and reliability.
5. REFERENCES
[1]. MAN B&W Diesel 46-98 MC Edition 40F – Engine No. 16, 2006;
[2]. Ship‘s engine overhauls condition reports (on board official papers).
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GRAPHO-ANALYTICAL METHOD FOR CALCULLATING
IRREVERSIBILITY PROCESSES WITH FINITE SPEED
Prof.Eng. Traian FLOREA, PhD1,
Lecturer.mat. Ligia-Adriana SPORIȘ, PhD1,
Assist.prof.Eng. Corneliu MOROIANU, PhD1,
Eng. Traian Vasile FLOREA Ph.D2,
Prof.Eng. Anastase PRUIU, PhD1
1 “Mircea cel Batran” Naval Academy of Constanta, ROMANIA
2 A.P.M. Agigea of Constanta, ROMANIA
Abstract: A technique for calculating the efficiency and power of Stirling machines is presented. This
technique is based on the First Law of Thermodynamics for processes with finite Speed. A new and novel pv/pX
diagram is presented that shows the effects of pressure losses due to friction, finite speed and throttling
processes in the regenerator of the Stirling engine. The method used for the analysis of this irreversible cycle
with finite speed involves the direct integration of equations based on the First Law for processes with finite
speed to directly obtain the cycle efficiency and power. This technique is termed the Direct Method.
The results predicted by this analysis were in good agreement with the actual engine performance data of twelve
different Stirling engines over a range of output from economy to maximum power. This provides a solid
verification that this analysis can accurately predict actual Stirling engine performance, particularly with
regard to efficiently and output power.
Keywords: power, finire speed, analysis
1. INTRODUCTION
A new technique for calculating the efficiency and power of actual operating Stirling
machines is presented. This technique is based on the First Law of Thermodynamics for
processes with finite speed [1 – 14] and a new method for determining the imperfect
regeneration coefficient [15] . The analytical results depend upon inclusion of two
calibration coefficients (y and z) based on experimental data to accurately predict
performance. The thermal efficiency is expressed as a product of the Carnot cycle
efficiency and second law efficiency [21, 22, 31, 32] as has been suggested by Bejan [23]:
iP,irrev,IIX,irrev,II
T,irrev,IICC
lnT/TP
P31
ln1
T/T1X1
T
T1
T
T1
LS,H1,
i
1
S,HL
1
S,H
L
S,H
Lirrev,IICCSE
(1)
with XirrevIISHL TT ,,,
, /1
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3/11
The pressure losses and their effect on efficiency and power of the engine depend on the
piston speed and hence the speed of the engine.
The power output of the engine is:
SwmRTPower gHSESE 2/ln, (2)
The speed for maximum power may be determined since the power output is also a
function of the engine speed. Therefore the operating speed of a particular Stirling engine
can be selected for either maximum economy or for maximum power. Also, knowledge of
the nature of these losses can be effectively used in engine design.
A major loss in Stirling engines is caused by incomplete regeneration. This is expressed
by the coefficient of regenerative losses, X. An analysis for determining this loss has been
made by Petrescu et al. and Florea [15, 33]:
1
,21
,,ln/
/111
TcR
TTyXyX
v
SHL
XirrevII (3)
M
eMX
B
12
211 ,
M
eMX
B
12 (4-5)
RR
gvg
Cm
cmM
, ,
w
S
cm
hAMB
gvg
R ,
1 (6-7)
3/2576,0
576,0424,0
Pr1/4
11
/4395,0
R
mmPgLm
Ddb
TvTcwRTPh
(8)
where y is one of the adjusting coefficients of the method with the value of 0.72.
One objective of this paper is to make a more realistic analysis of the pressure losses
through use of a pv/pX diagram as will be described below and by Petrescu et al. [14].
Finally, the technique for calculating the efficiency and power of Stirling engines is
presented and the results predicted by this analysis are compared with performance data
taken on twelve actual Stirling engines over a range of operating conditions [24, 25, 26,
27, 28].
2. THE METHOD OF DETERMINING THE PERFORMANCE OF THE
STIRLING ENGINE
Computation of pressure losses, work losses, efficiency and power for the processes
shown on the new pv/pX diagrams [14, 15] are made using the first law of
thermodynamics for processes with finite speed [1-13]. The first law written to
specifically include these conditions is:
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159
dVP
Pf
P2
Pb
c
aw1PQdU
i,m
f
i,m
throtti,m
(9)
The irreversible work is:
dVP
P
P2
Pb
c
aw1PW
i,m
f
i,m
throtti,mirrev
(10)
when applied to processes with finite speed, as shown on the pv/pX diagram.
Computing and summing all pressure losses of the Stirling engine cycle presented above,
the term PiirrevII ,, from eq. (1) becomes [14, 15, 33]:
ln
4
10w045,094,03N
w
w5
ln
ln1w
w
1,
4
52
L,S
,
L,SPi,irrev,II
(11)
The heat input during the expansion process is also irreversible due to finite speed. In
order to take account of this influence, an calibration coefficient z is introduced:
lnmRTzQ g,H34 (12)
Finally, the real power output of the engine, eq. (2) becomes:
S2/wlnzmRTPower g,HSEirrev,SE (13)
where the value of z was evaluated at 0,8 by comparison with available experimental data
for twelve Stirling engines [24-28].
3. DISCUSSIONS
The variation of the coefficient of regenerative losses, X, with the piston speed for several
values of the gas average pressure is shown in Fig. 2. It is an example of the results
obtained from the sensitivity study [15] for X. It shows an important increase of the
regenerative losses with the gas average pressure. Then, the results of computations based
on this analysis are compared to performance data taken from a number of operating
Stirling engines in Figs. 3-5 and Table I. The high degree of correlation between the
analytic and the operational data shown in these figures indicate that the analysis is
capable of accurately predicting Stirling engine performance under a wide range of
conditions.
This capability should be of considerable value in Stirling engine design and in predicting
the performance of a particular Stirling engine over a range of operating speed.
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Table I. Comparison between analytical results
and actual engine performance data [24 - 29]
Fig.1. The pv/pX diagram for description of the
Stirling cycle processes
Sti
rlin
g
En
gin
e
Act
ual
Po
wer
[kW
]
Cal
cula
t
ed
Po
wer
[kW
]
Act
ual
Eff
icie
nc
y
Cal
cula
t
ed
Eff
icie
nc
y
NS-03M,
regime 1
(economy)
2.03 2.182 0.359 0.3392
NS-03M,
regime 1
(max.
power)
3.81 4.196 0.31 0.3297
NS-03T,
regime 1
(economy)
3.08 3.145 0.326 0.3189
NS-03T,
regime 1
(max.
power)
4.14 4.45 0.303 0.3096
NS-30A,
regime 1
(economy)
23.2 29.45 0.375 0.357
NS-30A,
regime 1
(max.
power)
30.4 33.82 0.33 0.3366
NS-30S,
regime 1
(economy)
30.9 33.78 0.372 0.366
NS-30S,
regime 1
(max.
power)
45.6 45.62 0.352 0.3526
STM4-120 25 26.36 0.4 0.4014
V-160 9 8.825 0.3 0.308
4-95 MKII 25 28.4 0.294 0.289
4 – 275 50 48.61 0.42 0.4119
GPU-3 3.96 4.16 0.127 0.1263
MP1002
CA
200
W
193.9
W 0.156 0.1536
Free Piston
Stirling
Engine
9 9.165 0.33 0.331
RE-1000 0.939 1.005 0.258 0.2285
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4. CONCLUSION
The objective of this approach was to closely simulate the operation of actual
Stirling engines without losing insight to the mechanisms that generate the
irreversibilities. Pressure and work losses generated by finite speed of the actual processes
were computed as were the power and efficiency of engines. The first law of
thermodynamics for processes with finite speed was used to compute the power losses
generated by the pressure losses. The analysis presented was applied to specific operating
Stirling cycle engines and results were compared to the measured performance of the
engines. The strong correlation between the analytical results and actual engine
performance data indicates that the Direct Method of using the First Law for Finite Speed
is a valid method of analysis for irreversible cycles.
Fig. 2. Coefficient of regenerative losses Fig. 3. Comparison of the analysis results
versus the piston speed for several values with actual performance data
of the average pressure of the working gas for the NS-30S Stirling engine
(DC = 60 mm, b/d = 1.5, τ = 2, N = 700)
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Fig. 4. Comparison of the analysis results Fig. 5. Comparison of the analysis
with actual performance data for the results with actual performance
4-275 Stirling engine data for the Free Piston Stirling engine
REFERENCES:
[1] Stoicescu, L., Petrescu, S., 1964a, The First Law of Thermodynamics for Processes
with Finite Speed, in Closed Systems, (German language), Bulletin of Polytechnic Institute
of Bucharest, Vol. XXVI, No. 5;
[2] Stoicescu, L., Petrescu, S., 1964b, Thermodynamic Processes Developing with
Constant Finite Speed, (German language), Bulletin of Polytechnic Institute of Bucharest,
Vol. XXVII, No. 6;
[3] Stoicescu, L., Petrescu, S., 1965a, Thermodynamic Processes Developing with
Variable Finite Speed, (German language), Bulletin of Polytechnic Institute of Bucharest,
Vol. XXVII, No. 1;
[4] Stoicescu, L., Petrescu, S., 1965b, Experimental Verification of the Processes with
Finite Speed, (German language), Bulletin of Polytechnic Institute of Bucharest, Vol.
XXVII, No. 2;
[5] Stoicescu, L., Petrescu, S., 1965c, Cycles with Finite Speed, (German language),
Bulletin of Polytechnic Institute of Bucharest, Vol. XXVII, No. 2;
[6] Petrescu, S., 1969a, Contribution to the Study of Interactions and Processes of non-
equilibrium in Thermal Machines, Ph.D. Thesis, Polytechnic Institute of Bucharest,
Romania;
[7] Petrescu, S., 1969b, The Determination of the Expression of the Work in a Process
with Finite Speed using the Phenomenological Thermodynamics of Reversible Processes,
Studii şi Cercetări de Energetică şi electrotehnică, Romanian Academy, Vol. 19, No. 2;
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[8] Petrescu, S., 1971, Kinetically Considerations Regarding the Pressure on a Piston
Moving with Finite Speed, Studii şi Cercetări de Energetică şi Electrotehnică, Romanian
Academy, Vol. 1, No. 11;
[9] Petrescu, S., 1974, Experimental Study of the Gas-Piston Interaction with Finite
Speed in the Case of an Open System, Studii şi cercetări de Mecanică Aplicată, Romanian
Academy, Vol. 31, No. 5;
[10] Petrescu, S., 1991, Lectures on New Sources of Energy, Helsinki University of
Technology, Finland;
[11] Petrescu, S., Stanescu, G., Iordache, R., Dobrovicescu, A., 1992, The First Law of
Thermodynamics for Closed Systems, Considering the Irreversibility Generated by the
Friction Piston-Cylinder, the Throttling of the Working Medium and Finite Speed of the
Mechanical Interaction, Proc. of the Inter. Conf. on Efficiency, Costs, Optimization and
Simulation of Energy Systems, ECOS‘92, Zaragoza, Spain, edited by A. Valero and G.
Tsatsaronis, ASME, pp. 33-39;
[12] Petrescu, S., Harman, C., Florea, T., 1994, The Connection between the First and
Second Law of Thermodynamics for Processes with Finite Speed. A Direct Method for
Approaching and Optimization of Irreversible Processes, Journal of The Heat Transfer
Society of Japan, Vol. 33, No. 128;
[13] Petrescu, S., Zaiser, J., Valeria Petrescu, Florea, T., 1996, Lectures on Advanced
Energy Conversion, Bucknell University, Lewisburg, PA, USA;
[14] Petrescu, S., Harman, Florea, T., C., Costea, M., 2000a, Determination of the
Pressure Losses in a Stirling Cycle through Use of a PV/Px Diagram, paper accepted to
the Inter. Conf. on Efficiency, Costs, Optimization and Simulation of Energy Systems,
ECOS’2000, Entschede, Netherlands, July 5-7;
[15] Petrescu, S., Harman, C., Florea, T., Costea, M., 2000b, A Method for Calculating
the Coefficient for the Regenerative Losses in Stirling Machines, Proc. of 5th
European
Stirling Forum 2000, Ösnabruck, Germany, February 22-24;
[16] Petrescu, S., Stanescu, G., 1993, A Direct Method of the Study of Irreversible
Processes which are Developing with Finite Speed in Closed Systems, (Romanian
Language), Termotehnica, No. 1, Editura Tehnica, Bucharest;
[17] Petrescu, S., Stanescu, G., Florea, T., Costea, M., 1993a, The study of the
optimisation of the Carnot cycle which develops with finite speed, Proc. of the Inter. Conf.
on Energy Systems and Ecology, Cracow, Poland, edited by J. Szargut, Z. Kolenda, G.
Tsatsaronis andA. Ziebik, pp. 269-277;
[18] Petrescu, S., Stanescu, G., Costea, M., Florea, T., 1993b, A Direct Method for the
Optimization of Irreversible Cycles using a New Expression for the First Law of
Thermodynamics for Processes with Finite Speed, Proc. of the 1st Conference on Energy
ITEC‘93, Marrakesh, Morocco, pp. 650-653;
[19] Petrescu, S., Petrescu, V., Florea, T., Stanescu, G., Costea, M., 1993c, A
Comparison between Optimization of Thermal Machines and Fuel Cells based on New
Expression of the First Law of Thermodynamics for Processes with Finite Speed, Proc. of
the 1st Conference on Energy ITEC‘93, Marrakesh, Morocco, pp. 654-657;
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[20] Petrescu, S., Harman, C., Bejan, A., Florea, T., 1994, The Carnot Cycle with
External and Internal Irreversibility, Proc. of FLOWERS’94 Symposium, Energy for The
21st Century: Conversion, Utilization and Enviromental Quality, Florence, Italy;
[21] Petrescu, S., Harman, C., 1996, Stirling Cycle Optimization Including the Effects of
Finite Speed Operation, Proc. of the Inter. Conf. on Efficiency, Costs, Optimization
Simulation and Enviromental Aspects of Energy Systems, ECOS‘96, Stockolm, Sweden,
edited by P. Alvfors, L. Edensten, G. Svedberg and J. Yan, pp. 167-173;
[22] Costea, M., Petrescu, S., Harman, C., Florea, T., 1998, The Effect of
Irreversibility’s on Solar Stirling Engine Cycle Performance, Proc. of the Inter. Conf. on
Efficiency, Costs, Optimization Simulation and Environmental Aspects of Energy Systems,
ECOS‘98, Nancy, France, edited by A. Bejan, M. Feidt, M.J. Moran and G. Tsatsaronis,
Nancy, France p.821-828;
[23] Bejan, A., 1988, Advanced Engineering Thermodynamics, Wiley, New York;
[24] Fujii, I., 1990, From Solar Energy to Mechanical Power, Harwood Academic
Publishers, New York;
[25] Allen, D.I., Tomazic, W.A., 1987, ―ot Piston Ring Tests, NASA TM-100256;
[26] Geng, S.M., 1987, Calibration and Comparison of the NASA Lewis Free-Piston
Stirling Engine Model Prediction with RE-1000 Test Data, NASA TM-89853;
[27] Stine, W.B., Diver, R.B., 1994, A Compendium of Solar Dish / Stirling Technology,
Sandia Laboratories Report;
[28] Farell, R.A. et al., 1988, Automotive Stirling Engine Development Program, NASA
CR-180839;
[29] Organ, J.A., 1992, Thermodynamics and Gas Dynamics of Stirling Cycle Machine,
Cambridge University Press, Cambridge;
[30] Walker, G., 1983, Cry coolers – Part 1: Fundamentals, Plenum Press, New York;
[31] Costea, M., Petrescu, S., Harman, C., 1999, The Effect of Irreversibility on Solar
Stirling Engines Cycle Performance, Energy Conversion & Management, Vol. 40, pp.
1723-1731;
[32] Costea, M., 1997, Improvement of heat exchangers performance in view of the
thermodynamic optimisation of Stirling machine; Unsteady-state heat transfer in porous
media, Ph.D. Thesis, P. U. Bucharest & U.H.P. Nancy 1;
[33] Florea, T., 1999, Grapho-Analytical Method for the Study of Irreversible Processes
in Stirling Engines, Ph.D. Thesis, Polytechnic University of Bucharest;
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THE COEFFICIENT OF REGENERATIVE LOSSES
IN STIRLING MACHINES
Prof.Eng. Traian FLOREA, PhD1,
Assist.prof.Eng. Corneliu MOROIANU, PhD1,
Eng. Traian Vasile FLOREA Ph.D2,
Lecturer.mat. Ligia Adriana SPORIȘ, PhD1,
Prof.Eng. Anastase PRUIU, PhD1
1 “Mircea cel Batran” Naval Academy of Constanta, ROMANIA
2 A.P.M. Agigea of Constanta, ROMANIA
Abstract: The coefficient of regenerative losses, X, is the term that includes all of the losses due to heat transfer
in the regenerator. This parameter in turn depends on a large number of variables. Among these are piston
speed, cylinder dimensions, regenerator dimensions, materials internal to the regenerator, gas proprieties and
the range of operating conditions. These variables are employed in a new technique for calculating the
parameter X. The computed values of X were compared with estimated values of X based on experimental data
available in the literature. Agreement between these values was found to be excellent, indicating that the
technique for calculating X is accurate. This predictive capability should be a powerful tool in the design of
effective Stirling machines.
Keywords: irreversibility, losses, regeneration, Stirling, efficiency.
1. INTRODUCTION
This paper presents a new technique for calculating the efficiency and power of actual
operating Stirling machines. This technique is based on the First Law of Thermodynamics for
processes with finite speed (1-13) and is used in conjunction with a new and novel pv / pX
diagram (13,14) and a new method for determining the imperfect regeneration coefficient.
One of the objectives of this paper is to develop the method for determining the
imperfect regeneration coefficient X, and to use it for calculating the efficiency and the power
output of the Stirling engine.
Initially, the thermal efficiency is written as a function of three basis parameters.
,PiT,irrev,IICCIIirrevSESE (1)
where
S,H0CC T/T1 (2)
is the Efficiency of a Carnot cycle operating between the same temperature limits as the
Stirling engine.
The second law efficiency
S,HOT,irrev,II T/T1/1 (3)
takes into account the irreversibility due to the temperature difference between the heat source
and the gas in the engine. The second law efficiency
1
n
S,HO
IIirrevXl1-
T/T1X1
(4)
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takes into account the loses in the regenerator due to incomplete regeneration through use of
the coefficient of losses, X.
The second law efficiency 1
n0S,H11,
ii
iIIirrevXlT/TVP
VP1P
(5)
with XirrevIISHTT ,,,0 /1, takes into account the irreversibility losses due to the
pressure drop caused by the finite piston speed. The power output of the engine is
S2/wlnmRTPower g,HSESE
(6)
where is the compression ratio, w is piston speed, S is the stroke of the piston, and is the
specific heat ratio.
A major loss in Stirling engines is caused by incomplete regeneration. An analysis for
determining this loss is the primary objective of this paper. A second objective is to make a
more realistic analysis of the pressure losses through use of a pv / pX diagram as will be
described below (for details, see 11). Finally, the power and efficiency, as determined by
this analysis which involves the computation of X, is compared with performance data taken
on twelve actual Stirling engines over a range of operating conditions 7-17.
2. DETERMINATION OF LOSSES, EFFICIENCY AND POWER OF THE STIRLING
ENGINE BASED ON AN INTUITIVE PV / PX DIAGRAM FOR DESCRIPTION OF
THE CYCLE PROCESSES
Computation of pressure losses, work losses, efficiency and power for the processes
shown on the new pv / pX diagrams 14, 15 are made using the first law of thermodynamics
for processes with finite speed 1-14. The first law written to specifically include these
conditions is:
dVPPfPPbcawPQdU imfimthrottim ,,, /2//1
(7)
The irreversible work then is:
dVPPP
Pb
c
awPW imf
im
throttimirrev
,
,, /
21 (8)
when applied to processes with finite speed.
The work expression for the finite speed isothermal irreversible compression process 12
(Fig.1) can be integrated using the Direct Method 5,6,10,12-17 to obtain:
2
1
dVi,cpr,mi,cpr,mf
i,cpr,m
thrott2
1
i,mirrev,12 PP/PP2
Pb
c
awdVPW
(9)
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167
Fig. 1: The new pv/pX diagram of the ideal Stirling cycle
The work losses may be calculated for the compression process 12 by using eq. (9), 15:
12fthrott
i,cpr,mrev,12irrev,12losses,12 VVP2
PbP
c
awWWW
(10)
Computing and summing the losses due to finite speed of the pistons, throttling of the
gas through the regenerator 12,16, and mechanical friction 4,7 for the whole Stirling
engine cycle, and introducing them in eq. (5), it becomes 14:
(11)
The heat input during the expansion process is also irreversible due to finite speed. In order to
take account of this influence, an adjusting parameter z is introduced:
.lnmRTzQ g,H34 (12)
Finally, the real power output of the engine, eq.(6) becomes: .S2/wlnzmRTPower g,HSEirrev,SE (13)
ln/4
w045,094,03
w
wN5ln1
w
w1 ,
4
2
L,SL,SP,irrev,II i
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Where the value of z was evaluated at 0,8 by comparison with available experimental
data for twelve Stirling engines 12-17.
3. A METHOD FOR CALCULATING THE COEFFICIENT OF REGENERATIVE
LOSSES, X, IN STIRLING ENGINE
The analysis resulted in differential equations that were then integrated. This integration
is based on either a lump analysis, which gives pessimistic results, X1, or on a linear
distribution of the temperature in the regenerator matrix and gas (see fig. 2), which gives
optimistic results, X2.
Fig. 2: Gas and matrix temperature distribution in the regenerator
The resulting expressions for are:
.
1;
12
2121
M
eMX
M
eMX
BB
(14)
where:
.1
;
,
,
w
S
cm
hAMB
cm
cmM
gvg
R
RR
gvg
(15)
3/2576,0R
576,0mmP
424,0g
L
m
PrD1d/b4
11
TvTcwRT
P4395,0
h
(16)
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with mg is the mass of the passing through the regenerator, mR is the mass of the screens of the
regenerator, AR is the surface area of the wires in the regenerator, v is the viscosity of the
working gas, and h is the convective heat transfer coefficient in the regenerator (based on
correlation given in [17]).
The sensitivity of X1 and X2 to changes in operating variables such as the piston speed
was determined. The computed values of X1 and X2 were compared with values of X
determined from experimental data available in the literature [12-17]. The results based on the
theory were found to predict the values from experimental data by using the following
equation:
,1 21 XyyXX (17)
where y is an adjusting parameter with the value of 0,72.
The loss due to incomplete regeneration as determined through use of eq. (17) is the
final loss to be considered in the analysis. The second law efficiency due to irreversibility‘s
from incomplete regeneration is:
1021,, ln///128,072,01
TcRTTXX vHSXirrevII
(18)
In Fig. 3-5 the variation of the coefficient of regenerative losses with the piston speed is
represented for several values of the analysis parameters (d, S, porosity), and Fig. 6 illustrates
the convective heat transfer coefficient dependence upon the piston speed.
Fig. 3: Coefficient of regenerative losses Fig. 4: Coefficient of regenerative losses
versus the piston speed for several values of versus the piston speed for several value of the wire
diameter (DC = 60 mm, DR = 60 mm, the piston stoke (DC = 60 mm, DR = 50 mm,
Pm = 50 bar, S = 30 mm, N = 700, τ = 2) Pm = 50 bar, d = 0.05 mm, N = 700, τ = 2)
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Fig. 5: Coefficient of regenerative losses Fig. 6: Convective heat transfer coefficient in
versus the piston speed for several values the regenerator versus the piston speed for
of matrix porosity (DC = 60 mm, DR = 50 mm, several values of the average pressure
Pm = 50 bar, S = 30 mm, d = 0.05 mm, of the working gas (DR=50,,,b/d =1.5, η = 2)
N = 700, η = 2)
4. COMPARISON OF ANALYTIC RESULTS WITH THE OPERATING
PERFORMANCE OF ACTUAL STIRLING ENGINES
The results of computations of efficiency and power output based on this analysis are
compared to performance data taken from twelve operating Stirling engines in Figs. 7-8 and
in Table I.
Fig. 7: Comparison of the analysis results
with actual performance data for the
STM4-120 Stirling engine [27]
Fig. 8: Comparison of the analysis results with actual
performance data for the V-160 Stirling engine [27]
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Table 1: Comparison between the analytical results and actual engine performance data [24-29]
Stirling Engine Actual Power
[kW]
Calculated
Power [kW]
Actual
Efficiency
Calculated
Efficiency
NS-03M, regime 1
(economy) 2.03 2.182 0.359 0.3392
NS-03M, regime 1 (max.
power) 3.81 4.196 0.31 0.3297
NS-03T, regime 1
(economy) 3.08 3.145 0.326 0.3189
NS-03T, regime 1 (max.
power) 4.14 4.45 0.303 0.3096
NS-30A, regime 1
(economy) 23.2 29.45 0.375 0.357
NS-30A, regime 1 (max.
power) 30.4 33.82 0.33 0.3366
NS-30S, regime 1
(economy) 30.9 33.78 0.372 0.366
NS-30S, regime 1 (max.
power) 45.6 45.62 0.352 0.3526
STM4-120 25 26.36 0.4 0.4014
V-160 9 8.825 0.3 0.308
4-95 MKII 25 28.4 0.294 0.289
4 – 275 50 48.61 0.42 0.4119
GPU-3 3.96 4.16 0.127 0.1263
MP1002 CA 200W 193.9W 0.156 0.1536
Free Piston Stirling Engine 9 9.165 0.33 0.331
RE-1000 0.939 1.005 0.258 0.2285
This figures show that there is high degree of correlation between this analysis and the
operational data. This indicates that this analysis can be used to accurately calculate X and of
other losses. Therefore, this analysis can be used to accurately predicting Stirling engine
performance under a wide range of conditions. This capability should be of considerable
value in Stirling engine design and in the prediction the performance of a particular Stirling
engine over a range of operating speed.
The strong correlation between the analytical results and actual engine performance data
also indicates that the Direct Method of using the first law for processes with finite speed is a
valid method of analysis for irreversible cycles.
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REFERENCES [1] Petrescu Stoian, Florea Traian, Harman Charles, Costea Monica: A Method for
Calculating the Coefficient for the Regenerative Losses in Stirling Machines, European
Stirling Forum 2000, Osnabrück, Germany, February 22-24, 2000, pag. 121-129;
[2] Petrescu Stoian, Florea Traian, Costea Monica, Harman Charles: Application of the
Direct method to Irreversible Stirling cycles with Finite speed, International Journal of
Energy Research, No.26, pag. 589-609,, May, 27, 2002, edited by John Wiley & Sons,
Ltd., USA;
[3] Florea Traian, Petrescu Stoian, Costea Monica, Feidt Michel: La methode directe
utilisée dans la thermodynamique a vitesse finie pour l’optimisation des machines
thermique, Energie, environnement, economie et thermodynamique, Université
―Politehnica‖ Bucarest, avril 2002, pag, 72-79, ISBN 973-8165-22-9;
[4] Petrescu Stoian, Florea Traian, Feidt Michel, Harman Charles, Costea Monica:
Optimization of the Irreversible Carnot Cycle Engine for Maximum Efficiency and
Maximum Power through Use of Finite Speed Thermodynamic Analysis, Int. ECOS‘2002
Conference, G. Tsatsaronis, M. Moran, F. Cziesla and T. Bruckner, eds., Berlin, Germany,
Vol. II pp.1361-1368;
[5] Petrescu Stoian, Florea Traian, Costea Monica, Petre Camelia, Feidt Michel: A
scheme of Computation, Analysis, Design and Optimization of Solar Stirling Engines,
ECOS-2003, Copenhagen,Denmark, June 30-July 2, 2003, Volume I, Editors: Niels
Houbac, Brian Elmegaard, Bjorn Qvale, Michael J. Moran, pag.1255- 1262,ISBN
9015763461;
[6] Florea Traian, Dragalina Alexandru, Costiniuc Corneliu, Florea Elisabeta, Florea
Traian Vasile: A Method for Calculating of the Coefficient for the Regenerative Losses in
Stirling Machines, COMEFIM‘8, The 8 th International Conference on Mechatronics and
Precision Engineering, Technical University of Cluj Napoca, June 8 th - 10 th , 2006,
pag.747-754, ISBN 1221-5872;
[7] Florea Traian, Dragalina Alexandru, Costiniuc Corneliu, Florea Elisabeta, Florea
Traian Vasile: A Method for Determinig the Performances of Stirling Machines Based on
the First Law for Processes with Finite Speed and using a pv/pX Diagram, COMEFIM‘8,
The 8 th International Conference on Mechatronics and Precision Engineering, Technical
University of Cluj Napoca, June 8 th - 10 th , 2006, pag.755-764, ISBN 1221-5872;
[8] Alexandru DRAGALINA, Traian FLOREA, Corneliu COSTINIUC, Constantin
DANCU: Control Optimisation and Load Prediction for Marine Diesel Engines Using a
Mean Value Simulation Model, Conferinta internationala NAV-MAR-EDU 2007,
Constanta, 15-17 noiembrie 2007, ISBN 978-973-8303-84-3;
[9] Florea Traian, Dragalina Alexandru, Florea Traian Vasile, Pruiu Anastase: The study
of the irreversibility of the operational process of the external combustion engines with
heat regenerators and increase of power and output for the internal combustion engines
using the experimental and graphoanalytical methods, Proceedings of the internationally
attended national conference on thermodynamics, Brasov, Romania, 21 – 22 May 2009,
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173
Vol II, Series I, ISSN 2065-2119, Special Issue No.1 Vol.1 2009,pag. 347- 354, ISBN 978-
973-598-521-9;
[10] Florea Traian: Regenerarea cãldurii în masinile termice, Editura Leda&Muntenia,
Constanţa, 2001, 128 pag., ISBN 973-9286-96-8 şi ISBN 973-8082-51-X;
[11] Florea Traian: Regimurile optime de putere maximã şi grafice globale, sintetice pentru
optimizarea motoarelor cu ardere externã Stirling, Editura Academiei Navale, Constanţa,
2000, 176 pag., ISBN 973-99564-6-7;
[12] Florea Traian, Petrescu Stoian, Florea Elisabeta: Scheme de calcul pentru studiul
ireversibilitãţii proceselor funcţionale ale motoarelor cu ardere externã Stirling, Editura
Leda&Muntenia, Constanţa, 2000, 147 pag., ISBN 973-8082-07-2 şi ISBN 973-9286-55-0;
[13] Petrescu Stoian, Florea Traian, Harman Charles, Costea Monica: Advanced Energy
Conversion - volume I,(ed.rev.), Bucknell University, Lewisburg PA 17837, USA, January
2005, 469 pag., MECH 422/622;
[14] Petrescu Stoian, Florea Traian, Zaiser James, Harman Charles, Petrescu Valeria,
Costea Monica,Petre Camelia, Florea Traian Vasile: Advanced Energy Conversion -
volume II, (ed.rev.), Bucknell University, Lewisburg PA 17837, USA, February 2005, 497
pag., MECH 422/622;
[15] Petrescu Stoian, Florea Traian, Costea Monica,Florea Elisabeta, Florea Traian
Vasile: Thermodynamics and Heat Transfer, 769 pag., ENGR 204, Bucknell University,
Lewisburg PA 17837, USA, January 2006;
[16] Petrescu S., Harman C.: Stirling Cicle Optimization Including the Effects of Finite
Speed Operation, Proc. Of the Inter. Conf. On Efficiency, Costs, Optimization Simulation
and Environmental Aspects of Energy Systems, ECOS‘96, Stockholm, Sweden, edited by
P. Alvfors, L. Eidensten, G. Svedberg and J. Yan, 167-173, 1996;
[17] Organ J. A.: Thermodynamics and Gas Dynamics of Stirling Cycle Machine,
Cambridge University Press, Cambridge, 1992;
[18] Traian Florea, Anastase Pruiu, Marian Ristea, Nicu Olaru, George Dogarescu,
Traian Vasile Florea, February, 27, 2012 - Calculus and materials for Stirling Engine`s
Bolter and Regenerator , Published by WSEAS Press , pag. 183-186, Cambridge, UK.,
ISBN:978-1-61804-071-8;
[19] Florea Traian, Dragalina Alexandru, Florea Traian Vasile, Pruiu Anastase, May
2009, The study of the irreversibility of the operational process of the external combustion
engines with heat regenerators and increase of power and output for the internal
combustion engines using the experimental and grapho-analytical methods, Bulletin of the
Transilvania University of Brasov, Vol II, Series I, ISSN 2065-2119, Special Issue No.1
Vol.1 2009,pag. 347- 354, ISBN 978-973-598-521-9;
[20] Florea Traian, Petrescu Stoian, Florea Traian Vasile, Dancu Constantin, Pruiu
Anastase, The study of the irreversibility of the operational process of the external
combustion engines with heat regenerators, National Conference of Thermodynamics with
International Participation NACOT 2013 ―Present and Future in Thermodynamics‖,
Editura AGIR, Constanţa, 2013,ISSN-L 1222-4057, ISSN 2247-1871 Online.
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GAUSSIAN MODEL
Assistant Professor doctor ADINA TĂTAR,
―Constantin Brâncuşi‖ University of Tg-Jiu
Abstract: In this work programme shall be used in the mathematical modeling of the dynamics of atmospheric
pollutants.This is important in assessing the impact of pollutants on air.
Mathematical relationships used are presented within this model, the model structure, required
parameters in solving problems.
Key words:gaussian model, pollutants, mathematical relation, parameters, mathematical modeling
1.INTRODUCTION To assess the impact of pollutants on air and need to be fitted to a NOx installation of
desulphurisation plants, dusting, and were taken into account more scenarios and the impact
has been made using dispersion modeling in ambient air.
For the mathematical modeling of the dynamics of atmospheric pollutants (SO2, NO2
and PM10), resulting from the work of C.T.E. i used was the software OML- Multi.
OML Multi is a model of dispersion of pollutants from local scale developed by the
National Institute of Environmental Research-NERI (Denmark).
In the 1990s this model became operational, being widely used in Denmark for the
practical applications for predicting air quality in different areas, and can be run both in urban
areas and in rural areas up to a distance of 30 miles.
Throughout the 1990s the model has been improved both in terms of theory, but also
in terms of the presentation and view the results.
OML - Multi is a multisource gaussian-type model, designed for inclusion in his
theory of the main physical phenomena governing the dispersion of pollutants into the
atmosphere from industrial sources or other sources.
The pattern can include point sources and area sources. In this model were pursued
and better behavior of the model in most conditions possible, avoiding atmospheric
discontinuităţilor in describing the phenomenon of dispersion, the possibility of its application
to operational purposes. The final version OML-Multi is the result of a long process.
From its first validation by experiments, many new phenomena that have been
introduced over the years have imposed new and new tests and experimental validation.
2. THE STRUCTURE OF THE PROGRAMME
Structurally, OML- Multi consists of:
- Pre-processor-computational method of meteorological parameters needed for
modeling physical processes of dispersion, from the meteorological measurements.
Pre-processor weather requires as input meteorological measurements hourly and two
vertical temperature profiles carried out daily by radiosondaj;
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- The dispersion model itself-computational method of estimation of concentrations in
a system of predefined receptors based on physical parameters and other data entry required
(emission data, information about land, etc.).
Ground-level concentration is described by Gaussian form of the pollutant plume
relationship date 1:
2
2
2
2
2exp
2exp0,,
z
d
yzy
hy
u
Qyxc
(1)
-Q is the intensity of the source (the mass);
-hef is the actual height of the plume of pollutants;
- ζz is dispersion parameter vertically.
The reflection of the lower and upper limit of the layer is made by the method of the
source image, but the above relationship, for simplicity, has not included a detailed
description of all terms exponenţiali needed contributions from image sources.
If the vertical dispersion ζz exceeds 1.2 times the height value of the mixture, then the
model generates a uniform concentration distribution in the vertical plane of the mixing layer.
The OML, dispersion parameters are correlated directly with the physical parameters
of the boundary layer, describing the turbulence of the atmosphere, unlike most classical
models in which the dispersion parameters are calculated by method of Pasquill-Gifford-
Turner. Due to the variation of the height of the unrest, to amend the dispersion parameters
can easily approach makes it possible for sources with different heights, in addition, the
dispersion parameters are calculated by means of the composition of all the contributions
coming from the turbulence associated with each physical phenomenon that it generates.
As a general rule, in the case of any ζ (ζz and ζy) it breaks down as follows:
22
int
22
buildingernturb (2)
ζturb-represents the dispersion due to atmospheric turbulence;
-ζintern is the contribution resulting from the phenomenon of mixing up of ambient air
pollutant. This phenomenon is associated with scattering feathers with large carrying
capacity;
-ζbuilding is the turbulence generated by the presence of buildings near the sources of the
money.
On the basis of the same principle of decomposition based on statistical theory of
diffusion due to atmospheric turbulence, you can write:
222
convmechturb (3)
- ζturb andζconvdispersion parameters are assigned to those two processes generating
atmospheric turbulence: mechanical and convective processes.
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- OML implements separately these 5 processes generating turbulence and
differentiates the feathers of pollutant in published and non-published.
- Preprocesorul requires that the meteorological input data hourly weather
measurements and two vertical temperature profiles carried out daily by radiosondaj.
- Output Data are turbulence parameters: sensible heat flux (H), Monin Obukhov
length (L), speed of friction (uz) and the mixing height (day).
The meteorological OML was thoroughly described in numerous publications
(Berkowitz and Prahm-1982, Olesen and Brown 1992, Olesen and others 1992).
OML includes a procedure for modelling the dispersion of pollutants from sources
non-damp surface, rectangular area sources for which the ratio between length and width may
not exceed 10 (L/l < 10), and the length varies between 10 m and 1000 m.
Procedure of calculation is based on the assimilation of surface source with a finite
number of linear sources and contributions from these sources are integrated.
For the calculation of the concentration on the direction of the wind (downwind)
integral analytically using the function resolves the error.
Integral lateral dispersion resolves numeric using numerical techniques proposed by
Romberg. In the case of placing a receiver inside source, concentration on the propagation
direction of the wind shall take into account only the corresponding segment stretches from
the border's first direction of propagation up to the receiver.
In the case of placing the receiver at great distance from the source, it is treated as a
simple linear source. OML uses two distinct values of wind speed:
-Uhs-wind velocity at emission level, used for the calculation of supraînălţării and of
the effects of building;
-um-mediated vertical wind speed used in the calculation of sigmelor and the estimated
time of transport.
Dependence on height windspeed is given by the theory of similarity (Monin and
Obukhov, 1954):
L
z
L
z
z
zz
k
uzu mm
0
0
0ln (4)
Similarity functions used are those proposed by Businger (1971).
Consider the existence of a gradient OML wind on height between the ground surface
and the time of length L.
Input data are:
-hourly weather data, generated in a specific format in preprocesorului weather
rolling;
-data relating to the physical parameters of the sources: sources (point sources-basket)
or geometric dimensions-length-width-height, if sources surface;
-emission data: mass flow, exhaust temperatures;
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-stroke variation: factors that describe the variation in time of the emissions for each
type of source entered in the model: punctual or surface;
-data related to the network of receptors: receptor coordinates definition in a spherical
coordinate system or rectangular.
The output fields are represented by nodes in the network's strengths of receptors.
OML multi generates in all nodes of the network, the average hourly concentrations of
receptors, as well as monthly, annual average, percentile and other values important in
statistical assessment of air quality.
Weather data were processed using pre-packaged CPU Model meteorological OML
have a Multi format recording annual hourly and wind measurements at a resolution of one
degree.
3.CONCLUSIONS
Graphical representation of the results of mathematical modeling of dispersion of the
pollutants of interest shall be made on topographic maps using georeferenţiate software
Global Mapper 11.
The calculations shall be carried out in a grid with the specified size for the main
features of pollutants emitted by stationary sources directed the burning C.T.E.
The ranges of mediation used for mathematical modeling are those corresponding to
the period of mediation, to be used for each pollutant according to the order MAPM nr.
592/2002.
The software allows modelling of the dispersion on these intervals of mediation.
You can also achieve dispersion maps.
Weather data were processed using pre-packaged CPU Model meteorological OML
Multi have a format recording annual hourly and wind measurements at a resolution of one
degree.
BIBLIOGRAPHY [1] INSEMEX, Computer modeling of the dispersion of dust from dust and gas stations for
fans of the Jiu Valley mining operations, Petroșani, 2010
[2] Order MAPM nr.592/25.06.2002 to approve the norm on the limit values, threshold values
and evaluation methods of sulfur dioxide, nitrogen dioxide and oxides of nitrogen, particulate
matter PM10 and PM2.5, lead, benzene, carbon monoxide and ozone in ambient air ,
published in Official Monitor no. 765/21.10.2002
[3] SC.EPC CONSULTANŢĂ DE MEDIU SRL, Study on dispersion of pollutants emissions
of sulfur dioxide, nitrogen oxides and particulates (PM10) emissions from stationary sources
of SC Complex Energetic Rovinari SA, Bucharest, 2010
[4] S.C. ISPE SA , Study Environmental Impact Assessment, Bucharest, 2008
[5] STAS 11103/78Air purity. Determination of Suspended Powder
[6] Tatar Adina -Milena, Modelling,Dynamic processes in the atmosphere in 2010, Report no.
3, University of Petrosani, 2010
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178
THE DETERMINATION OF THEORETICAL COMBUSTION
TEMPERATURE OF HEAVY FUELS CONSIDERING THE
DISSOCIATION OF WATER VAPOURS
FROM THE BURNING GASES
Ph. D
1. Corneliu MOROIANU, Email address: [email protected]
Ph. D1. Ligia Adriana SPORIȘ, Email address: [email protected]
Ph. D1. Traian FLOREA, Email address: [email protected]
1The Naval Academy ―Mircea cel Bătrân‖ Constanța
Abstract: Some components of the burning gases dissociate at high temperatures in the burning space of the
combustion engines. Due to the dissociation of water vapours, the temperature of fuel components from the
burning gases may have higher values. In contact with the surrounding cold surfaces, a heat exchange takes
place inducing the fall of gas temperature so that, the balances of dissociation reactions move to the right,
leading to the reduction of fuel components produced as a result of this phenomenon. This paper gives us an
analytical method for determination the theoretical combustion temperature of heavy fuels considering the
dissociation of water vapours.
Key words: fuel combustion, analytical modelling, dissociation, water vapours.
INTRODUCTION
Some components of the burning gases dissociate at high temperatures in the burning
space of the combustion engines, beginning with 1500 0C. By ―dissociation‖ we mean the
reversible splitting of substance molecules into simple molecules, atoms, radicals or ions, as a
result of chemical covalent bond breaking under the action of outside heat power.
Chapter 1. We‘ll take into account the dissociation of water vapours and carbon dioxide
according to the following reactions:
2H2 + O2 2H2O (1)
2CO + O2 2CO2 (2)
The chemical processes in the furnace are simultaneously developed in both
directions: the direct reaction, during which the initial substances are changed into final
products and the counter-reaction (back reaction\ feedback), of dissociation, by which the
reaction products are changed again into initial products.
The development rates of the two opposite reactions depend on the concentration of
the participant substances. At the beginning of the process, when the concentration of the
initial substances is much higher than the final ones, the direct reaction is developed much
faster than the counter-reaction.
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According as the process is developed, the concentration of the initial substances is
reduced but the concentration of the reaction products is increased, having as a result the
decrease of direct reaction rate, of forming the final substances and the acceleration of the
counter-reactions, of restoring the initial substances. It gets to the chemical balance in which
the rates of the two reactions, of forming and splitting (decomposing) of the reaction products,
are equal.
The dissociation degree (coefficient) represents the ratio between the number of the
dissociated kmoles and the initial number of total kmoles of the respective component. So:
- for the water vapours:
OH
OH
OH
2
d2
2 n
na (3)
- for carbon dioxide:
2
d2
2
CO
CO
COn
na (4)
where the number of kmoles ―n‖ is expressed in [kmole\kg].
There are initially considered in mixture OH2n kmoles of water vapours. After dissociation
according to the relation (1) in the balanced state, we find:
- kmole water vapours = OHOH 22a1n (5)
- kmole hydrogen = OHOH 22an (6)
- kmole oxygen = 2
an
OH
OH2
2 (7)
- total kmoles = 2
)a2(n
OH
OH2
2
(8)
In the balanced state, the partial pressures of gas components will be:
RT
V
a1n OH
OH
2O2H
2
(9)
TRV
anp
OHOH
H22
2 (10)
RTV2
an OH
O
2O2H
2 (11)
where V - mixture volume [m3]
R - constant of gases
T - temperature [C].
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180
According to the law of mass action, we can define the balance constant of chemical reaction
such as:
V
TR
)a1(
a
p
ppk
2
OH
3
OH
OH
O
2
H
OHp
2
2
2
22
2 (12)
Where (i = H2, O2, H2O) are the partial pressures of components.
The equation of gas state for the analyzed case becomes:
,TR)a2(n2
1pV OHOH 22
(13)
Where is the mixture pressure.
After substitution, we can write:
p
a1a2
ak
2
OHOH
3
OH
OpH
22
2
2
(14)
and
p
a1a2
ak
2
COCO
3
CO
pCO
22
2
2 (15)
We can estimate that the dissociation degree depends on the partial pressure of the
component (inversely proportional) and on the temperature (directly proportional). The
dissociation of the gases develops with heat absorption (input), a part of the physical heat of
gas mixture passing into the chemical heat of fuel components, appearing as a result of
dissociation, H2 and CO2.
The total heat content (enthalpy) – the physical heat plus the chemical heat – remains
constant in both cases, with dissociation and without dissociation. The theoretical combustion
temperature is reduced.
For determining the theoretical temperature, we made the initial special diagram Ig
(,t), for the marine fuel RMF 25, emulsified 5% without considering the dissociation. Then,
we made the special diagram Ig (I ,t) of emulsified fuel considering the dissociation, for a
temperature and a partial pressure given. We made the calculations and the graphical
interpretation by the help of a mathematical interpreter Mathcad 7.
So, for the same value of total heat content (enthalpy) 30933.4 [kJ\kg] we obtain the
temperature 1886 [C] for the 5% emulsified fuel considering the dissociation and 1947.6 [C]
for emulsified fuel without considering the dissociation, the temperature difference being of
= 61.6 [ C], so the theoretical combustion temperature with dissociation is lower than in the
case in which its determination is made without taking into account the dissociation.
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181
1800 1850 1900 1950 2000
Ga
s E
nth
alp
y [k
J/kg
]
3*104
3.03*104
3.05*104
3.08*104
3.1*104
3.13*104
3.15*104
3.18*104
3.2*104
Iti
It3i
Ti
Temperature [C] Fig. 7.1 - The calculation of theoretical combustion temperature for marine fuel RMF 25, emulsified 5% with
dissociation (__red_) and without dissociation (_blu__).
[C]
200
150
100
50
0 5 10 15 20Wf [%]
ΔT
Fig. 7.2 – Variation in temperature difference T depending on the water percentage in the emulsion, for the
marine fuel RMF 25.
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182
The temperature difference T depends on the value of emulsification coefficient
recording higher values for higher emulsification coefficients (Fig.7.3). This phenomenon
leads to the fall of theoretical combustion temperature which for the processes taking place in
gas phase can have as a direct effect the reduction of nitrogen oxide quantity.
2. CONCLUSION
Due to the dissociation of water vapours, the temperature of fuel components in the
burning gases can have higher values. In contact with the surrounding cold surfaces, a heat
exchange takes place inducing the fall of gas temperature so that, the balances of dissociation
reactions move to the right, leading to the reduction of fuel components produced as a result
of this phenomenon.
REFERENCES:
[1] WILLIAMS A., Combustion of droplets of liquid fuels, review. Comb. and
Flame 21), p. 12, 1973.
[2] WILLIAMS A., The mechanism of combustion of droplets and sprays of liquid fuels,
Oxidation and Combustion Reviews 3, p. 1.1968.
[3] GHIA Victor, Combustion graphology used to improve emulsions of water-in-heavy fuel
oil, IKP Stuttgart, 2001.
[4] MOROIANU Corneliu, Arderea combustibililor lichizi în sistemele de propulsie navale,
Editura Academiei Navale ―Mircea cel Bătrân‖, 2001.
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183
MATHEMATICAL MODEL FOR BURNING THE MARINE DIESEL
FUEL DROP IN A HOT OXIDIZING ENVIRONMENT
Ph. D1. Corneliu MOROIANU, Email address: [email protected]
Ph. D1. Traian FLOREA, Email address: [email protected]
Ph. D1. Ligia Adriana SPORIȘ, Email address: [email protected]
1The Naval Academy ―Mircea cel Bătrân‖ Constanța
1The Naval Academy ―Mircea cel Bătrân‖ Constanța
Abstract. It was proposed a mathematical model for burning the liquid fuel drop in a hot oxidizing environment.
The model was numerically solved by the finite element method. The droplet ignition periods were calculated as
a function of ambient temperature, oxygen concentration, initial droplet diameter and activation energy.
Key words: droplet, burning, mathematical model
1. INTRODUCTION
The object of this analysis is the liquid fuel droplet gradually subjected to the action of
hot, gaseous and exogenous medium. The fuel vapors at the surface of drop diffuse to the
environment and from the environment to the surface of drop diffuse the oxygen. In each
point of the area surrounding the drop in which the fuel and oxygen vapour concentrations are
non-zero, a chemical reaction is produced at a rate determined by Arrhenius‘ reaction,
generating the heat release, the fuel and oxygen consumption as well as the appearance of
burning products. In a certain point of which position depends on the heat balance of the
system, the temperature of gas increases reaching the ignition point. We propose the
following working assumptions:
- the fuel droplet considered has a sphere symmetry according to the assumption that
there is no relative motion between the droplet and the gas, as well as the free
convection is negligible;
- the heat transfer is made only by conduction;
- the pressure is the same all over the droplet medium and constant in time;
- the temperature of droplet surface is equal to the boiling temperature of the liquid at
the given pressure;
- all the components of the gaseous medium satisfy the equation of perfect gas state;
- the chemical reaction is a second-order reaction with a rate established by
Arrhenius‘law.
2. THE MATHEMATICAL MODEL
The processes developed in a gaseous atmosphere surrounding the droplet are
described by the set of equations for the energy conservation and for the components. This set
is formed of the equation of non-steady heat conduction including the flux term resulted from
the chemical reaction and other four non-steady equations of mass. Taking into account the
heat dissipation and including the flux terms for vapours of fuel, oxygen, nitrogen and
burning products, we can write:
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184
RT
EexppCAC
C
Q
r
Tr
rCr
1
t
T21
p
2
p
2 (1)
RT
EexpTCACb
r
TC
T
rD
rr
1
t
C21i
i
2
i
2
i (2)
where: i = 1,2,3,4 – refers to fuel, oxygen, nitrogen and burning gases;
C – concentration of component
D – mass diffusion coefficient (m2/s);
- coefficient of thermal conductibility;
A – pre-exponential constant (m3/kg s deg
½);
- density (kg/m3);
bi – stoichiometric coefficient for component i.
The indices used in the development of mathematical model:
c – liquid; g – gas
k – droplet N–normal conditions
p – fuel; s – droplet surface
w – boiling; z – ignition;
0 – initial parameters; 1 – fuel;
2 – oxygen; 3 – nitrogen;
4 – burning gases; - parameters of a gas element at a long
distance to the droplet.
The existing conditions in the droplet are described by the equation of non-steady heat
conduction:
r
Tr
rCr
1
t
T 2
p2
(3)
The boundary conditions for the three above equations are the following: for t = 0 and for t
0. Because of the non-linearity of the equations (1), (2) and (3) the analytical resolution of the
problem is not possible and it is necessary the numerical resolution.
3. TEST RESULTS FOR MARINE DIESEL DMA 25 MARINE FUEL To estimate the values of interest, namely, the dependence of delay time of ignition on
the initial diameter of droplet, the dependence of delay time of droplet ignition on the ambient
temperature as well as the dependence of delay time of ignition on the activation energy value
and on the pre-exponential constant mainly for the calculation of the values and the
parameters specific to marine Diesel DMA 25 (marine fuel):
c = 890 [kg/m3];
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c = 1,163 (0,12993 - 0,000025.T) [J/m s K];
Cpc = 4186,8. (-0,02144 + 0,00149. T) [J/kg K];
Q = 4192.107 [J/kg];
Tw = 353,26 [K ];
L = 3,94. 105 [J/kg].
The constants of diffusion have been calculated according to the relation:
Di = D0 (Ti / 273)2, (4)
where the values of diffusion D0 constants ―i‖ at the temperature 273 K are:
- for marine Diesel fuel: D0 = 0.751 . 10-5
[m2/s];
- for oxygen: D0 = 1.78 . 10-5
[m2/s];
- for nitrogen: D0 = 1.8 .10-5
[m2/s].
The diffusion constant for burning gases was calculated as a weighted average between the
diffusion constants of CO2 for which D0 = 1.39 x 10-5
(m2/s) and the water vapours D0 = 2.0 x
10-5
[m2/s] by the relation:
0H00HCO0CO02222sp
D.gD.gD ; (5)
Taking 2COg = 0,83 and OH2
g = 0,17, we have: sp0D = 1,49 10
-5 [m
2/s].
For calculation we take into account the variation of conductivity coefficient g and
the specific heat coefficient Cpg related to the temperature and the gas composition in the
ignition medium. It was supposed that at the droplet surface the temperature is equal with the
liquid boiling temperature and the concentration of fuel vapours is constant and equal with the
concentration of saturated vapours.
4. THE DEPENDENCE OF DELAY TIME OF IGNITION ON THE ACTIVATION
ENERGY VALUE AND ON THE PRE-EXPONENTIAL CONSTANT
The estimated delay time of droplet ignition mainly depends on the activation energy
value E and on the pre-exponential constant A, appearing within the flux that mark the rate of
oxidation reaction. These values are difficult to determine for the most fuels used. In Figure 1
and Figure 2 it is presented the dependence of delay time of ignition the DMA 25 fuel
droplet with its initial diameter d0 = 500 [m] and the initial temperature Tp0 = 300 K placed
in the air with ta = 1000 K on the activation energy and the pre-exponential constant.
The delay time of ignition the DMA 25 light fuel droplet is inversely proportional with
the value of pre-exponential constant, the variation ratios being different depending on the
activation energy value; thus, the three times increment of the pre-exponential constant value ,
for the same characteristically values of environment, droplet and activation energy, led to the
reduction of delay time value of ignition, from 1.6 to 4.5 times.
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10
20
30
40
50
60
50 75 100 125 150 A
2/1
3
kskg
m
E=35000
E=40000
E=45000
[ms]z
Fig. 1 - The dependence of delay time of ignition the marine DMA 25 fuel droplet on the activation energy for
different values of pre-exponential constants.
As the delay times of ignition experimentally determined, under the same conditions,
have different values (from a few milliseconds to 2.5 seconds) the estimation of real values of
E and A, on practical data, and of the curves in figures1 and 2, is relative. The values of the
activation energy and the pre-exponential constant were estimated in the following way:
- from the experimental data, they were adopted the values of critical diameter of light
fuel droplet docr = 200 m at an ambient temperature of T0 = 1090 0K;
- the value of the activation energy was chosen so that the ignition should be performed
when the droplet evaporation was completed, E = 41850 (kJ/kmol);
- for the other calculations, they were adopted the data obtained at tests, so E = 41350
(kJ/kmol) and A = 100 (m3
/kg s K1/2
).
0,2
0,4
0,6
0,8
1,0
1,2
1,4
1,6
1,8
2,0
0,00,6 0,7 0,8 0,9 1,0 1,1 1,2 1,3
][5000 md
][3000
KTp zlg
0
1000
T K
1
23.0
0,5
1,0
1.020 g
Fig. 2 - The dependence of delay time of ignition the marine DMA 25 fuel droplet on the pre-exponential
constant for different values of the activation energy.
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5. THE DEPENDENCE OF DELAY TIME OF DROPLET IGNITION ON THE
AMBIENT TEMPERATURE
The calculations were made for a variable ambient temperature T0 , from 800 to 1300
0K, for different initial parameters of the droplet and different shares of oxygen in the
burning medium. The results have been presented in Figures 3 and 4 by the relation:
lg z = f(1/T0) (6)
The curves represented in the figures are almost some straight lines, resulting that the delay
time of fuel droplet ignition is an exponential function of ambient temperature. The curves
represented in the figures 3 and 4 can be used for determining the constants Az and Ez on the
experimental data, with the relation:
Z = AZ exp (-Ez / R.T0) (7)
where:
Az and Ez are the conventional activation energy and the initiation energy of ignition.
0.7
0.8
0.9
1.0
1.1
1.2
1.3
1.4
1.5
0.60,6 0,7 0,8 0,9 1,0 1,1 1,2 1,3
]m[23,0g2o
][3000
KTp zlg
0
1000
T K
1
700
500300
]m[900d0
Fig. 3 - The dependence of delay time of ignition the marine DMA 25 fuel droplet on the ambient temperature
for different initial diameters.
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0,5
0,7
0,8
0,9
1,0
1,1
1,2
1,3
1,4
1,5
1,6
1,7
35000 40000 45000
0,6
zlg ][10000 KT
][5000 md
][3000
KTp
23.020 g
A=50
75
100
150
125
][Kmol
KJE
Fig. 4 - The dependence of delay time of ignition the marine DMA 25 fuel droplet on the ambient temperature
for different oxygen concentrations.
6. The dependence of burning time of droplet on the initial diameter
In figure 5 it was represented the dependence of burning time of droplet at the ambient
temperatures between 700 – 1100 0K for different initial diameters of droplet. It is obvious
that the burning time is much reduced with the decrease of initial diameter of the droplet.
a 210ms
40
30
20
10
500 1000 1500 2000 md 0
K700
K800
K1000
K1100
Fig. 5 - The dependence of delay time of ignition the marine DMA 25 fuel droplet for different initial diameters
and different ambient temperatures.
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189
7. CONCLUSIONS
The calculations made related to the process of ignition a fuel droplet in hot oxygen
medium, allow to draw the following conclusions:
- the delay time of fuel droplet ignition is an exponential function of the ambient
temperature; the activation energy of ignition (conventional ignition energy) hasn‘t a constant
value, it depends on the oxygen concentration in the medium and on the initial diameter of the
droplet;
- the delay time of ignition depends on the initial diameter of the droplet, specially,
for low relative temperatures of the medium and droplets of average initial diameter;
- the delay time of ignition depends on the oxygen concentration, specially, for low
temperatures and low oxygen concentration;
- the life time of the droplet reduces with the increase of the ambient temperature and
the oxygen concentration;
REFERENCES
[1] DRYER F.L., Water Adition to Practical Combustion Sistem-Concepts and Aplication,
Sympozium of Combustion, 1996, p. 34-38.
[2] LAW C.K., Theory of Multicomponent Droplet Vaporization, Combustion and Flame,
1998, No.4, p. 210- 219.
[3] LAW C.K., Asymptotic Theory for Ignition and extinction in Droplet Burning,
Combustion and Flame, 1989, No.6, p.24.
[4] MARTIN G. F., HEDLEY A. B., Combustion of a single droplets and simplified spray
system, J. of the Institute of fuel, 1971, p.38-54.
[5] GHIA V., COLIBABA A., A method for establishing the optimal quality of water-havy
fuel, Sci.Tech. Electrotehn. et Energ., 1996, Tome 41, nr.3, p. 401-412.
[6] MOROIANU C., Arderea combustibililor lichizi în sistemele de propulsie navale,
Editura Academiei Navale ―Mircea cel Bãtrân‖, 2001.p.44-76.
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190
ASUPRA UNUI SISTEM KOROVKIN
ÎNTR-UN CON DE FUNCŢII PONDERATE
Lector univ. Dr. Ligia-Adriana SPORIȘ,
Profesor ing. Dr. Traian FLOREA,
Conf. ing. Dr. Corneliu MOROIANU,
Academia Navală ‖Mircea cel Bătrân‖ Constanța, România
Abstract: The aim of this note is to present a construction of a Korovkin system for a cone of weighted
continuous set-valued functions.
Keywords: liniar space, Korovkin, function
1. PRELIMINARII
Scopul acestei lucrări este de a prezenta o construcţie a unui sistem Korovkin pentru
un con de funcţii ponderate.
Contextul în care ne vom situa va fi următorul:
- V,G , con local convex separat şi G , spaţiu liniar (astfel, putem considera că ne
aflăm în cadrul SOLC, deoarece topologia simetrică poate fi privită ca o topologie local
convexă şi local plină Hausdorff );
GAGCConv Ø topologia încompacta ,,GConvA G pe erioarăsup (1)
ce devine un con local convex ca subcon a conului local convex plin V,GDConc , unde
Vv,vvvV ;
- X , spaţiu local compact Hausdorff;
- W , pondere pe X .
Se verifică fără dificultate că V,GCConv este un con local convex dirijat la dreapta
şi M -uniform, v -semilatice, iar toate elementele sale sunt mărginite.
Reamintim că există o scufundare naturală ,GCConvGj** j , unde
GCConvA ,AaasupA .
Atunci,
**GGCConvM (2)
are următoarele proprietăţi:
a) *0 w,vM V,v -compactă.
b) M este strict separantă pentru GCConv ,
(i.e. V,v 1 ,GCConvBA, a.i. 0vM ,vBA a.i.
1BA ).
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191
c) n1,i ,Ga ,aVa,...,a,aco ii
n
1in21
.
Acum, vom considera:
XJ ,VvGCConv;XCfGCConv;XC sW Wvf a.i. compact şi
wvf0 pe J\X (3)
unde
Vv ,W
vvvV WWW este sistemul de vecinătăţi abstracte.
Fie
Xx M, ,GCConv;XCM*W
xWX (4)
Se demonstrează cu uşurinţă că GCConv;XCW şi WXM moştenesc aceleaşi proprietăţi ca
(1) şi (2).
2. UN SISTEM KOROVKIN PENTRU GCConv;XCW
Mai întâi, vom considera
G;XC GCConv;XCfGCConv;XF Wi
WW de rang finit, n,1i a.i.
x,...xcoxf X,x n1 (5)
Prop. 1:
GCConv;XFW este un subcon sup-stabil al conului local convex
WW V,GCConv;XC .
Corolar 2:
GCConv;XFW este un con dirijat la dreapta M -uniform şi v -semilatice.
Prop. 3:
Fie GCConv;XCf W .
Atunci, X,x ,G ,Vv * fvGCConv;XFg WW a.i. gf xx .
Demonstraţie prop.3:
Conform definiţiei lui x şi a continuitatii lui xfa ,xf a.i. fa x .
Conform definiţiei lui XY ,CW compact a.i. Wvxf şi
Y\Xx ,vxf0 W .
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192
Pentru Yy , alegem yfay . ( în particular, aax ).
Conform continuităţii lui yVUU ,f y
o
y a.i. yw1
vzfa y
şi
yUz ,1ywzw ; de unde:
zw
vzf
1yw
vzfay
, yUz .
Definim:
n
1iyi i
ag , unde n,1ii
este o partiţie a unităţii corespunzătoare
subacoperirii finite n,1iyi
U
a lui X . g verifică condiţiile: Xy ,vyfyg căci
1x1 şi n1,i ,0xi nyy a,...,aCXg
Prop. 4:
Fie V,G , un con local convex, cu toate elementele mărginite şi GC , un subcon.
Atunci, s*C
*C GGSubGSup .
Teorema 5:
GCConv;XFW este un sistem Korovkin (la stâng ) pentru GCConv;XCW .
Demonstraţie teorema 5:
Conform Prop.3 şi a definiţiei anvelopei inf, avem că ffx
şi deci,
WXF
MSubf W .
Cum WXM este strict separantă, W
X*0
W M0\vEx şi cum WF , duM dirijat,
sW*W
FCCSubf W
, conform Prop.4.
REFERENCES
[1]. Altomare, F. and Campiti, M., Korovkin–type Approximation Theory and its
Aplications, de Gruyter Studies in Mathematics. vol.17, cap.3, pag.122-169, cap.6, pag. 314 -
394, 1994;
[2]. Campiti, M., Approximation of continuous set-valued functions in Fréchet spaces,
L Analyse Numérique et la Theory de L Approximation, Tome 20, Nr.1-2, pag.25-38, 1991;
[3]. Keimel, K. and Roth, W., A Korovkin type approximation theorem for set-valued
functions, Proc. Amer. Math. Soc., pag.819-823, 1988.
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193
ASUPRA UNOR ASPECTE CALITATIVE ALE CONVERGENŢEI
ÎN SPAŢII LINIARE ORDONATE TOPOLOGICE
Lector univ. Dr. Ligia-Adriana SPORIȘ,
Conf.ing. Dr. Corneliu MOROIANU,
Profesor ing. Dr. Traian FLOREA,
Academia Navală ‖Mircea cel Bătrân‖ Constanța, România
Abstract: The aim of this note is to present some particular subspaces resembling with Korovkin closures.The
terminology used is like in [1].
Keywords: liniar space, Korovkin, function
1. INTRODUCERE
Definiţia 1.1. Fie (G,) un spaţiu uniform separat, E, F două mulţimi şi
(E,G), (E,G).
Un operator liniar FE:T se numeşte (, ) – admisibil dacă
)( T .
Definiţia 1.2. În acelaşi context, fie E (E,G) (înzestrată cu topologia indusă de
)(ES ) şi , E .
a) ,:,)()(:)( FELLExHW iiiU (,) – admisibil astfel încât iiL )(
este relativ compactă în E , FE:S)( (, ) – admisibil; dacă: SL H
i în
(F, (G)), atunci )x(S)x(Llim ii
în (F, (G)), unde F este )(FS compactă,
F este o mulţime închisă şi }.
b) )(:Ex)H(V , ii )()( , relativ compactă în E , dacă:
Hi în (G, ), atunci )()(lim xxi
i în (G, ) }.
c) )(:)( ExHU , )( ; dacă pe H, atunci
)()( xx }.
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2. PRINCIPALELE REZULTATE
Teorema 2.1. În contextul anterior şi presupunând în plus că este închisă în E ,
rezultă că )()()( HUHVHWU .
Corolar 2.2. Dacă E este spaţiu liniar topologic, H E, , E astfel încât este
slab*- închisă, atunci )()()( HUHVHWU .
Definiţia 2.3.
a) Fie E un spaţiu liniar reticulat topologic, H E şi V(E) conul homeomorfismelor
laticiale continue pe E.
FExHWU )(:)( spaţiu liniar reticulat topologic, V(F) echicontinuă
slab*- închisă; iiL )()( echicontinuă, FELi : operatori liniari şi pozitivi,
FES :)( homeomorfism laticial continuu, dacă SLHi : în topologia η ,
atunci )()(lim xSxLii
în η
b) Fie E un spaţiu reticulat normat, H E şi 1:)(1 VEV .
FExHW MU )(:)(, spaţiu reticulat normat; )(1 FV slab*-închisă cu
,sup MLii
FELi : operatori liniari şi pozitivi; FES :)( operator liniar şi
pozitiv )(,)( 11 FVEV -admisibil; dacă SLHi : în topologia η , atunci
)()(lim xSxLii
în η
c) EMEEBM :)(
Teorema 2.4.
a) Dacă E este spaţiu liniar reticulat topologic şi H E, atunci
)()( HUHWU ,
b) Dacă E este spaţiu reticulat normat şi H E, atunci
)(),(,)( 1, EBEVHUHW M
MU
.
BIBLIOGRAFIE
[1] Altomare, F., Campiti, M., Korovkin-type approximation Theory and its Applications, de
Gruyter Studies in Mathematics, vol. 17, 1994;
[2] Altomare, F., Teoremi di approsimazione di typo Korovkin in spazi di funzioni, Rend.
Mat. (6) 13, nr. 3, 1980;
[3] Altomare, F., On the universal convergence sets, Ann. Mat. Pure Appl. (4), 138, 1984;
[4] Donner, K., Extension of Positive Operators and Korovkin Theorems, Lecture Notes in
Math., 904, Springer-Verlag, 1982.
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195
PROGRAM FOR THE CALCULATION OF GEOMETRIC
OPTIMIZATION OF PRIMARY SEALS
Ph. D. Lecturer Monica BÂLDEA, University of Pitesti, Romania,
Ph. D. Lecturer Mihaela ISTRATE, University of Pitesti, Romania,
Abstract: The problem to be solved optimally is to minimize the flow losses.Program for the calculation of
geometric optimizationof primary seals indicates that the optimal geometry related to a optimum width of the
sealing surface
Keywords: program, primary seals, geometric optimization
1.INTRODUCTION
The face seal assembly operates centrifugal pump consists of the drive shaft equipped with
the pump sub-assembly Optimization of condensation is to satisfy two conflicting
requirements :
- Limit the minimum leakage ( loss ) or their absence . This involves minimizing and
reducing to zero the thickness of the lubricant film between the friction surfaces ( sealed fluid
to the lock-in) ;
- Limiting friction and wear , which involves ensuring satisfactory lubricating surfaces
Principal remedies are :
- Achieving a dynamic balance under the primary sealing element seals the fluid to ensure a
minimum separation of surfaces in relative motion or pressure contact asperities low as
possible ;
- Foster tribological contact conditions rough by a good choice of materials and lubricating
fluid .
Achieving these remedies involves knowing the influence of factors : the dynamic
behavior of the rotor surface deformation , thermal effects , physicochemical properties of
surfaces , etc. . It was found that a properly designed seal but made inappropriate material
does not work well . So in the present circumstances when the life of the seals Front has
expanded considerably assume that the materials are appropriate . This was due and
technologies for obtaining materials and thermochemical treatments.
2.PUTING THE OPTIMIZATION PROBLEM
Experimental to use a face seal size manufacturing firm shaft diameter of 45 mm. For
sealing the laboratory samples was achieved after a loss rate of 0.3 ml / h over a period of 300
hours at a pressure of 3 MPa and at a speed of 2870 rev / min.
Schematic diagram of unaligned primary seal is shown in Figure 1.
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196
Fig.1
Scheme friction ring surface geometry cell is presented in Figure 2
Fig.2
For sealing function , the question of optimal design front seal small portable flow
hydrodynamics.
Data entering the optimization program are :
a. Functional characteristics :
- Sealed fluid pressure , p1 = 3 MPa ;
- The speed of the rotor , n = 1500 rev / min ;
- The sealed fluid , characterized by ρ = 900 Kg/m3 ; = 0,02 Pa·s; E = 1,4·10
9 N/m
2;
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b.Geometrical characteristics :
- Inner radius of the sealing surface: Ri = 22.75 mm ;
- The outer radius of the sealing surface : Re = 26,75 mm;
- Maximum rotor radius Rm = 27,5 mm;
- The elastic element 8 mounted in parallel on the spring circumference d0 = 52 mm , the
rigidity k = 5.84 MPa , prestressed by f0 = 8 mm;
- Shaft diameter da = 45 mm;
- Misalignment of the rotor surface rad5
2 105 ;
- Misalignment of the stator surface rad5
1 105,2 ;
- Thickness of the sealing gap center .10 mh
The problem to be solved optimally is to minimize flow losses. I believe that optimal
geometry related to the optimal width of the sealing surface , b = Re - Ri .
3.SETTING RESTRICTIONS
- Dimensional restrictions:
021
1
a
a
R
Rr (1)
021
2
m
e
R
Rr (2)
012
3
elmi R
RRr (3)
024
44
e
i
R
Rr (4)
- Restriction for stability:
08 0
22
1 tWkfRRp am (5)
- Restrictions to avoid closing / opening gap sealing:
To find these restrictions must determine:
a) trh ,,min , trh ,,max ;
b) the conditions under which the 0000 maxmin hlhhhk , 1,00 k , ,..10 l
The restrictions are: 21000 eRhhk ; 00210 hlRh e
4.RESULTS AND CONCLUSIONS We use a program in MATLAB and EXCEL .In Figures 3 and 4 the change in the width
of the seal with the diameter of the pump shaft and the pressure shaft diameter of 37.5 mm.
Figure 5 shows the variation in flow from the pressure loss with the same width of seal to the
rotor.
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198
Fig. 3
Objective function to optimize been met by the shaft diameter of 80 mm. The other
restrictions are met in all diameters. The optimization program we considered as a basis of
comparison performed at the same flow diameter of the seal firm front[1],[7] .Burgmann
model exceeds the required flow rate of loss to a smaller diameter (75 mm). For pressures
above 3 MPa results change. It was considered appropriate for the study of change in the
width of the sealing surface of the shaft diameter while keeping the objective function, the
maximum loss rate of 0.3 ml / h depending on the pressure. It was observed that the width of
the sealing surface pressure doubles 15MP (the width of the pressure 10MP)
Fig 4
In Fig.4 shaft diameter is constant.,Pressure varies but the value of the objective
function.,Losses flow remains constant d = 37.5 mm; Q = 0.3 ml / h
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Fig 5
In Figure 5 shows that the pressure varies, the flow rate varies, but the difference Re-Ri are
the same for each pressure.
Burgmann losses flow relationship:
2221943
10752,710885,1
ln
dDnp
d
D
hQ
(6)
The optimized results were obtained at different pressures (p = 3 bar, p = 5bar, p = 7bar,
p = 10 bar, p = 15bar). Putting optimization problem is the problem to be solved, namely
optimal is to minimize flow losses and so the have established certain restrictions that lead to
specific outcomes that will help with future research on the study of mechanical seals.
BIBLIOGRAPHY
[1]Burgmann,Dipl.ing.Jochen Seeling-Gleitringdichtungen fur Steriprozesse in der
Pharmazie ,in der Biochemie,der Lebensmittelindustrie und Gentechnik,Nr.330,1986
[2]Crudu,I., Etanşări pentru organe de maşini in mişcare.Tribosisteme industriale,
Tribotehnica 80, Bucureşti,
[3]Istrate, M., Studiul etanşărilor primare la etanşările frontale, Editura Larisa, Câmpulung,
2013
[4]Istrate, M., Baldea,M., On predictive control using vibration detection method on
condensation damage to the machine with single stage pump,Scientific
Bulletin.Automotive,year XII,nr.16
[5]Lazăr, D.,ş.a. Influenţa mediului asupra alegerii cuplului de materiale pentru inelele
etanşărilor frontale. Tribotehnica` 87, 24-26 sept., Bucureşti, vol. III, p. 79-84.
[6]Popa, N.,ş.a. Asupra uzurii si tipurilor de uzură din etanşările axiale ale pompelor din
industria petrochimică, Tribotehnica 87, Bucureşti, 24-26 sept. 1987, p. 139-143.
[7]Schunk ‚Tradition et Progres,1990.
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A NOTE ON (α,β)-CUT IN INTUITIONISTIC
FUZZY SETS THEORY
Iuliana Carmen BĂRBĂCIORU , Lecturer Ph. D.
‖Constantin Brâncuşi‖ University, Tg. Jiu
Abstract.In this article, we give some basic definitions from Intuitionistic fuzzy sets theory andwe introduced
new operation (α,β)-cut in intuitionistic fuzzy sets theory with examples and characterizations.
Keywords: Intuitionistic fuzzy sets, support, (α,β)-cut and core of a intuitionistic fuzzy sets.
1. INTRODUCTION
The concept of intuitionistic fuzzy sets was introduced by K.T. Atanassov [1] as a
generalization of the notion of a fuzzy set
, AA x x x X (1)
Definition 1.[1] An intuitionistic fuzzy set (IFS) A in X is given by
, ,A AA x x x x X (2)
where Aμ :X [0,1] is called degree of membership and A : X [0,1] is called degree of
non-membership, with the condition
0 1A Ax x , x X (3)
Definition 2. [2] We call degrees of indeterminacy of x to A, for each A in X the numbers:
1A A Ax x x , x X (4)
IfA is a fuzzy set (1) then supp( ) / A(x) 0A x X is called fuzzy support of A. If and
if there is x such thatA(x)=1, i.e. / A(x) 1x X , the fuzzy set (1) is called normal. In
the case of fuzzy set theory an α-cutor a setof level α , α[0.1],of fuzzy set A is:
[A]α =
if 0
0 if
1
0
A
A
x X x
x X x
(5)
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Remark 1.Here B indicates the topological closure of a set B. Therefore this definition
requires that X be a topological space.
2.(α,β) -CUT AS THE INTUITIONISTIC FUZZY SETS
In the case of IFS we have:
Definition 3. [2] The support of A(denoted supp(A)) is the set of all those elements of an
universal set whose membership andnon-membership grades in A are greater than zero.
supp( ) / 0, 0,0 1A A A AA x X x x x x (6)
Example 1.Let and .
Then supp( ) , ,A a b d .
Definition 4. [2]The core of A(denotedcore(A)) is the set of all those elements of an
universal set whose membership grades in A are greater equal to one andnon-membership
grades in A are greater equal to zero.
core( ) / 1, 0,0 1A A A AA x X x x x x (7)
Example 2.Let and . Then
core( )A c .
Definition 5. [4]The maximum value attained by A x is referred to as the height of A is
denoted by ht(A). If ( ) 1Aht x and ( ) 0Aht x , then the IFS A is called normal.
Otherwise A is said to be subnormal.
Example 3.Let and . ThenA
is normal. If A is subnormal. Since
ht(A)=0.6.
Definition 6. We consider α,β[0.1] then, for any IFS set A,
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[A](α,β)
=
0, ,0 1 if
0, 0,0 1 if
, 1
0, 0
A A A A
A A A A
x X x x x x
x X x x x x
(8)
is called (α,β)-cut as the IFSA.
Definition 7. We consider α,β[0.1] then, for any IFS set A,
[A]+(α,β)
=
0, ,0 1 if
0, 0,0 1 if
, 1
0, 0
A A A A
A A A A
x X x x x x
x X x x x x
(9)
is called strong (α,β) -cut as the IFSA.
Remark 2. We observe that:
[A] (0,0)
= 0, 0,0 1 supp(A)A A A Ax X x x x x (10)
[A]+(0,0)
= 0, 0,0 1 =XA A A Ax X x x x x (11)
[A] (1,1)
= 1, 1,0 1 (A)A A A Ax X x x x x core (12)
[A]+(1,1)
= 1, 1,0 1 =A A A Ax X x x x x (13)
Example 4.Let and
. Then
[A](α,β)
=
if 0 0.2, 0.5 1
b,c if 0.2 0.4, 0.4 0.5
b,c if 0.4 0.6, 0.3 0.4
if 0.6 0.8, 0.2 0.3
if 0.8 1, 0 0.2
X
b
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[A]+(α,β)
=
, , if 0 0.2, 0.5 1
, if 0.2 0.4, 0.4 0.5
, if 0.4 0.6, 0.3 0.4
if 0.6 1, 0.4 0
b c d
b c
b c
The principle of excluded middle is not true to IFS. Some operations on IFSs have ben
also introduced in [4]:
Definition 8.Given two IFSs A and B over an universe of discourse X, one can define the
following relations:
A ⊂ B iff∀x ∈ X, BA x x and BA x x
A = B iffA ⊂ B andB ⊂ A
as well as the following operations [1]:
, ,A AA x x x x X
A ∩ B = , ,A B A Bx x x x X , where
min ,A B A Bx x and
max ,A B A Bx x
A ∪ B = , ,A B A Bx x x x X , where
max ,A B A Bx x and
min ,A B A Bx x
Theorem 1. Let A and B two IFS and one α,β, γ, δ[0.1]. Then following are true:
1) [A]+(α,β)
[A](α,β)
2) If α ≤ γ and β ≤ δ then [A](γ,δ)
[A](α,β)
3) [AB](α,β)
= [A](α,β) [B]
(α,β) [DA,B ](α,β) [DB,A ]
(α,β)
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4) [AB](α,β)
= [A](α,β) [B]
(α,β)
5) [AB]+(α,β)
= [A]+(α,β) [B]
+(α,β)
6) [AB]+(α,β)
= [A]+(α,β) [B]
+(α,β)
7) [AC]
(α,β) ≠ ( [A]
+(1-α,1-β) )
C
Where
[DA,B ](α,β)
=
, ,0 1 if
0, 0,0 1 if
0 , 1
0, 0
BA
A B
A
A
B
B
x X x x x x
x X x x x x
[DB,A ](α,β)
=
, ,0 1 if
0, 0,0 1 if
0 , 1
0, 0
B A B A
B A B A
x X x x x x
x X x x x x
Proof: 1) If ( ),
x A
, then ,A Ax x which means
,A Ax x proving that ( ),
x A
. So, [A]+(α,β)
[A](α,β)
.
2) If ( ),
x A
then , A Ax x . Consequently , A Ax x i.e.
( ),
x A
. So, [A](γ,δ)
[A](α,β)
.
3) Suppose ( ),[ ]x A B then ,max BA x x and
min ,A Bx x , AA x x or
, BA x x or ,B Ax x or ,B Bx x . Thus ( ),
x A
or
( ),
,B Ax D
or,
A,B
( )
x D
or ( ),
x B
( ) ( )( ) ( ) , ,, ,
, ,A B B Ax A B D D
. Conversely, assume that
( ) ( )( ) ( ) , ,, ,
, ,A B B Ax A B D D
.Then ( ),
x A
or
( ),
,B Ax D
or,
A,B
( )
x D
or ( ),
x B
, A Ax x or
, BA x x or ,B Ax x or ,B Bx x
,max BA x x and min ,A Bx x ( ),[ ]x A B .
4) Suppose ( ),[ ]x A B then ,min BA x x and
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max ,A Bx x , AA x x and , BA x x and
,B Ax x and ,B Bx x ( ) ( ), ,
x A B
.
Proof of (5) and (6) are exactly similar to those of (3) and (4). Only difference is
instead of inequality here we will have > inequality.
7) Suppose ( ),
Cx A
then , ,0 1A A A Ax x x x . But
then ( )1 ,1
C
x A
1 , 1 ,0 1A A A Ax x x x . Therefore
[AC]
(α,β) ≠ ( [A]
+(1-α,1-β) )
C .
Remark 2.In any fuzzy [AC]
α =( [A
C]
+(1-α))C
but in IFS [AC]
(α,β) ≠ ( [A]
+(1-α,1-β) )
C .
Example 5.Let and
.
,0.5,0.1 , , 0.2,0.6 , ,0.8,0 , ,0.1,0.7 ,( ,0.6,0.3CA a b c d e . Then
,( )
, ,C a cA e
for α=0.3, β=0.3. 1-α=0.7,1- β=0.7 [A]+(1-α,1-β)
= { } ( [A]+(1-α,1-β)
)C = {a,b,c,d,e}. Hence in IFSs, [A
C]
(α,β) ≠ ( [A]
+(1-α,1-β) )
C .
Theorem 2. Let A and B two IFS and one α, β, γ, δ[0.1]. Then:
1) A B if and only if [A](α,β)
[B](α,β)
2) A B if and only if [A]+(α,β)
[B]+(α,β)
3) A = B if and only if [A](α,β)
= [B](α,β)
Proof: 1) Assume that A Bwe will prove that[A](α,β)
[B](α,β)
for all α, β[0.1].
A Biff∀x ∈ X, BA x x and BA x x . Suppose there is (γ, δ)[0.1]
such that ( ), ,) (
A B
. This means there is an x in ,( )
A
such that ( ),
x B
.
Then ,B AA Bx x x x , a contradiction since AB.
Conversely, assuming that [A](α,β)
[B](α,β)
for all α, β,[0.1] we will prove that
AB. For this we have to prove that BA x x and BA x x for all x.
[A](α,β)
[B](α,β) ,A AB Bx x x x . Otherwise, y X for
which ,A AB By y y y y[A](α,β)
but y[B](α,β)
[A](α,β)
[B](α,β)
.
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A contradiction to the fact that [A](α,β)
[B](α,β)
for all α, β,[0.1].
Proof of (2) areexactly similar to those of (1). Only difference is instead of inequality here we
will have > inequality.Proof of (3) is trivial.
4. CONCLUSIONS
I have introduced a new definition of (α, β)-cut, by changing conditions in the
definition of [5], obtaining a generalization to α -cut level .
REFERENCES
[1] Atanasov, K.T., Intuitionistic fuzzy sets, Fuzzy Sets Syst., vol. 20,pp. 87–96, August 1986.
[Online]. Available: http://dx.doi.org/10.1016/S0165-0114(86)80034-3
[2] Atanasov, K.T.,Intuitionistic fuzzy sets: past, present and future, inEUSFLAT Conf., M.
Wagenknecht and R. Hampel, Eds. University ofApplied Sciences at Zittau/G¨orlitz,
Germany, 2003, pp. 12–19.
[3] Che, L.,Zadeh, A., Fuzzy sets, Information and Control, vol. 8, no. 3, pp. 338–353, 1965.
[4] Despi, I., Opriş, D., Yalcin, E., Generalized Atanasov Intuitionistic fuzzy sets, The Fifth
International Conference on Information, Process, and Knowledge
Management,eKNOW2013.
[5] Veeramani,V.,Batulan R., Some Characterisations of α-cut in Intuitionistic Fuzzy Set
Theory.
[6] Zeng, W. and Li, H., Correlation coefficient of intuitionistic fuzzy sets, Journal of
Industrial Engineering International, vol. 3, pp. 33–40, July 2007.
[7] Yusoff, B.,Taib, I., Abdullah, L.,and Wahab, A. F., A new similarity measure
on intuitionistic fuzzy sets,World Academy of Science Engineeringand Technology, vol. 78,
pp. 36–40, 2011.
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207
LYAPUNOV TYPE OPERATORS ON ORDERED BANACH SPACES
Iuliana Carmen BĂRBĂCIORU , Viorica Mariela UNGUREANU,
Constantin Brancusi University of Targu Jiu, Romania
Abstract. This paper studies the properties of a family of Lyapunov- type operators which includes the
ones associated with the linear quadratic optimal control of linear stochastic differential systems (SDSs)
affected by infinite Markovian jumps (MJs) [8]. We prove that this family of Lyapunov type operators
generates a positive causal evolution operator acting on certain infinite dimensional ordered Banach
spaces.
Keywords: Lyapunov operators, positive operators, nuclear operators.
1. INTRODUCTION
The applications of the optimal control theory in both science and engineering are
various and numerous. As an example, we mention here the optimal control problem of
minimizing the concentration of the polluted water during the waste water treatment [1].
Although this optimization problem is nonlinear, the linear quadratic (LQ) control methods
can be applied even in this case (see [4]]). Lyapunov equations play an important role in LQ
control theory. If the studied process suffers abrupt changes in its evolution, the classical
approach may not be applicable. For example, this happens in the case where the
mathematical model of the process is a linear stochastic differential system affected by
Markovian jumps. In this situation the Lyapunov equations are more complicated because
they are defined by Lyapunov type operators acting on infinite dimensional, ordered Banach
spaces of sequences of operators (see [8]). The aim of this paper is to identify a more general
class of such Lyapunov-type operators which generate positive evolution operators on certain
ordered Banach spaces.
2. NOTATIONS
In this paper H and U are real separable Hilbert spaces and ,.,. . denote the inner
product and the norms of elements and operators. Also UHL , is the real Banach space of
linear and bounded operators from H into .U If HU , we shall use the short notation
HL for HHL , . The Banach subspace of )(HL formed by all self-adjoint operators will
be denoted by HS . An operator )(HLA is called nonnegative and we write 0A , if
HSA and 0, xAx for all Hx . Following [6], we denote by )(1 HS (resp. )(2 HS )
the Banach space of all nuclear operators (resp. Hilbert-Schmidt operators) from HS .
Denoting by .Tr the trace operator and by the adjoint operator, we known that )(1 HS is a
Banach space when endowed with the nuclear norm TTTrT 1
. Also, it is known that
)(2 HS is a Hilbert space with the inner product
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RTTrTR 2
,
and the Hilbert-Schmidt norm TTTrT 2
(see for e.g. [3]).
Now, let Z be an interval of integers, which may be finite or infinite and let B be a real
Banach space. Then }sup,}{{ iggBiggl iiB ZZZ
Z is a real Banach space
with the norm Z
. ( see [6]). If HSB (or L(H)) then Z
Bl will be denoted by Z
HSl (or Z
HLl ).
An element Z
HSlX is said to be nonnegative and we write 0X if 0iX for all Zi .
The cone HK of all nonnegative elements of Z
HSl induces an order ― ‖ on Z
HSl . We say that
a linear and bounded operator ZZ
USHS llL , is positive if UH KK . If
Z
HULlA , , ,,
Z
UHLlB then AB and A are defined by Z iiBiAiAB , and
Z iiAiA , , respectively. We note that
Z
HULlA , and Z
HLlAB . Now let us
consider the linear subspace },{11
iTTlTi
HSHZ
ZN of
Z
HSl . It is known (see
[6]) that 1
.,HN is a Banach space.
If B is a Banach space we denote by ),( BJCb , RJ or TsJ , , Ts 0 , the
Banach space of all mappings BJG : that are continuous and bounded [5]. Similarly,
),(1 BJCb is the space of all continuously differentiable and bounded mappings on J which
derivatives are also bounded on J . For ),,R( Hb LC NL we consider the forward
differential equation
.
0,
HDsY
tstYtdt
tdY
N
L
It is known that this equation has a unique solution ),,(;, 1
Hb LTsCDstY N and the linear
operator on HN defined by tsDstYDstU c ,;,:,L is a strong evolution operator (in
the sense of Definitions 4.1 and 4.2 from [2], [5]) and is called the causal evolution operator
generated by L .
3. MAIN RESULTS
Let us consider a stochastic differential equation of the form
,0,
,,,
00
1
0
tttx
tdwtxttAdttxttAtdx kk
r
k
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209
where Rttwtwtwtw r ,,..,, 21 is a standard r dimensional Wiener process and
Rtt , is a right continuous, homogeneous Markov chain with the state space Z and the
infinitesimal matrix Z
jiij ,
with ,0ij if Zji, , ji and ciiijijj
,Z
,
ZZ
jcijjii
,1,
. Here itAk , is a notation for the i-th component itAk of tAk .
A Lyapunov-type operator associated with the above equation is given by
(1) HXXttXAXtAXt NL
,)( 1 ,
where HIitAitA ii
20 ),(),(
and jXitAiXitAiXt ijijj
kk
r
k
,1
1 ),(),(,Z
, Zi .
We know (see [8]) that it is well defined on HN . Now, let us consider a family R}{ ttLL
of operators defined by (1) with Z
HLb lCA , R , Hb LC N,R(1 and t1 being a
positive operator for all Rt . Arguing as in [7], we shall prove that L generates a positive
causal evolution operator on HN .
From the hypothesis Z
HLb lCA , R , we deduce easily that HLCiA b ,., R . It
follows (see [5]) that the family iA ., generates a causal evolution operator istU ;, on H,
which have the properties:
a) the mapping istUst ;,, is . continuous on }0,,{ tsst , uniformly with
respect to i ,
b) );,(,);,(
istUitAt
istU
, uniformly with respect to i for st ,
c) steistU ;, , where tAA t RR
sup: .
Now, let us prove the following.
Theorem 1. Assume that Z
HLb lCA , R . Then the linear and bounded operator
HXtXAXtAXt NL
,)( , Rt generates a positive causal evolution operator
on HN , namely HXstXUstUXst N
,,,:, .
Proof. Obviously, tL and st, are linear operators on HN and st, is positive. The
properties of nuclear operators (see the appendix of [6]) imply that ),R( Hb LC NL and
st, is 1
. -continuous on HN for all .0 ts Hence, L generates ( see [5]) a unique
uniformly continuous causal evolution operator stV , on N H . We shall prove that stV ,
coincides with st, and, consequently, L generates a positive causal evolution operator on
.HN Let stts 00 ,0, be fixed.
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210
We first observe that
1
00
0
0
1
0000
0
0
0
),,)((),(,,
),(,)(,,
:,,,,
istXUstUtAtt
istXUistUstU
itAXstiXsttAtt
iXstiXst
tsXitg
1
00
0
00
10000
,,,,
,)(,,)(
itAXsttt
istUstUiXstU
iXsttAistXUstUtA
.,,,,:,,)(
,,
,,,)(
,,)(,,
01000
0
0
0100
100
0
0
tsXitfiXstUistUtAtt
istUstU
istUistUiXstUtA
istXUistUtAtt
istUstU
From the properties a)-c) of the evolution operators istU ;, it follows that for any 0
there is 1,0 such that, for all 0tt , 10 3,,,, iXetsXitf . We conclude
that 110 33,,,, XeiXetsXitg
ii
ZZ
. Thus, for any 0 there is 1,0
such that
etAststtAtt
stst3,,)(
,,0000
0
0
for all 0tt . Here .
is the norm of HL N . Thus that the mapping st, is norm differentiable in t on HN and
.,
,,,
HIss
sttt
st
N
L
On the other hand, we know that the unique solution of the above equation is stV , and,
therefore, ststV ,, . The conclusion follows.
Lemma 2. The cone HH NK is closed.
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211
Proof. Let HHnX NK ,nN, be a convergent sequence in HN . We have to prove that its
limit also belong to HH NK . Let Hnn XX N lim . It follows that iX n is . -
convergent to iX in HL . Since the cone HS of all nonnegative operators from HL
is closed, we deduce that 0iX for all Zi and HX K . Now it is clear that
HHX NK and the conclusion follows.
The next theorem is the main result of this paper.
Theorem 3. If Z
HLb lCA , R and Hb LC N,R(1 is such that HLt N1 is a
positive operator for all Rt , then the mapping HXXtXtX NL ,1 , Rt
generates a positive causal evolution operator on HN .
Proof. Consider the Cauchy problem
HXtX
tXttXtdt
tdX
N
L
00
1 ,
on HN . Since ),R(1 Hb LC NL it follows that 1L generates an evolution operator
0,ttS on HN and the unique solution 00 ,,: XttXtX of the above Cauchy problem is
given by 0000 ,,, XttSXttX . Moreover, a variation of constant formula shows that
tX is also the unique solution of the integral equation
.,, 100
0
dssXsstXtttX
t
t
It is known that the solution of the above integral equation can be obtained as the limit of the
sequence of Voltera approximations N, ktX k defined by
.,,
R,
1001
00
0
dssXsstXtttX
tXtX
k
t
t
k
Lemma 2, implies that 01 ,0,
0
ttdssXsst k
t
t
if HHk sX NK for all
tts ,0 . Thus, it follows inductively that ttssX HHk ,, 0 NK for all Nk . Using
again Lemma 2 we deduce that 0, tttX HH NK because it is the limit in HN of a
sequence of elements of the closed cone HH NK .
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REFERENCES
[1] E. V. Grigorieva, E. N. Khailov, Optimal Control of waste water cleaning plant, Eighth
Mississippi State - UAB Conference on Differential Equations and Computational
Simulations. Electronic Journal of Differential Equations, Conf. 19 (2010), pp. 161-175.
[2] W. Grecksch, C.Tudor, Stochastic Evolution Equations, A Hilbert Space Approach Math.
Res. Vol 75, Akademic Verlag, 1995.
[3] C. Kubrusly, The Elements of Operator Theory, Second edition, Birkhäuser, 2011..
[4] Magdi S. Mahmoud, Coordinated Control of Waste Water Treatment Process,
Proceedings of the World Congress on Engineering 2010 Vol III..
[5] A. Pazy , Semigroups of linear operators and applications to partial differential
equations, Applied Mathematical Sciences 44,Springer- Verlag, Berlin, New -York, 1983.
[6] V.M. Ungureanu and V. Dragan, Stability of discrete-time positive evolution operators on
ordered Banach spaces and applications, J. Differ. Eqns. Appl., 19(2013), 6, 952-980.
[7] V. M. Ungureanu, V. Dragan, Nonlinear differential equations of Riccati type on ordered
Banach spaces, Electronic Journal of Qualitative Theory of Differential Equations, Proc. 9th
Coll. QTDE 17 (2012): 1-22.
[8] V. M. Ungureanu, Optimal control for infinite dimensional stochastic differential
equations with infinite Markov jumps and multiplicative noise, J. Math. Anal. Appl.,
DOI:10.1016/j.jmaa.2014.03.052, 417.2 (2014): 694-718.
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RANDOMLY GENERATED SUBGROUPOIDS OF X×Z×X
Mădălina Roxana BUNECI, University Constantin Brâncuşi of Târgu-Jiu
Abstract. The purpose of this paper is to provide Maple procedures for random generation of subgroupoids of
the trivial groupoid X×Z×X, where Z is the group of integer numbers.
Keywords: discrete groupoid; pseudorandom number generator; orbit.
.
1. INTRODUCTION
We shall use the notation and terminology from [1]-[3]. In [3] we proved that a
subgroupoid G of XZX, where Z is the group of integer numbers, is characterized by the
set X and two functions f : XX and k :XZ satisfying the properties
1. f(f(u))=f(u) for all uX.
2. k(f(u)) 0 for all uX.
3. If k(f(u)) ≠ 0, then k(u){0,1,…, k(f(u))-1}.
If the function f and k are given, then the groupoid G can be recover as in [2]:
G ={(u,ku,v+tku,u,v): f(u)=f(v), tZ},
where
ku,u := k(f(u)) for all uX.
ku,v:= ( k(u)+k(f(u)-k(v)) mod k(f(u)), if k(f(u))≠0
k(u) – k(v), if k(f(u)) = 0
for all (u,v)X×X with the property that f(u)=f(v) and u≠v. Conversely, k(u)=ku,f(u) for all
uX.
The purpose of this paper is to provide Maple procedures for random generation of the
values of the functions f:XX and k:XZ and consequently, of the groupoid G. The
motivation for generating such groupoids is to test the visualization procedures defined in [4].
2. SUBGROUPOIDS OF XZX GENERATED USING MERSENNE
TWISTER ALGORITHM
As in [3] for implementation in Maple of the reduction to A={x1,x2,…,xn}X of a
subgroupoid GX×Z×X characterized by functions f (satisfying f(A)A) and k we use a list
gd of three arrays:
gd[1] contains a sequence obtained by sorting A and eliminating the duplicates,
gd[2][i] = the index in gd[1] of f(gd[1][i]), i=1..n,
gd[3][i] = k(gd[1][i]), i=1..n.
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In order to generate the subgroupoids G we use the RandomTools package (in the
Maple environment) and more precisely, the RandomTools[MersenneTwister] subpackage
that contains functions for creating pseudo-random number generators using the Mersenne
Twister algorithm. The Mersenne Twister algorithm was developed in 1997 by Makoto
Matsumoto and Takuji Nishimura [5] and it is based on a matrix linear recurrence over a
finite binary field F2. It provides long period length of 219937
-1, high order dimensional
equidistribution property, speed and reliability. For a k-bit word length, the Mersenne Twister
generates numbers with an almost uniform distribution in the range [0,2k − 1].
The below procedure random_groupoid(n, kmax, nmax) randomly generates a
subgroupoid G={(u,ku,v+tku,u,v): u~v, tZ} of X×Z×X, where X is a finite set and Z is the
group of integers. The data of G are stored in gd. The parameter n represents the cardinality of
X, kmax is the maximum of the set
{ku,u, uX}={k(f(u)), uX}
and nmax is maximum of the set
{|ku,f(u)|, uX, k(f(u))=0}
> with(RandomTools[MersenneTwister]): > random_groupoid:=proc(n, kmax, nmax)
local gd,i,j,s,norbits,sn,co,represent,a,b; gd:=[array(1..n),array(1..n), array(1..n)]; for i from 1 to n do gd[1][i]:=i end do;
s:=NewGenerator(range = 1 .. n); norbits:=s(); co:=1; represent:=array(1..n);
represent[1]:=1; gd[2][1]:=1;
s:=NewGenerator(range = 0 .. kmax); gd[3][1]:=s(); for i from 2 to n do
s:=NewGenerator(range = 0 .. n-1); sn:=s();
if sn<norbits then
co:=co+1; represent[co]:=i; gd[2][i]:=i;
s:=NewGenerator(range = 0 .. kmax); gd[3][i]:=s() else
s:=NewGenerator(range = 1 .. co); a:=s();
s:=NewGenerator(range = a .. co); b:=s();
s:=NewGenerator(range = a ..b);
gd[2][i]:=represent[s()]; if gd[3][gd[2][i]]=0 then
s:=NewGenerator(range = 0 .. 2*nmax); gd[3][i]:=-nmax+s()
else s:=NewGenerator(range = 0 .. gd[3][gd[2][i]]-1); gd[3][i]:=s()
end if end if
end do; RETURN(gd)
end proc;
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The NewGenerator(range=integer..integer) command used in the procedure
random_groupoid requires RandomTools[MersenneTwister] subpackage. It outputs a Maple
procedure, a pseudo-random number generator, which when it is called outputs one pseudo-
random integer. The output of the generator belongs to indicated range. >gd:=random_groupoid(10,8,3);
The groupoid encoded by gd is G ={(u,ku,v+tku,u,v): u,vX, f(u)=f(v), tZ}X×Z×X, where
X={1,2,3,…,10} and
ku,u := k(f(u)) for all uX.
ku,v:= ( k(u)+k(f(u)-k(v)) mod k(f(u)), if k(f(u))≠0
k(u) – k(v), if k(f(u)) = 0
f : XX, f(1)= 1, f(2)=1, f(3)= 3, f(4)=3, f(5)= 5, f(6)=6, f(7)= 5, f(8)=1, f(9)= 9, f(10)=1,
k:XZ, k(1)=3, k(2)=1, k(3)=2, k(4)=1, k(5)=1, k(6)=7, k(7)=0, k(8)=0, k(9)=4, k(10)=2.
Hence for instance
2
8G ={: r()=2 and d()=8}={(2,k2,8+tk2,2,8): tZ}
={(2,k(2)-k(8) mod k(1)+k(1)t,8): tZ} ={(2, 1+3t,8): tZ}
The procedure orbits(gd) [3] displays the graph of the equivalence relation (principal groupoid) associated with the groupoid G
encoded by gd. Let us see it result for the preceding groupoid
as well as for another randomly generated groupoid.
>orbits(gd);
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>orbits(random_groupoid(100,8,3));
The following procedure random_groupoid_op:=proc(n, kmax, nmax) generate a
subgroupoid G ={(u,ku,v+tku,u,v): f(u)=f(v), tZ}X×Z×X, where X={1,2,3,…,n} with the
property that the probabilities pk of {u: f(u)=f(k)} satisfy: p1p2…pn. The parameters n,
kmax, nmax have the same signification as in the case of the procedure random_groupoid.
> with(RandomTools[MersenneTwister]): > random_groupoid_op:=proc(n, kmax, nmax) local gd,i,j,s,norbits,sn,co,represent;
gd:=[array(1..n),array(1..n), array(1..n)]; for i from 1 to n do gd[1][i]:=i end do;
s:=NewGenerator(range = 1 .. n); norbits:=s(); co:=1; represent:=array(1..n);
represent[1]:=1; gd[2][1]:=1;
s:=NewGenerator(range = 0 .. kmax); gd[3][1]:=s(); for i from 2 to n do
s:=NewGenerator(range = 0 .. n-1); sn:=s();
if sn<norbits then
co:=co+1; represent[co]:=i; gd[2][i]:=i;
s:=NewGenerator(range = 0 .. kmax); gd[3][i]:=s() else
s:=NewGenerator(range = 1 .. co);
gd[2][i]:=represent[s()]; if gd[3][gd[2][i]]=0 then
s:=NewGenerator(range = 0 .. 2*nmax); gd[3][i]:=-nmax+s()
else s:=NewGenerator(range = 0 .. gd[3][gd[2][i]]-1); gd[3][i]:=s()
end if end if
end do;
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RETURN(gd) end proc;
>gd:=random_groupoid_op(100,8,3);
>orbits(gd);
The procedure perm_unit_space(gd,p) permutes with respect to p: XX the unit
space X of the groupoid G ={(u,ku,v+tku,u,v): f(u)=f(v), tZ}X×Z×X encoded by gd. More
precisely, it returns the groupoid H=
u
v
u,v
H , where
u
vH ={(u,kp(u),p(v)+tkp(u),p(u),v): f(p(u))=f(p(v)), tZ}
> perm_unit_space:=proc(gd,p) local n,i, gd2, gd3, j;
n:=op(2,op(2,gd[1])); gd2:=array(1..n);gd3:=array(1..n);
for i from 1 to n do
j:=1;
while(j<i) and gd[2][p[i]]<>gd[2][p[j]] do j:=j+1 end do;
if(j<i)then gd2[i]:=j;else gd2[i]:=i end if;
end do;
for i from 1 to n do
if gd2[i]=i then
gd3[i]:=gd[3][gd[2][p[i]]];
else
if gd[3][gd[2][p[i]]]<>0 then
gd3[i]:=irem(gd[3][p[i]]+gd[3][gd[2][p[i]]]-gd[3][p[gd2[i]]],
gd[3][gd[2][p[i]]])
else
gd3[i]:=gd[3][p[i]]-gd[3][p[gd2[i]]]
end if `
end if
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end do; RETURN([evalm(gd[1]),evalm(gd2),evalm(gd3)])
> end proc;
In the following we use the procedure random_groupoid_op(n, kmax, nmax) to
generate gd that encodes the subgroupoid
G ={(u,ku,v+tku,u,v): f(u)=f(v), tZ}X×Z×X, X={1,2,3,…,n}
with the property that the probabilities pk of {u: f(u)=f(k)} satisfy: p1 =max {pj, j=1..n}. Then
we use the command randperm(n) (belonging to combinat package) to get a random
permutation p, and lastly the procedure perm_unit_space(gd,p) to permute the unit space X
of the groupoid G with respect to p: XX and obtain a new groupoid.
> gd:=random_groupoid_op(10,8,3);
> with(combinat):
> p:=randperm(10);
> perm_unit_space(gd,p);
> orbits(gd);
>orbits(perm_unit_space(gd,p));
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BIBLIOGRAPHY
[1] M. Buneci, Groupoids and irreversible discrete dynamical systems I, Fiabilitate şi
durabilitate (Fiability & durability), No. 1/2012, 350-355.
[2] M. Buneci, Groupoid reductions associated to discrete dynamical systems, Annals of the
―Constantin Brâncuşi‖ University of Târgu-Jiu. Engineering Series. No. 3(2012), 171-182.
[3] M. Buneci, Using Maple to represent the subgroupoids of trivial groupoid X×Z×X,
Fiabilitate şi durabilitate (Fiability & durability), Supplement No 1 (2013), 446-454.
[4] M. Buneci, Using Maple for visualization of topological subgroupoids of X×Z×X, 7th
Symposium Durability and Reliability of Mechanical Systems SYMECH 2014, Târgu-Jiu,
May 2014.
[5] M. Matsumoto and T. Nishimura, Mersenne twister: A 623-dimensionally equidistributed
uniform pseudorandom number generator, ACM Transactions on Modeling and Computer
Simulations 8 (1998), 3–30.
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USING MAPLE FOR VISUALIZATION OF TOPOLOGICAL
SUBGROUPOIDS OF X×Z×X
Mădălina Roxana BUNECI, University Constantin Brâncuşi of Târgu-Jiu
Abstract. The purpose of this paper is to present various ways to visualize topological subgroupoids of the
trivial groupoid X×Z×X, where Z is the group of integer numbers endowed with the discrete topology and X a
topological space.
Keywords: topological groupoid; Khalimsky topology; equivalence relation; visualization;
.
1. INTRODUCTION
We shall use the notation and terminology from [1] - [4]. In [3] we proved that a
subgroupoid G of XZX, where Z is the group of integer numbers, is characterized by the
graph R of an equivalence relation on X and a family of integer numbers {ku,v}(u,v)R
satisfying the following conditions:
1. ku,u0 for all uX.
2. If ku,u ≠ 0, then ku,v + kv,w = ku,w (mod ku,u), else ku,v + kv,w = ku,w.
We also proved that if ku,u ≠0 and u≠v, then we may consider
ku,v{0,1,…, ku,v-1}
for all v such that (u,v)R. The groupoid G is represented as G=
u
v
u,v R
G
where
u
vG ={(u,ku,v+tku,u,v): tZ}, (u,v)R
Alternatively, we prove in [4] that G can be completely characterized by X and two functions
f:XX and k :XZ satisfying the properties
4. f(f(u))=f(u) for all uX.
5. k(f(u)) 0 for all uX.
6. If k(f(u)) ≠ 0, then k(u){0,1,…, k(f(u))-1}.
If the function f and k are given, then the relation R is defined by (u,v)R if and only if
f(u)=f(v), ku,u := k(f(u)) for all uX and
ku,v:= ( k(u)+k(f(u)-k(v)) mod k(f(u)), if k(f(u))≠0
k(u) – k(v), if k(f(u)) = 0
for all (u,v)X×X with the property that f(u)=f(v) and u≠v.
The purpose of this paper is to provide various ways to visualize the topological
subgroupoids G of XZX assuming that X is a topological space and Z has the discrete
topology. We use Maple environment to implement the visualizations.
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2. VISUALIZATION OF SUBGROUPOIDS OF XZX DATA
Let G ={(u,ku,v+tku,u,v): f(u)=f(v), tZ} be a subgroupoid of XZX, where X is a finite
set {x1, x2, …, xn} and Z is the group of integers. As in [4] we shall use the characterization
of G in terms of f:XX and k :XZ in order to implement in Maple the groupoid G, where
k(u)=ku,f(u) for all uX. More precisely, we use a list gd of three arrays:
gd[1] contains the elements of X (gd[1][i]=xi, i=1..n),
gd[2][i] = the index in gd[1] of f(gd[1][i]), i=1..n,
gd[3][i] = k(gd[1][i]), i=1..n.
The procedure visualization(gd) represent each (r,d)-fibre j
i
x
xG as the rectangle with
top left corner (i-1,j) and bottom right corner (i,j-1) filled with a color uniquely determined by
i jx ,xk and i ix ,xk .
visualization:=proc(gd)
local n,no_iso0, maxku, maxkuv0,i,j,elem,m,c,p,q,z,mk;
n:=op(2,op(2,gd[1]));
no_iso0:=0; maxku:=0; maxkuv0:=0;
for i from 1 to n do
if gd[3][gd[2][i]]>maxku then maxku:=gd[3][gd[2][i]]
else
if gd[3][gd[2][i]]=0 then
no_iso0:=no_iso0+1;
for j from 1 to i-1 do
if
(gd[2][j]=gd[2][i] and abs(gd[3][i]-gd[3][j])>maxkuv0)
then
maxkuv0:= abs(gd[3][i]-gd[3][j]);
end if
end do
end if
end if
end do;
elem:=array(1..n*n);c:=array(0..n+1,0..n+1);
for i from 0 to n+1 do
for j from 0 to n+1 do
c[i,j]:=-2
end do
end do;
z:= no_iso0/n; mk:= 2*(1-z)/(maxku*(maxku+1));
for i from 1 to n do
for j from 1 to n do
if gd[2][i]=gd[2][j] then
if gd[3][gd[2][i]]=0 then
c[i,j]:=frac(1+(gd[3][i]-gd[3][j])/(2*maxkuv0+1)*z);
else
c[i,j]:=z/2+(gd[3][gd[2][i]]*(gd[3][gd[2][i]]-1)/2+1+
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irem(gd[3][gd[2][i]]+gd[3][i]-gd[3][j],gd[3][gd[2][i]]))*mk;
end if
end if
end do
end do;
m:=0;
for i from 1 to n do
for j from 1 to n do
if gd[2][i]=gd[2][j] then
m:=m+1;
elem[m]:=rectangle([i-1,j],[i,j-1],color=COLOR(HSV,c[i,j],1.,1.));
end if;
end do;
end do;
RETURN(display(seq(elem[i],i=1..m),axes=none,style=patchnogrid))
end proc;
For each k{1,2,…,kmax}, where kmax=max{ku,u: uX} the procedure visualization
allocates a hue (in HSV model). Thus we can visualize the distribution of {ku,u: uX} among
{1,2,…,kmax}. However if kmax is big and the length of the minimal interval containing the
set {ku,u:uX} is small, then less details are visible. Therefore in this it would be better to use
a version of the visualization procedure that allocates hues (in HSV model) only for each ku,u.
The left image below is obtain using the first version, while the right correspond to the second
version.
Also if n is big less details are visible. In this case it is better to represent only the (r,d)-fibres j
i
x
xG with i=a1..b1 and j=a2...b2 where a1, b1, a2 and b2 are chosen in concordance to the region
of interest. The pictures below illustrated this situation:
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3. VISUALIZATION OF TOPOLOGY OF SUBGROUPOIDS G XZX
Let us consider that X is endowed with a topology X and Z is endowed with the
discrete topology. Then under the operations
(x, n, y)(y, m, z) = (x, n+m, y)
(x, n, y)-1
= (y, -n, x)
XZX become a topological groupoid. In the following the unit space of the groupoid
XZX, {(x,0,x), xX}, is identified with X. We endow any subgroupoid G XZX with
the subspace topology G coming from XZX.
In [1] we started with a topological groupoid (G, ηG), we introduced a topology ηR(ηG)
on the principal groupoid R associated with G (called transported topology from G) and a new
topology ηGR on G (called the modified topology on G with respect to R). Let us recall that a
basis for the topology ηR(ηG) is given by the family of sets {U(F)}F, where each F is a finite
collection of open subsets of G (i.e. F G) and
U(F) = Ud,rFU
Moreover a basis for the topology ηGR is given by
FU
1Ud,rd,rV
where V runs over all open sets of G and F runs over all finite collections of open subsets of
G.
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Let us use the notation
(x,y)(u,v)
if and only the sequence ((xi,yi))i converges to (u,v), where xi=u and yi=v for all i. According
to [2] this is equivalent to (xi)iI converges to u with respect to X, (yi)iI converges to v with
respect to X and
1. for ku,u0: kx,x0, kx | ku (kx divides ku) and kx,x | ku,v –kx,y
2. for ku,u=0: (kx,x =0 and ku,v =kx,y) or (kx,x0 and kx,x | ku,v –kx,y)
We want to know if (u+p,x+q)(u,v) for p,q{-1,0,1}. Let us assume that u+p (respectively,
v+q)U for all neighborhood U of u (respectively, v) with respect to X. In this case if p=0 or
q=0, then (u+p,x+q)(u,v) if and only the procedure visualization allocates the same hue (in
HSV model) to u
vG and u p
v qG
. If (u+1,v+1)(u,v) then we draw a rectangle r1 on the right
top corner of the rectangle r associated to u
vG by the procedure visualization. The dimensions
of r1 are ¼ of the dimensions of r and color is that of u p
v qG
. The below procedure
visualization_top(gd) allows us to visualize the topology of G in this way for the case
when X is endowed with the indiscrete topology X={, X}. We present here only the part of
the procedure that differs from visualization(gd), meaning the construction of the array
elem containing the rectangles associated to each u
vG .
visualization_top:=proc(gd)
………….
m:=0;
for i from 1 to n do
for j from 1 to n do
if gd[2][i]=gd[2][j] then
m:=m+1;
elem[m]:=[rectangle([i-1,j],[i,j-1],color=COLOR(HSV,c[i,j],1.,1.))];
for p from -1 to 1 by 2 do
for q from -1 to 1 by 2 do
if
((c[i+p,j+q]<>-2) and (c[i,j]<>c[i+p,j+q]) and (gd[3][gd[2][i+p]]<>0) and
(irem(gd[3][gd[2][i]],gd[3][gd[2][i+p]])=0) and (irem(gd[3][i+p]-
gd[3][j+q]-gd[3][i]+gd[3][j],gd[3][gd[2][i+p]])=0))
then
elem[m]:=[rectangle([i-1/2+p/4,j-1/2+q/4], [i-1/2+p/2,j-1/2+q/2],
color=COLOR(HSV,c[i+p,j+q],1.,1.)),op(elem[m])]
end if;
end do;
end do;
end if;
end do;
end do;
…….
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The following two pictures are the representations of a groupoid G XZX, where
X={1,2,…,n} returned by the procedure visualization (left) and visualization_top (right). We
see, for instance that (4,4)(3,3), (4,4)(5,5), (4,6)(5,5), (4,6)(3,5), etc.
The below procedure visualization_topK(gd) allows us to visualize the topology
of G the case when X={x1, x2, …, xn} is endowed with the topology X with basis
{{x2k+1},k=0..[n/2]} {{x2k-1, x2k, x2k+1}X, k=1..[n/2]}
(Khalimsky topology – see [5], [6] and [7]). For an (r,d)- fibre u
vG we modify the color of the
rectangle associated to u
vG by the procedure visualization by decreasing the saturation (in the
HSV model) by 1/8 for each odd index of u, v in X. We present here only the part of the
procedure that differs from visualization(gd), meaning the construction of the array elem
containing the rectangles associated to each u
vG .
visualization_topK:=proc(gd)
.....
m:=0;
for i from 1 to n do
for j from 1 to n do
if gd[2][i]=gd[2][j] then
m:=m+1;
elem[m]:=[rectangle([i-1,j],[i,j-1],color=COLOR(HSV,c[i,j],1-
irem(i,2)/8-irem(j,2)/8,1.))];
if irem(i,2)=0 and irem(j,2)=0 then
for p from -1 to 1 by 2 do
for q from -1 to 1 by 2 do
if
((c[i+p,j+q]<>-2) and (c[i,j]<>c[i+p,j+q]) and (gd[3][gd[2][i+p]]<>0) and
(irem(gd[3][gd[2][i]],gd[3][gd[2][i+p]])=0) and (irem(gd[3][i+p]-
gd[3][j+q]-gd[3][i]+gd[3][j],gd[3][gd[2][i+p]])=0))
then
elem[m]:=[rectangle([i-1/2+p/4,j-1/2+q/4], [i-1/2+p/2,j-1/2+q/2],
color=COLOR(HSV,c[i+p,j+q], 1-irem(i+p,2)/8-irem(j+q,2)/8,1.)),op(elem[m])]
end if;
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end do;
end do;
end if;
end if;
end do;
end do;
The following two pictures are the representations of a groupoid G XZX, where
X={1,2,…,n} returned by the procedure visualization_top (left) and visualization_topK
(right). We see, for instance that (2,2)(1,1) if X is endowed with the indiscrete topology
but not with the Khalimsky topology.
BIBLIOGRAPHY
[1] M. Buneci, Topological groupoids with locally compact fibres, Topology Proceedings 37
(2011), 239-258.
[2] M. Buneci, Groupoids and irreversible discrete dynamical systems II, Fiabilitate şi
durabilitate (Fiability & durability), No. 1/2012, 356-359.
[3] M. Buneci, Groupoid reductions associated to discrete dynamical systems, Annals of the
―Constantin Brâncuşi‖ University of Târgu-Jiu. Engineering Series. No. 3(2012), 171-182.
[4] M. Buneci, Using Maple to represent the subgroupoids of trivial groupoid X×Z×X,
Fiabilitate şi durabilitate (Fiability & durability), Supplement No 1 (2013), 446-454.
[5] E.D. Khalimsky, Pattern analysis of n-dimensional digital images, in: Proc. of the IEEE
Internat. Conf. on Systems, Man and Cybernetics, 1986, 1559–1562.
[6] K. Y. Kong, Concepts of digital topology, Topology and its applications, 46 (1992), 219-
262
[7] V. Kovalevsky, Finite Topology as Applied to Image Analysis, Computer Vision, Graphics
and Image Processing, 46 (2) (1989), 141-161.
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ASPECTS OF A LINEAR PROGRAMMING MODEL DEDICATED TO
THE TRANSPORT SYSTEM
Lect. PhD. eng. Elisabeta Mihaela CIORTEA,
University ‖1 Decembrie 198‖ of Alba Iulia, [email protected]
Lect. PhD. math. Mihaela ALDEA,
University ‖1 Decembrie 198‖ of Alba Iulia, [email protected]
Abstract: In the paper is presented a linear programming model whose theory has benefited from the
contribution of the interdisciplinary approach that allowed deeper analysis of complex systems maximum
efficiency. For modeling system we have used Petri nets because we have in our case discrete event systems. In
use of the non-timed and with auxixliary times Petri model, the transport stream was divided into sections, and
these sections will be analyzed successively. Due to the complexity of the system and the large amount of
calculations required it was not possible to analyze the system as a unitary whole. A first attempt to model the
system as a unitary whole led to the blocking of the model during simulation, because of the large processing
times.
Keywords: Petri nets, transport, processing
LINEAR PROGRAMMING MODEL
Mathematical programming models and especially their subclass, linear programming
models, plays an extremely important role both in theory and in practice Error! Reference
source not found..
The theory benefited from the contribution of the interdisciplinary approach which
allowed: further analyzing the maximal efficiency of complex systems, the discovery of new
concepts of optimum, it has perfected the methods of research and knowledge, and the
practice has been enriched with an extremely useful instrument for analysis and substantiation
decisions.
The structure of general linear programming model is established primarily by the set of
activities {A1, A2, ... An} that compose the analyzed system, the set of used resources {R1, R2,
... Rm} as well as technical relations between these. The relationship between activities and
resources is determined by the manufacturing technology for each activity Aj (j=1,...,n) and
may be characterized numerically by the column vector a(j)
with components (a1j, a2j, ... amj).
The elements {aij, i = 1,...,m; j = 1,...,n} are called technical coefficients or specific
consumption coefficients and show how much of the resource Ri is consumed to produce a
unit of the product Pj (as a result of the activity Aj). All the manufacturing "technologies"
defined by the column vectors a(j)
can be organized in a matrix A with m lines and n columns;
each line refers to a resource Ri (i = 1,...,m) and each column relates to an activity Aj (j =
1,...,n).
Denoting by xj (j = 1,...,n) the result of Aj in a given period and bi (i = 1,...,m) available
quantities of resources Ri (i = 1,...,m), the following technical restrictions can be written
mathematically:
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228
mnmn2m21m1
2n2n222121
1n1n212111
bxa...xaxa
bxa...xaxa
bxa...xaxa
or Ax b (1)
where
nnmnmm
n
n
b
b
b
b
x
x
x
x
aaa
aaa
aaa
A...
si ...
;
...
............
...
...
2
1
2
1
21
22221
11211
(2)
Each inequation / restriction incorporates two statements:
- the amount of a resource consumption can not exceed the amount available;
- the total consumption Rij of resource Ri for the activitiy Aj is proportional to the
intensity, i.e. xj, so
jijij xaR (3)
The system of restrictions described above makes the link between resources and
activities through the m linear restrictions.
The linear programming model 0 contains restrictions on the type (1) as well as a
criterion for "performance" to assess the effectiveness of each activity. Depending on the
purpose, we can choose as a criterion of efficiency an indicator that measures the effort, one
that measures the result or an indicator expressed as the ratio between result and effort.
The maximum efficiency means minimizing the effort and maximizing the outcome,
and the concept of optimum is defined as a program that minimizes or maximizes an objective
function and in the same time satisfies all technical restrictions.
Assuming that each component of the vector line c = (c1, c2, ..., cn) measure the
efficiency of a unit of the result of Aj, then we can introduce the linear function:
nn xcxcxcxf ...)( 2211 (4)
assessing the performance of any program x.
Summarizing, we obtain the following linear programming software:
)(xfoptimx
(5)
(6)
(7)
(8)
The relations (5), (6), (7) and (8) together constitute the general model of a linear
programming problem, each having a specific role:
(1)
(2)
(3)
njx
mIIIkbxa
mIIIibxa
j
n
j
kjkj
n
j
ijij
,1 0
,...,2,1 unde
,...,2,1 unde
1
212
1
211
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229
- the relation (5), where f(x) =
n
1jjjc x is called the objective function for efficiency of
the problem, evaluates the performance of each program options x;
- the relation (6) by type
n
1jijij bxa represents resources type restrictions;
- the restriction (7) such
n
1jkjkj bxa it refers to the technical restrictions qualitative;
- the relation (8) xj 0 j = 1,...,n called the non-negativity variables condition, ensures a
feasible solution from the point of view of economic logic.
In the case of determining optimal production assortment structure, are known the
available quantities of each raw material bi, the technological coefficients aij, the maximum
quantities jx and the minimum
jx that can be produced from each assortment in the analyzed
period and the unitary profits pj, for each type of product.
The general dynamic model of manufacturing system is given by the matrix vector
equation:
x k
x k
x k
A A A
A A A
A
A A A
x k
x k
x k
B B B
B B B
B
B B B
u k
u k
u k
f x k u
n
n
n
ij
n n nn n
n
n
ij
n n nn n
1
2
11 12 1
21 22 2
1 2
1
2
11 12 1
21 22 2
1 2
1
2
1 11
1
1
.
.
.
. . .
. . .
. . . . . .
. . . . .
. . . . . .
. . .
.
.
.
. . .
. . .
. . . . . .
. . . . .
. . . . . .
. . .
.
.
.
,
1
2 2 2
k
f x k u k
f x k u kn n n
,
.
.
.
,
(9)
and so x k A x k B u k f x k u ka ij a pq a 1 , (10)
1, , , , , , , , , ,n i j n n p q n m i j p q (11)
where x k 1 is the matrix of system conditions at the time of t x k 1 , and u k
are the matrices of states and inputs at time t , Aij is the interaction matrix Sb j with Sbi
influencing state x k 1 of the entire system, Bpq - the interaction matrix between u kq
and x kp in which u k x kq
f
p
pq influencing state x k 1 of the entire system,
f x k u k , (12) – the internal interaction matrix between the states x t and their inputs
u t of the entire system in time t , that influence the state x t 1 of the entire system in
the next moment t 1 .
The order of matrix A n nij l c, , is given by the product of the number of each of the
kinematic couplings Sbc and the number of state parameters of each coupling. The elements
aij are linear and nonlinear expressions.
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The elements bpq are determined by the rule:
0 then ),( influencesnot )(
0 then ),( influences )())(),((
pqpq
pqpq
qppqbkxku
bkxkukukxf (13)
This rule also applies to the matrix elements (12).
The equations of state are subject to the conditions and restrictions:
- for S continue t
- for S discrete t k t Te
e
Ne
,1
;
if t cte then T N te e ,
- 0x – a initial state known of S , and x xa0 0 for ,
- R x k u k , 0, R expressing a set of restrictions in the matrix (12),
- k q x k , and 0 0 0 q x for .
ANALYSIS AND INTERPRETATION SYSTEM
The sequence of events is reduced to a simple ordering of their occurrence. The
simulation involves the consecutive execution of transitions, according to the enforcement
rule of transitions Error! Reference source not found.0 Error! Reference source not
found..
SECTION II with auxiliary times:
Fig.1: Petri net SECTION II with auxiliary times:
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231
By using the generalized stochastic Petri net, it obtains the model of the production
system to be analyzed. The execution durations of transitions are distributed using an
exponential law which allows obtaining a graph of the Petri net marking, and this is an
homogeneous Markov process. In the timed Petri nets it is considered that the viable and
marginal properties are some of the most important in the distributed system under review.
The results obtained contribute to finding and studying a large number of timed Petri nets for
which it can produce an effective analysis.
By adopting a new location are reduced the transportation distances. The ovens are
situated on the line making it easier for the administration of cargo passing through the ovens.
The packaged goods do not have to enter in the box and crowding the existing space. A
summary of the presented simulation results is indicated in the following tables.
The results shown in the tables above are obtained when using the simulation of a
number of 1300 iterations.
The second model is applied to section 2 P-timed, deployed in a time of 12,055,273 sec.
for the existing model, and 11756868 sec. for the proposed model with a number of 1300
events. In the figure are shown only the fields that change its value. At this section the actual
time of transport is 81.82 min. and the transportation time obtained from the application of the
new location is 82.70 min. Model: Section 2 with timed positions.xml
Events:1302
Time:12055273
Place Name Arrival Sum Arrival Rate Arrival Dist. Throughput
Sum
Throughput
Rate
Throughput
Dist.
Waiting
Time
Queue
Length
Vagonet disponibil 68 5.6407e-006 177283.4265 69 5.7236e-006 174714.1014 2799.8261 0.016025
Incarcare Vagonet 69 5.7236e-006 174714.1014 69 5.7236e-006 174714.1014 15 8.5855e-005
Transport Vagonet 69 5.7236e-006 174714.1014 69 5.7236e-006 174714.1014 60 0.00034342
Vagonet neutilizat 69 5.7236e-006 174714.1014 69 5.7236e-006 174714.1014 174654.1014 0.99966
Descarcare in Stocator 1 69 5.7236e-006 174714.1014 69 5.7236e-006 174714.1014 15 8.5855e-005
Stocator 1 69 5.7236e-006 174714.1014 69 5.7236e-006 174714.1014 15 8.5855e-005
Spatiu 1 69 5.7236e-006 174714.1014 69 5.7236e-006 174714.1014 174699.1014 0.99991
Incarcare in Cuptor 69 5.7236e-006 174714.1014 69 5.7236e-006 174714.1014 4320 0.024726
ARDERE BISCUIT 69 5.7236e-006 174714.1014 69 5.7236e-006 174714.1014 86400 0.49452
Ardere neutilizata 69 5.7236e-006 174714.1014 69 5.7236e-006 174714.1014 88314.1014 0.50548
Descarcare din Cuptor 69 5.7236e-006 174714.1014 69 5.7236e-006 174714.1014 30 0.00017171
Transport cu Vagoneti 69 5.7236e-006 174714.1014 69 5.7236e-006 174714.1014 60 0.00034342
Vagoneti neutilizati 69 5.7236e-006 174714.1014 69 5.7236e-006 174714.1014 174654.1014 0.99966
Incarcare pentru Biscuitare 69 5.7236e-006 174714.1014 69 5.7236e-006 174714.1014 30 0.00017171
BISCUITARE 69 5.7236e-006 174714.1014 68 5.6407e-006 177283.4265 81000 0.4569
Biscuitare neutilizata 68 5.6407e-006 177283.4265 69 5.7236e-006 174714.1014 94888.0145 0.5431
Descarcare de la Biscuitare 68 5.6407e-006 177283.4265 68 5.6407e-006 177283.4265 15 8.461e-005
Stocare 2 68 5.6407e-006 177283.4265 68 5.6407e-006 177283.4265 15 8.461e-005
Spatiu 2 68 5.6407e-006 177283.4265 68 5.6407e-006 177283.4265 177268.4265 0.99992
Descarcare pentru transport vagonet
68 5.6407e-006 177283.4265 68 5.6407e-006 177283.4265 15 8.461e-005
Transport vagonet 68 5.6407e-006 177283.4265 68 5.6407e-006 177283.4265 60 0.00033844
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232
vagonet neutilizat 68 5.6407e-006 177283.4265 68 5.6407e-006 177283.4265 177223.4265 0.99966
Incarcare dispozitiv
Glazurare 68 5.6407e-006 177283.4265 68 5.6407e-006 177283.4265 15 8.461e-005
GALZURARE 68 5.6407e-006 177283.4265 68 5.6407e-006 177283.4265 720 0.0040613
Glazurare neutilizata 68 5.6407e-006 177283.4265 68 5.6407e-006 177283.4265 176563.4265 0.99594
Descarcare 68 5.6407e-006 177283.4265 68 5.6407e-006 177283.4265 120 0.00067688
Transport vagon 68 5.6407e-006 177283.4265 68 5.6407e-006 177283.4265 200 0.0011281
vag neutilizat 68 5.6407e-006 177283.4265 68 5.6407e-006 177283.4265 177083.4265 0.99887
Fig. 2: Global performance indicators relating to the positions in the SECTION 2 model, considered with
stochastic time delay by type P
Model: Section 2 with timed positions.xml
Events:1302
Time:11756868
Place Name Waiting Time Queue Length
Vagonet disponibil 2799.8261 0.016432
Incarcare Vagonet 15 8.8034e-005
Transport Vagonet 45 0.0002641
Vagonet neutilizat 170344.3913 0.99974
Descarcare in Stocator 1 15 8.8034e-005
Stocator 1 30 0.00017607
Spatiu 1 170359.3913 0.99982
Incarcare in Cuptor 15 8.8034e-005
ARDERE BISCUIT 86400 0.50707
Ardere neutilizata 83989.3913 0.49293
Descarcare din Cuptor 15 8.8034e-005
Transport cu Vagoneti 90 0.0005282
Vagoneti neutilizati 170299.3913 0.99947
Incarcare pentru Biscuitare 15 8.8034e-005
BISCUITARE 81000 0.46849
Biscuitare neutilizata 90563.3043 0.53151
Descarcare de la Biscuitare 15 8.6758e-005
Stocare 2 30 0.00017352
Spatiu 2 172865.1176 0.99983
Descarcare pentru transport
vagonet 15 8.6758e-005
Transport vagonet 45 0.00026027
vagonet neutilizat 172850.1176 0.99974
Incarcare dispozitiv
Glazurare 15 8.6758e-005
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GALZURARE 720 0.0041644
Glazurare neutilizata 172175.1176 0.99584
Descarcare 120 0.00069406
Transport vagon 180 0.0010411
vag neutilizat 172715.1176 0.99896
Fig. 3: Global performance indicators relating to the positions in the SECTION 2 model, considered with
stochastic time delay by type P
CONCLUSIONS
The simulation of the proposed manufacturing system using timed Petri nets, offers the
possibility of viewing over time the manufacturing process.
Applying product manufacturing times and transportation times obtained by measuring
the spot, it is obtained graphical representations that show the average times of transport
activity, but also the evolution of the average time of processing related to the transport
activity time, using as parameters sets of finite products.
REFERENCES
1. Abrudan Ioan, „Sisteme flexibile de fabricaţie. Concepte de proiectare şi
management‖, Editura DACIA, 1996, ISBN 973-35-0568-4
2. Bauşic Florin, „Dinamica maşinilor de construcţii‖, Editura MatrixRom, Bucureşti,
2001, ISBN 973-685-229-6
3. Bejan Andrei, „Modelarea timpului de orientare în sisteme de aşteptare cu priorităţi‖,
Teza de doctorat, Chişinău, Septembrie 2007, Universitatea de Stat din Moldova,
Facultatea Matematică şi Informatică
4. Camerzan Inga, „Proprietăţi structurale ale reţelelor Petri temporizate‖, Teza de doctor
în informatică, Universitate de Stat din Tiraspol, Chişinău, 2007-12-15
5. Mihăilă N., „Introducere în programare liniară‖, Editura didactică şi pedagogică,
Bucureşti, 1964
6. Păstrăvanu Octavian, Matcovschi Mihaela, Mahulea Cristian, „Aplicaţii ale reţelelor
Petri în studierea Sistemelor cu evenimente discrete‖, Editura Gh. Asachi, 2002, ISBN
973-8292-86-7
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AN EXTREMAL PROBLEM FOR UNIVALENT FUNCTIONS
Professor dr. Miodrag IOVANOV, ―Constantin Brâncuşi‖ University of Târgu-Jiu,
Abstract: 1. Let K be a compact class of functions of the form
f(z)=z + a2z2 +………. (1)
which are regular and univalent in the unit disc U and let p and a be complex numbers,
p 0; p 1; 0 < |a| < 1.
For f K, p and a fixed, the equation
f(z) = pf(a) (2)
has at most a solution zf in U.
If p = 0 or p = 1, then for any f K the equation (2) has only the solution z = 0 or z = a
respectively. We will exclude the case p = 0 or p = 1 and consider the following extremal problem:
given K, p and a, p 0; p 1; 0 < |a| < 1, determine
m(p; a; K) = min{: = |zf|, f K} (3)
This problem was first considered by p. T. MOCANU [4] who solved it for the whole class
S of normalized univalent functions.
I. KACZMARSKI [3] obtained m(p, a, K) for K = SR, the subclass of S consisting of
functions with real coefficients and K = S, the class of starlike functions. L. BURSHTEIN [1]
solved this problem for K = TR, the class of tipically real functions and for some other classes
represented by Stieltjes integrals [2]. M. READE and E. ZTOTKIEWICZ [7] obtained m(p,a,K)
for K =
S , the class of starlike functions of order , K = S°, the class of convex functions and
also for K = TR, by using a different method.
In this paper we consider the following more general problem: given K, a, 0 < |a| < 1,
and the polynomial pn(z) = cnzn + Cn-1z
n-1 + ……+ c0, where c0 0, c, are complex numbers,
determine
m(c0; c1…..cn; a; K) = min{: = |zf|, f K } (4)
where zf satisfies the equation
f(z) = pn(z)f(a) (5)
We‘ll solve this problem for K =
S , K = Sc and K = TR.
We recall that the function f of the form (1) is starlike of order ; 0 < α < 1, iff
)(
)(Re
'
zf
zzf , z U (6)
The class of such functions shall be denoted by
S …..
0S = S is the class of starlike
functions.
A function f of the form (1) is convex iff
0)(
)(1Re
'
"
zf
zzf , z U (7)
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The class of such functions shall be denoted by S°.
A function f of the form (1) is tipically — real iff f(z) is real if and only if z (-1; 1).
The class of such functions shall be denoted by TR.
2. If K, z and a are given, the set
Kfzf
zf;: K) z, D(a, (8)
is called the domain of variability of f(z)/f(a) for the class K. If p, a, K are given, then (2) has
a solution if and only if p D(a, z, K), z U.
We need the following lemmas :
Lemma 1. [7] The domain of variability of
112,
azf
zaf for the class
S
is the closed disc
22
1
1
1
1
zz
za
(9)
Lemma 2. [5]. The domain of variability for the class TR is the convex hull of the set
22;: TR) z, D(a,1
1
ttzz
taa (10)
We will find (4) by using the condition pn(z) D(a,z,K) for
S , S*, S° and TR
3. For the class
S we have the following result
THEOREM 1. If c0, c1,..., cn are complex numbers, c0 0; 0 < |a| < 1
and then,121
zap
zaz
zap
zzSacccm
nn
n 1:inf,,,.......,, 10 (11)
Proof. We put the condition pn(z) D[a, z,
S ).
Using Lemma 1 we deduce that the solution z of (5) must satisfy the condition
2211
1
z
az
z
za
z
zapn
(12)
which can be written in the following form
zap
zaz
zap
z
nn
1 (13)
From this we easily get (11).
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236
For 12
1 we obtain
zap
zz
zap
zzSacccm
nn
n 1:inf,,,.......,,2
110 (14)
If we take c1 = c2 = …. = cn = 0; c0 = p we get
11
,,2
1
pa
paSapm (15)
The extremal function is f(z) = z(1 + ei·z)
-1; = arg a(p-1). Since f is convex we deduce
11
,,
pa
paSapm c (16)
This result is due to M. READE and E. ZLOTKIEWICZ [7]. If α = 0, from (11) we get
zap
zz
zap
zzSacccm
nn
n 1:inf,,,.......,, 10 (17)
If we take c0 = p, ci =0, i = 1,2, …,n, we deduce
12
11
2
121,,
2222
ap
paa
ap
paaSapm (18)
The extremal function in this case is f(z) = z(1-ei
·z)-2
. This result is due to
KACZMARSKI [3].
4. Let K = TR and consider the equation (5), where pn(z) = cnzn+…+c0, ci are real, c0 0,
pn(a) 1, z is real and -1 < a < 1.
In this case we nave the following result:
THEOREM 2. If ci, i = 0,1,…,n, are real numbers c0 0 and 0 < a < 1, then
,min,,,.......,,
1
110 zTRacccm
zn
(19)
where z and , satisfy the equations
01
12
a
zzp
a
zn (20)
and
01
12
ap
an
(21)
respectively. The extremal functions are f(z) = z(1-z)2 and f() = ·(1 +)
-2 respectively.
Proof. We put the condition pn(z)D(a, z, TR).
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Using Lemma 2 we deduce
2,2,1
1
ttzz
taazpn (22)
Hence our problem is to find the minimum of |z| where z verifies (22).
If we let A = a + a-1
the equation (22) can be written
012 ztAzptzz n (23)
The solution of this equation will be a function of t, z = z(t); t [-2; 2].
If at a point t (-2; 2), z(t) has an extremal value, then z’(t) = 0. If we take the
derivative in (22) and put the condition z’(t) = 0, we deduce z(t)[pn(z(t))-1] = 0.
Since f is univalent on (-1,1), pn(z)=1 and f(z) = pn(z)f(a) imply z = a. This contradicts
pn(a)1. Hence z(t) = 0. But this holds only for c0 = 0 which contradicts our hypothesis.
Hence the only points where z has an extremal value are t = ±2. This completes the proof of
Theorem 2.
The equation (22) can be written
zpz
Azzpzt
n
n
1
12
(24)
Remark. Consider the case c0 = 1 and n = 2m + 1.
The polynominal qn-1(z) = c1 + c2z + … + cn2n-1
is of even degree 2m.
In [6] T. POPOVICIU has given sufficent conditions for the positivity of a polynomial
of even degree. Using these conditions we get:
THEOREM 3. If
1,...,1,0,0,0 2
2232121 miccc iii (25)
where
3
2cos
1
2
n
, then in the class TR we have
0
1
1:min,,,.......,,
2
110
a
zzp
a
zzTRacccm n
zn (26)
The extremal functions is the Koebe function
21 z
zzf
(27)
We shall apply Theorem 2 to the particular case: c0 = p; c1 = q; c2 = c3 = … = cn = 0.
In this case the equation (5) becomes
f(z)=(p+qz)·f(a) (28)
From Theorem 2 we deduce that the minimum of |z| is obtained for z = ±2.
Equation (24) becomes
qzpz
pzAqpzqzt
1
23
(29)
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Suppose 0 < a < 1. Then we have
THEOREM 4. If 0 < p ≤ 3
2, 0 < q <
3
1 then in the class TR we have
m(p; q; a; TR) =
z (30)
where
z is the smallesi positive root of the equation
0122 23 pzpAqzqpqz (31)
The extremal functions is the Koebe function 21 z
zzf
Proof. The graph of the function defined by (29) has the following form (fig.1).
We remark that
z (0, 0
z ) where 0
z is the solution of the equation (29) for t = 0 i.e. the
solution of
023 pzAqpzqzzg (32)
Since
g(0) = p > 0, (33)
g(1) = 2(p + q)- A < 0 (34)
and
1,2(010 1 qpaaAgg ), (35)
we deduce 0
z (0;1).
Fig. 1.
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239
Example. For p = q = a = 7
1 we get m (
7
1,7
1,7
1,TR) 0,02.
THEOREM 5. If 0< p <1; q > 3
1; p + q <
2
A then in the class TR we have
zzTRapm
z
z,min,,
1
1 (36)
where
z is the smallest positive root of the equation (31) and 0
z is the biggest negative root
of the equation
0122 23 pzpAqzqpqz (37)
The extremul functions are f(z) = z(1 + z)-2
and f() = (1-)-2
respectively.
If p, q, are real numbers, we deduce :
THEOREM 6. If p, q are real numbers, 0 < a < 1, then in the class TR we have
,min,,,
1
1zTRaqpm
z
(38)
where z and , are the Solutions of (31) and (37) respectively.
The extremal functions are f(z) = z(1 + z)-2
and f() = (1-)-2
respectively.
REFERENCES
[1] Burshtein, L., Roots of the equation f(z) = αf(a) for the class of typically — real
functions. Mat. Zametki 10, 41-52 (1971).
[2] Burshtein, L., The solution of the equation f(z) = αf(z) in the class of star — shaped
functions, Izv. Vyss. Ucebn. Zaved. Mat., no., 12 (151), 47-50 (1974).
[3] Kaczmarski, I., Sur l’equation f(z) =pf(c) dans la famille des functions univalentes á
coefficients reels, Bull. Acad. Pol. Sci, vol. XV, 4, 245-251 (1967).
[4] Mocanu, P. T., On the equation f(z) = αf(a) in the class of univalent functions.
Mathematica vol. 6 (29), 1, 63-79 (1974).
[5] Pilat, B., On typically — real functions with Montel’s normalization,. Annales UMCS,
XVIII, 53-72 (1964).
[6] Popoviciu, T., Sur une condition suffisante pour qu’un polynom soit positif, Mathematica,
vol. XI, 247-256 (1935).
[7] Reade, M. O., Zlotkiewicz„ E., On the equation f(z) = pf(a) in certain classes of analytic
functions. Mathematica vol. 13 (36), 2, 281—286 (1971).
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240
BOOLEAN NORMED ALGEBRAS
Prof.Drd. Constantin P. BOGDAN
Universitatea din Craiova
As.univ. Olimpia PECINGINA
Universitatea ―Constantin Brancusi‖ ,Tg-Jiu
ABSTRACT: In this section we begin a systematic study of algebras given by algebraic measures.Knowing that
the measure is an essential positive total additive function.The most important lesson is made up of probability
measures.Each algebra with measures of probability can be interpreted as a system of events, with the measure
itself as the probability of this system.The bulk of it in the next chapters allow the translation in the language of
probability theory.
ALGEBRE BOOLEAN NORMATE
1. standardized Algebra 1.1 Definition and its properties of Boolean algebra normed
topological definition. A Boolean algebra (abbreviated normata ABN ) is a pair , ,
where is complete and AB is the measure of . Through the routine of the language,
we'll talk often about a "ABN ". If It is a measure of the probability then sometimes
use the term algebra to probability. As is always the outer measure.Therefore, all statements
for Boolean algebra complement proven with external measures applied to an ABN.In
particular, each ABN , turns into a metric space with metric
: ,x y x y . (1)
Considering that the measure is totally additive, nx involve ,© 0n np x x .
Indeed,
1 ,n k kk n
x x Cx
1 n k k
k n
x x Cx
. (2)
Theorem 1. The Topology the metrical of a on coinciding with the topology ( )o .
This theorem is a special case. It is enough to recall the fact that the metric topology
satisfies the condition ( )os .
Corollary 1. Either si two measures on a AB complete.Then for each 0 real,
there are 0 so that the inequality x involve x .
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To prove it is sufficient to observe that the relationship 0nx and 0nx , in
virtue of the theorem 1, expressing the same thing: convergence in topology from scratch ( ).o
This convergence can be called "convergence to the extent".It is obvious that each measure is
a function. Corollary 1 looks like this concept of absolute continuity, while important for a set
of functions, it becomes useless in our case. For each AB complete all the steps, admits
metric spaces , are homeomorfe to each other.
Corollary 2.
Because the relationship 0nx keep it off, it is necessary and sufficient that each absolute
increase of indices kn There is a joint 1 2( ...)kin k k so ( )
©ki
o
nx .
In fact, the coincidence of topology ( )o si ( )os It is sufficient to refer to the corollary of
Theorem 1 2 shows us that each sequence kn anulandu-it contains a joint to the extent ( )o
convergence knx . This statement can be made more precise method of choice highlighting
such consequential: a convergence ( )o It is enough that the series 1k
knx converge.
We demonstrate that.
Lemma 1. If 1i
iy then ( )
©o
iy .
Demonstratie.Se Yes m and si k , We have m km k
i ii m
i m
y y
i
i m
y
.
Considering that so far as is ( )o - continue:
i ii m
i m
y y
(3)
The right side of this inequalities disappears: 0 lim inf 0i i i imm i i m
i m
y y y
(4)
The right side of this inequalities disappears: 0 lim inf 0i i i imm i i m
i m
y y y
Considering that the measure is essentially positive, we see that lim ©i iy or
( ) lim ©o y
Lemma is proved. Using this Lemma, we consider the problem of complete metrics of a
Boolean algebra.
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Teorema 2
A AB complete with metric It is a complete metric space.
Demonstration
Fie 1n nx
a Cauchy sequence which comply with . We can choose a joint
1 1 2 ...kn kx n n
so series 11 ,
k kk n np x x
1
,©k kn np x x
converged.
Therefore, according to Lemma 1,1
( )
k k
o
n nx x x
. So, we have
© limnk
x lim 1
lim ©.n k kk
x n nx x
Therefore, there is an element x so ( )
k
o
nx x . Now, the inequality
,( ) ( , ) ( , )k kn n n nx x x x x x We can easily notice that
( )
,( ) 0o
nx x taking into account that
1n nx
is a Cauchy sequence. It has been demonstrated that ,x is complete.
Observation. Theorem 2 remain valid if is a foreign measure, to demonstrate, it is
sufficient to slightly change the proof Theorem 2.
1.2 its properties of a converged ( )o
Starting from Lemma 1, it is easy to demonstrate another important theorem expressed by m.
Frechet.
Theorem 3 Every ABN is regular. I actually set a fact even more generally: regularity of the algebra.
Thus, each can be considered a ABN space metric. What else can we say about the properties
in this space? For example, will be connected? The answer is negative, in general, since some
lie algebras are normed listed all finite AB, which are clearly disconnected.
Theorem 4 An ABN is a metric space continue connected in the shape of an arc. This theorem implies, in
particular, that the set of values in a measure coincide (in accordance with the terms of the
theorem) with the range[0, 1] . But this has been proven previously: base is a Theorem
Demonstration 4 follow now. So either two elements 0 1,x x x database. We will build a
path between these elements. This is done in a few steps. 1. Show that for all , ,u v u v
There are w so 12
( , ) ( , ) ( , )u w w u v .Suppose u u Cv şi v v Cv .
These elements are disjoint, but not equal to zero at the same time and
( , ) ( , )u v u v u v u v u v (5)
Let's assume that for the determination of 0u si u v . (6)
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Moreover, we can consider the 0 with all quasimasurile regulated by condition
of ( ) 1. 1 It is clear that 0 0.K These categories (and their subclasses) are listed in
mathematical statistics "statistical structures." We will build some elements u şi v with
the following properties: 1 12 2
, , , .u u u v u u v v
We Place .w u v u v Then 1 12 2
( , ) ( )
( ) ( , ).
w u u u v
u v u v
Similarly 1
2( , ) ( , )w v u v .
2. Now, knowing that 0u x si 1v x as we build the item above 01w x a which distance
between 0x and 1x is 10 12
( , )x x In addition, we define 001x and 011x also, continuing this
process we will apply our crowd of AB has all the numbers 0 1( , )r x x , where [0,1]r
dyadic rational-it. Moreover, such a built function 0 is uniformly
continuous: 0 0, .p t t t t
3. We remain to extend this application continuity through the whole range 0, 1)0, ( .x x
Get some continuous functions that apply in AB such that 0(0) x and
0 1 1( ( , )) .x x x It's a good trajectory between points 0x and 1x .
The demonstration is complete. We will add to this very important Observation. in an ABN
form each lot continues |M x x
It is connected in the shape of an arc, 0, 1 .
The proof of the theorem is clear that: u v a then .w a The Crowd M is
closed.That's why each trajectory What unites 0 1,x x M lies entirely in .M
This observation will allow us later to demonstrate his famous Theorem of Lyapunov vector
measures about. Definition: a complete AB is called normata if it admits a few steps. Each
normata holds many measures AB in general; but are equivalent in some places such as the
corollary of the theorem 1 shows 1: define the same topology, topological order
metric.Theorems 3 and 4 are obviously valid for lie algebras normed. In essence, a normata
is a AB AB analyzed together with complete system of measure . Moreover, it is
considered that the system is not empty.From now on we will recover through ( )M M .
Also consider the set K of all total additive on quasimasurile . Each of these is a continuous
function quasimasuri.If v K then the crowd | 0x vx is an ideal of the form u .
Quasimasurilor restriction v the complementary area Cu It is a measure.Usually we
consider probability measures satisfying the condition 1. 1 We note the probability
measures with ( ).oM Similarly we will put Moreover, we can consider the 0 with all
quasimasurile regulated by condition of ( ) 1. 1 It is clear that 0 0.K These
categories (and their subclasses) are listed in mathematical statistics "statistical structures."
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1.3 The ABN Izomorfisme
Either , and ,v the two ABN. An application f on poset E (for example, a
subalgebra or area) It is called as constanta v f x x for all .x E First of all we are
interested in homomorfism and isomorphism.Talking about a homomorfism or homorfism of
the , on ,v , We always refer to it as homomorfismul (izomorfismul) keeps his
on . The method is often useful in izomorfismelor.
The following theorem relies on this method.
Theorem 5.
If 0 and 0 There are two subalgebre of everywhere and ( )o - dense
then each measure constant monomorfismului 0 of 0 on 0 extends to a measure of
constant izomorfismului 0 of 0 on 0 . Such an extension is unique.
Demonstration.
Lie Algebras and I'm a regular. Constant-mean that measures homomorfismele 0 si 1
0
satisfying the condition ( )E . Indeed, either: 1
,nn
x x
0., nx x
If: 1 1x x , 2 2 1,x x Cx 3 3 1 2 ,....x x C x x Then
0 0 0
0 .
n n nn n
n
n
n
v x v x v x
x x v x
Hence, 0 01
.nn
x x
The last equality says that that condition ( )E is fulfilled. In our case it involves ( )E
.
Thus, homomorfismul 0 satisfies the condition ( )E
. By analogy, we will check if this
condition is satisfied for the 1
0 .AB and meet the condition; It is easy to see, for
such terms of algebras ( )E and ( )E
are equivalent to ( )E and ( )E
In this case, the extension of monomorfismului 0 is an isomorphism on . Show
that it is able. For each x There is a sequence nx in 0 converging at x .. Passing to
the limit in the relationship 0 ,n n nv x v x x (7)
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We arrived at the desired equality .v x
The uniqueness of an extension obtained thus is obvious. The demonstration is complete. We
will cite two examples in which the theorem applies to 5. In these examples and There
are two normed algebras. And and v There are two measures of the probability of these
algebras.
I. Be and containing compact and autonomous subalgebre everywhere 0 and that 0
. Let's say these subalgebre include not only of systems alternators, but also (considering
some measures and v ) with the same power.Either 0
E an independent system of
generators for 0 and either 0
E an independent system of generators v for 0 .
Finally, we assume for simplicity that
12
x vy
for all 0
x E and 0
E . In this case, each of which applied to each from 0
E on 0
E
an isomorphism is extensive 0 None of his 0 on 0 . It is easily checked that this
measure is isomorphism. In fact, if
1 2 ... ,kx x x x (8)
where 0 0
1,2,...,ix E CE i k iar i jx x for i j then 1
2kx At the same time
0 1 2 ... ,kx x x x (9)
si de asemenea 0 0
1,2,..., ,i xx E CE i k i jx x pentru .i j Asadar
10 2
.kv x x
We must take into account the fact that each element of 0 It is a finite sum of
elements of disjoint form (1). Thus, by Theorem 5, there is a constant measure of
izomorfismului on .
II. Now let's consider a typical situation when there are two pairs of regular subalgebre
,
and ,y y with the following properties:
1) ( )x x x x
for any x
and x ; in a similar way
( )v y y vyvy for any y si y ;
2) ,
and
,
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Suppose there are izomorfisme with constant measures and many of his
on
and that of on . We show that in this case there is an isomorphism with the
constant measure None of his on by extension of and .
To this end, we introduce subalgebrele 0 ,
and 0
, .
To this end, we introduce subalgebrele 0 ,
and 0
, . If 0
and 0 , It is sufficient to construct an isomorphism with the constant measure of 0 pe
0
CONCLUSIONS
The main issue is topical because it approaches the fuzzy systems underlying the artificial
intelligence that is implemented in the economic and industrial machines.
REFERENCES
[1] Balbes si Dwinger,The curatours of the University of Missouri,1974
[2] Dumitru Buşneag ,Categories of Algebric Logic, Editura Academiei
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247
EXTENSION OF AN ADDITIVE FUNCTIONS NUMARABILE
Prof.Drd. Bogdan P. Constantin
Universitatea din Craiova
As.univ.Pecingina Olimpia
Universitatea ―Constantin Brancusi‖ ,Tg-jiu
ABSTRACT: All measures to start the construction of theories from user a fundamental theorem of a. Lebesgue
whose contemporary formulations is due to c. Caratheodory.
NORMED ALGEBRAS
Lebesgue Theorem Caratheodory-Demonstration.
Either o AB complete.We consider subalgebra 0 with a quasimasura . We
will now undertake the following tasks: construction of a subalgebras regular
that
includes 0 and a quasimasura additive numarabila
on
so x x
, where it is
possible, x x
for any x 0 . In order to accomplish the task, we will define an
outer quasimasura by associating with each .x the crowd xS that is all most families
numarabile 0 satisfying the condition sup x , and by:
inf xS
.
The Demonstration. Either a AB complete.We consider subalgebra 0 with a
quasimasura . We will now undertake the following tasks: construction of a subalgebre
regular
that includes 0 and a quasimasura additive numarabila
on
so
x x
, where possible, x x
for any x 0 . In order to accomplish the task,
we will define an outer quasimasura by associating with each .x the crowd xS that
is all most families numarabile 0 satisfying the condition sup x , and by:
inf xS
.
We note the main characteristics of this external quasimasuri.
1. If 0 0x x then x 0 .x
This property is obvious.Implies that is finite.The following property is also evidence
2. Outside measurement este monotona: x involve x .
3. If kx x then x .k kx
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Considering that the measure is totally additive, nx Indeed, involve establishing a
chance 0 , associated with each kx family k xS so that the inequality
2k
k
kx
remains.Clearly, gender equality k k belongs to xS ;
and, that's why
x
kk k
x
.
Because is random, we obtain the inequality. Now we arrange the
with all the elements
x so equality
( ) ( ) ( )xu x u C u (4)
keep for any u . It is clear that always ( ) ( ) ( ),xu x u C u so we no longer
stays than to validate the seeming inequality backside.
Lemma 2.Either 1,2...nZ n
si be the sequence nZ What tends to repeat .z Then
( ) lim ( )nn
u z u z
for any .u
Demonstration. Everything is obvious nz decreases.Suppose that nz z and 1 ©.z Then
complete all the steps, admits metric spaces , are homeomorfe to each other.
1 11 1
( )nn n n z
n n
u z u z z u z C
11
lim .
n nn
nn
u z u z
u z
Lemma is proved.
Lemma 3. The Crowd
is a subalgebra on regular basis.
Demonstration.
In condition of the main (4) items x si xC have equal status, so
contains each element
together with the complementarul or. Is Yes ,x y
and we have z x y cu .u
We will have
( ) ( ) ( )xu u x u C
( ) ( )
( ) ( )
y
x x y
u x y u x C
u C y u C C
( )
( ) ( ) ( )y x x y
u x y
u x C u C y u C C
( ) ( ),zu z u C
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Since ( ) ( ) ( )x xu x C u C u C C
( ) ( )
.
x x
z
u x C C C C
u C x u C
Thus .z
Note that
is the subalgebra. We remain to show that
is on a regular
basis.Either 1 2, ,..., ,...nx x x a
numarabila and submultime m k
ii m
x y
m km k
i ii m
i m
y y
i
i m
y
.
Considering that so far as is ( )o - continue:
In the previous Lemma,
( ) lim ( ),nn
u x u y
( ) lim ( )nx y
nu C u C
Hence, ( ) ( ) ( ).xu x u C u
Thus, .x
It has been demonstrated that
is a subalgebra on regular basis.
Lemma 4 0
Demonstration. Either x 0. Choose an item u and a correspondent by chance uS .
Families of elements of the form x z z and xC z the corresponding elements
are x u and that .xC u
So ( ) xz z
z z x z C
( ) ( ).
xz z
x
z x z C
x u C u
Taking into account that by chance, we conclude that ( ) ( ) ( )xu x u C u
Thus, .x
Axiona is demonstrated.
Lemma 5. If ( ) 0x then .x
Demonstration.Se Yes u , as a result ( ) ( ) ( )xu x u C u ( )
©ki
o
nx .
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250
In fact, the coincidence of topology ( )o and ( )os It is sufficient to refer la Theorem 4
Suppose that ,x y
and x d .y Atunci
x
x y x y
x y x x y C
( ) ( )x y
x
.y
So, see for example aditivitatii.So, for any sequence disjuncta nx in ,
We have
1
nn
x
11
,mm
n nnn
x x
and thus:
11
.m
n nnn
x x
Considering the inequality:
1
nn
x
1 11
,m m
n n nn nn
x x x
which is maintained, we get to equality:
0 lim inf 0i i i imm i i m
i m
y y y
(4)
The right side of this inequalities disappears:
They are studying the structure of subalgebrei
that is defined quasimasura
.
Se da un x
Incidentally, we choose the corresponding n xS 1,2,...n so
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251
1( )n
ny
x x y x
1,2,...n to be valid.
Now we will put x sup .n n It is clear that x x and x belongs to subalgebrei 0
and also
1
sup
( ) .n
n
n
x x
y x
So, , 0.x x x x x x
Thus, each element x is represented as ,x x u
where 0 , 0,x u si .x x
Lemma 1, 1
( )
k k
o
n nx x x
. So, we have
Even more so, since the is there a submultime numarabil 0 numarabila such
as: 02sup ,x x
where:
0 0 2sup sup .x x
Now we can consider 0sup a substitute for 0.x Therefore,
0 0 2 2.x x x x x x
Lemma is proved.
Definition: a quasimasura v a subalgebra It is called complete as long as the
conditions , ,x x and 0v involve x (and obviously 0v ).
As well as in Lemma 6, quasimasura
I built it is complete.
Lemma 9. Either an additive numarabila full qasimasura to some subalgebra - that
includes regular 0. It is assumed that x x for any 0.x Then:
1)
considered as a metric space. What else can we say about the properties in this space? For
example, will be connected? The answer is negative, in general, since some lie algebras are
normed
listed all finite AB, which are clearly disconnected.
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Teorema 4
An ABN is a metric space continue Astfel, .x x Applying this to an element
,x
result .x x
It remains to prove the Lemma enunt first. First we will
show that if 0v then v and 0.v Indeed, as in Lemma 8, There is an
element ,v v satisfying 0.v v
All items belong to him 0 and thus
his . So v and
0 0.v v
Quasimasura It is thus complete; v and 0.x Now it is clear that each x
belong to him , taking into account that x can be written as ,x x u where x It is an
element and 0.u So inclusiveness
and Juliet are demonstrated. We need.
complete the demonstration only point 1).
Lemma 10. If
sup ( )ny
y
In general: the regularity of the algebra. Thus, each can be considered a ABN space metric.
What else can we say about the properties in this space? For example, will be connected?
The answer is negative, in general, since some lie algebras are normed listed all finite AB,
which are clearly disconnected. Indeed, in this case
x x x
for any 0 ,x so the 1 of an external steps leads to the desired
equality.
Teorema 6. Either a AB complete, and 0 a subalgebra of , and a
quasimasura in 0 . Then there is a subalgebra) regular
including 0 and (b)) a
quasimasura additive numarabila
in
with the following properties:
1)
x x for any 0;x
2) for each additive numarabila quasimasura in
and for any 0x Image check
,x x the inequality x x
It is true for any .x
How is numarabila then the additive equality
x
x
It is true for any 0.x in other words
It is an extension of .
Call quasimasura
It is built in the proof theorem 6
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253
CONCLUSIONS
The main issue is topical because it approaches the fuzzy systems underlying the artificial
intelligence that is implemented in the economic and industrial machines.
REFERENCES
[1] Balbes si Dwinger,The curatours of the University of Missouri,1974
[2] Dumitru Buşneag ,Categories of Algebric Logic, Editura Academiei
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254
ABN AND METRIC STRUCTURES SPACES OF MEASURES
As.univ. Olimpia-Mioara PECINGINA
Universitatea ―Constantin Brancusi‖ ,Tg-Jiu
Prof.Drd. Constantin P. BOGDAN
Universitatea din Craiova
ABSTRACT Is given a measurable space , , .m This space (ii) corresponds to the "metric structure,
Boolean algebra ̂ the resulting algebra is factorization- According to maiprany negligible.This is a
metric structure complete with AB as m̂ . Taking us a certain freedom, we apply the term to the metric
structure of ABN ˆ ˆ,m too.So, every metric structure associated with a metric space offers an example of
ABN.As a result every ABN can be represented in this form. We refer particularly to the Boolean
izomorfismele; izomorfismele metric structures.However, the theory of measure uses another important concept
of isomorphism between spaces.It happens in a few variations, but in all cases we are dealing with a "point" of a
space on the other.Of the many definitions you choose only those that are really used in this part.
Keywords and phrases: boole algebras
1. THE STRUCTURE OF THE METRIC MEASURE SPACE
Is given a measurable space , , .m This space (ii) corresponds to the "metric structure,
Boolean algebra ̂ the resulting algebra is factorization- According to maiprany
negligible.This is a metric structure complete with AB as m̂ .
Taking us a certain freedom, we apply the term to the metric structure of ABN ˆ ˆ,m too.So,
every metric structure associated with a metric space offers an example of ABN.As a result
every ABN can be represented in this form.Before you formulate a corresponding theorem we
refer to the concept of isomorphism. We refer particularly to the Boolean izomorfismele;
izomorfismele metric structures.However, the theory of measure uses another important
concept of isomorphism between spaces.It happens in a few variations, but in all cases we are
dealing with a "point" of a space on the other.Of the many definitions you choose only those
that are really used in this part. Considering the two categories ? and ? whose
elements are the spaces in the form of measures , , .m Morfismele of the first category
are possible applications 1 2: with the following property:
a) 1
1e for any 2e
b) If 2 0m e then 1
1 0m e
If c) 1
1 2m e m e for any 2e (conservation measure) then homomorfism is called
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a metric.These homomorfisme are taken as morphisms of category ? .
In fact every object of category ? is defined by the , algebra and negligible ideal;
quasimasura sets m playing a supporting role.
These two categories they correspond to two forms of izomorfisme.Later we will call an
isomorphism between two measures of spaces 1 1 1, ,m and 2 2 2, ,m as part of his ?
an isomorphism of these spaces.Such an isomorphism is an application bijectiva
2 1: having its properties a) and b) with reverse aplicatiia 1. Moreover, if
(question 1 ) has the property c) then we call an isomorphism metric.If there is an
isomorphism between two measures of spaces then say that these spaces are izomorfice.
Measure spaces are called izomorfice mod0 (izomorfice metric mod0 ). If we exclude
some negligible, we get crowds izomorfice spaces. It is easy to notice that an
isomorphism of spaces imply a corresponding Boolean structures metric isomorphism,
izomorfismul and metric involves an isomorphism of Boolean algebras normed.The converse
is not generally available but can be valid if successfully restrict our chathosts from well-
conducted group spaces that we have considered.
Theorem 8. For every ABN , There's a space masurabilbil , ,m so ABN , si
ˆ ˆ,m sunt izomorfice.
In other words, every ABN is izomorfa metric structures. We refer here to an isomorphism
metric (measurement).
Demonstration.
We can use any of the three representations of proved the Loomis-Sikorski.The last two
theorems are applicable, since every algebra is regular normata.According to one of these
theorems, we can find ABN , a space an algebra of poset from , and a -
ideal I of this algebra, so that there is an isomorphism the quotient algebra 1| on .
In this case, there is a measure on ; This makes it possible to define a quasimasuri
additive numarabile m on According to the following conditions: .m e e
Here is a homomorfism He became a Canon of on 1| . With key on positive
, We can set up easily as the ideal I coinciding with negligible maiprany m , and is an
isomorphism necessary ABN 1ˆ| ,m on the ABN , . Primarily the role of the main
space play space Stone ; In the case of 2 and 3 main space is "standard", bound
only by the value of but not of algebra itself.In other words we get R the Cantor of the
value r ; so lead to the production of r elements of the range 0,1 . Among the most
interesting questions is the following: Why masurabilbil is the best place in terms of the
representation of an ABN?
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2 THE STONE OF AN ABN
We consider the Stone space AB complete . We will identify and 0
.CO Every quasimasura 0 on 0 meet the Lebesgue Theorem hypothesis-
Caratheodory and admits an extension numarabila to a quasimasura additive on algebras
. If quasimasura 0 It's actually a positive numarabila essential additive measure
then this algebra may be described more in detail.We're now in this description. 1. remind you
first of all that each lot matchless belongs to . Be a lot .e rare. Its closure e It is also
rare.We consider the open complementary ? ;G e is represented as a semi-open crowds
reunion
,tt T
G x
tx t T (1)
Taking into account that e then it is; t T 1.tx Our Algebra 0 is normabila (since
measure 0 is available), therefore, meet the requirements of numarabil and the meeting can
be represented can be represented as the smallest common sequences of Hamid Ibrahim:
1
1nt
n
x
, 1,2... .nt T n
We can assume that 1 2
...t tx x Applying the additivity of numarabila 0 This will result in
0 01.nt
x Atunci
e e 0 0 0( ) 1t nn
x tC x 0, 0e , e (2)
2.Algebra 0 , as any normabila, algebra is regular, and thus sets a rare ideal. They note
with I and consider the algebra of maiprany
. (3)
This algebra includes all crowds form 2 0, , .e x q x q I It is clear that 1 we have
(4)
3. Of course a few extensions of numarabile additive 0 exist in . In other words, this is
quasimasura 0 ,oU where U is a homomorfism Birkhoff-Ulam. Of positivity
of his 0 equality 0e is equivalent to the ker .e U I Quasimasura is
complete, since the condition of e e si 0e involve e I and .e
4. Both quasimasurile and numarabile are additive and complete when as 0 is
extended.Taking into account that is an extension of the Lebesgue measure, then,
si | . At the same time, we see that .
5. So we mark the following conclusion.If 0 is an ABN, 0 It is a measure of the 0 , and
is an extension of the Lebesgue
1) his field is algebra includes all crowds form 2 ,x q where 0x and q
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are rare.
2) negligible sets There are even rare submultimile of compact space .
Therefore, all measures in 0 extend the same algebra with the same crowd negligible.
Application 2x I x x It is in this case izomorfismul that is presented in the
theorem 8, coefficient algebra izomorfismul |I on 0 . As I said above, this is an
isomorphism in the ABN, since is constant measurement:
2 2 0ˆ .x I x q x x (5)
But if does not coincide with 0 then induces an isomorphism between and 0.
Notice that each ABN , is izomorfica metric spaces with structures
, , .
Each isomorphism in the ABN , and , induce a homomorfism between Stone
spaces and an isomorphism between measures of space.
3. LEBESGUE SPACES-ROKHLIN
The Discontinuity Of The Cantor T can be used as a representation of a space ABN
, where .cardT r Indeed, there is a ideal I the algebra of Baire space interrupted
extremely compact and an isomorphism coefficient algebra of 0 |IB on . Let us
remember that the algebra of Baire 0B It is the most insignificant algebra including
algebra semideschisa .TD
If his He is considered a measure then this measure "pass" in quasimasura m in
algebra 0B According to the rule 2me e I . In this case mI I ideal becomes
exactly ideal of negligible Baire maiprany m . The structure of the metric space measures
0, ,B m It is in fact ABN ,
We obtain the same metric structure if you replace 0B with algebra complete
0 ,mmB B I
where mI
includes all related elements of crowds mI ideal. "Measure " m
expands on the mB just like izomorfismul . This representation has the special features as a
result of the exceptional role of algebra TD This algebra has the following properties:
1) Each non-empty crowds centered in TD has the nevida intersection.It is obvious because
TD consists of the compact crowd.
2) Each lot in mB is mod0 with the crowd in algebra generated by TD . This means
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there is a standard extension to quasimasurii | Tm D .
3) TD separate the original space points. The property is called the compactitudine of
algebra TD . Its properties 2 and 3 by definition means that TD is a basis of , , .mB m
In the case of some measurable space , ,m subalgebra 0 It is also called a
compact if its properties owns the 1,2 and 3 (of course replacing t and tD with
question 0 ).
A space masurabilbil , ,m with a full size m It is called Lebesgue space-Rokhlin has a
compact if numarabila. theory of these places is completely developed by V.A.Rokhlin in
1940; he called "Lebesgue spaces".We note the Lebesgue space-with Rokhlin .
From what I said at the beginning of this chapter, shall be deducted for each ABN separabila
represents the structure of a metric space Lebesgue-Rokhlin.Because the database structure
numarabilitatii of a Lebesgue space metric-Rokhlin will always be separabila.We will not
submit this theory of space in detail
As a consequence m is supposed to be a measure of probability, 1.m
Either , ,i
i im 1 , 2i two Lebesgue spaces-Rokhlin. everyone has meant most
number of atoms.Taking into consideration the crowds zero for maintaining a general lines,
we'll list the crowds in descending order.Either 1 1
1 2
, ,...m m
and 2 2
1 2
, ,...m m
crowd in 1
and that 2 where 1
1 2
... 1,2 .i
m m i It turns out that this crowd is meeting the
invariance image allows us to classify Lebesgue spaces-Rokhlin metric.Namely,
1) If 1 0km for any i and k then izomorfice metric spaces are, In this case izomorfice
metric metric structures are also what is obvious.
2) If 1 2
k km m for any 1,2,...k then the spaces 1
1 1, ,m and 2
2 2, ,m are metric
izomorfice mod0 and their structures are izomorfice metric metric.
3) If the metric izomorfice metric structures are then 1 2
k km m for any 1,2,...k and
izomorfice metric spaces are mod0. The proof of this theorem to "classification" is feasible.For example monografiia of
V.G.Vinokurov, see B.A.Rubshtein and A.L.Fedorov.
Result from this theorem as Lebesgue spaces-izomorfice metric structures with Rokhlin are
izomorfice mod0 and if these structures are continuous ("nonatomice") then there is an
isomorphism between these "pure" Lebesgue spaces-Rokhlin. Izomorfica classification of
Lebesgue spaces-Rokhlin is equivalent to the classification of ABN. A subspatiu of a
measurable space , ,m It is a space masurabilbil , ,e eE m where , 0E mE si
|e em m . If em m then both spaces have the same metric structure and more
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specifically, there is a canonical isomorphism ˆ ˆ,m on ˆ ˆ,e em generated by the
application e e E .e Note all the fundamental things just now: a subspatiu of a
Lebesgue space-Rokhlin is also Lebesgue space-Rokhlin.Sometimes the concept of subspatiu
is interpreted in a wider sense without it is assumed that E It is measurable.So if the
m E m but E then you can still have E in a measurable space and even more so,
with the same metric structure but in any Lebesgue space-Rokhlin will not be produced. It is
clear that every space , ,m a Lebesgue space isomorphic-Rokhlin is also Lebesgue
space-Rokhlin. If we limit the majority of continuous cardinalitatea will happen the same with
izomorfismele mod0. so the Lebesgue spaces-Rokhlin category is "well built" as a whole.
Lebesgue spaces-Rokhlin comprise a category well built "but are also remarkable in terms of
intrinsic structures.Now we will show the main examples.We'll start with the case of the
Lebesgue spaces continuously-Rokhlin are izomorfe to each other. In fact, one example has
already been displayed; it's the Bernoulli ,,N pq pq . We prefer if 12
p q and
abbreviated writing 1 12 2
and 1 12 2
. The compact numarabila we can take
semideschisa algebra .ND The existence of such databases involves exactly the fact that space
is a Lebesgue space Bernoulli-Rokhlin.Am remember already that points maiprany missing;
Therefore, our example is the Example of a Lebesgue space-Rokhlin., and each of these areas
must be isomorphic Bernoulii.In particular space, all Bernoulli spaces built on N
discontinuous are metric izomorfe. A second example of Lebesgue space-Rokhlin is Lebesgue
space 1, , ,nnI l where nI is the n-dimensional cube.In previous chapters we have
described the : 0,1N by the formula: 21
.n
n
n
x
Similar applications can be constructed in the square 0,1 0,1 , the cube, etc.All are
"almost" bijective and continuous, during the process of "measure" Bernoulli 1 12 2
in
Lebesgue measure: .l e e
Application It is not bijectiva to items N of the form 1, 2,... ,0,0,...nx x x and
1, 2,... ,1,1,...nx x x which corresponds to the rational points of the interval binaries.They form
a lot S numarabila, and its image S includes all rational points of the interval
binaries.Let a bijectie some of S on S (both of them are zealous and
numarabile).Application the date of
,
,
x S
x S
(6)
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is an isomorphism of Bernoulli's range of Lebesgue space. This Lebesgue interval that is
Lebesgue space-and every Lebesgue space Rokhlin-Rokhlin continuously is isomorphic to
it.The same thing is true for squares, cubes, etc. Lebesgue. gotta call it as the best example for
a Lebesgue space-continuous Rokhlin is simply the square Lebesgue. A Lebesgue space-
Rokhlin differently is represented simply as a numarabila or finite group points to the
component 1 2,...,m m An example of another type of interval ,a b with a group of distinct
points 1 2,...,x x to which extent is entirely supported. Coincidence of corresponding maiprany
elements involved, an isomorphism mod0; but no genuine isomorphism is not possible, since
these areas have different cardinalitati and do not allow any bijectie.
Finally, most general example of Lebesgue space-Rokhlin is the interval or Lebesgue square
(or Bernoulli space) with the most numarabila lot of points associated with it.Every Lebesgue
space-Rokhlin is isomorphic metric mod0 such an "example" of space.To simplify the
exposition, this is often taken as the basis for the definition of the Lebesgue space-Rokhlin.
REFERECES
[1] Balbes si Dwinger,The curatours of the University of Missouri, 1974
[2] Dumitru Buşneag ,Categories of Algebric Logic, Editura Academiei ,1990
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INCREASING RESISTANCE OF STRUCTURAL ELEMENTS WITH
CFRP REINFORCEMENTS
Lecturer PhD. Cătălina IANĂŞI, “Constantin Brâncuşi” University of Tg-Jiu [email protected]
Abstract: One of the defining features of a new material is to be resistant, easy to process, to
combine the qualities of basic materials, in the current technique, but not to borrow from them
their negative properties. Composite materials are metallic or nonmetallic matrix reinforced by
the dispersion of particles, fiber or gas. Fibers are able to withstand elastic applications but to
resist for all requests. Matrix serves only for ensuring a support for fiber, stabilizing the fibers
against the forces of disruption. In recent years, carbon fiber composites have been increasingly
used in different ways in reinforcing structural elements. Specifically, the use of composite
materials as a reinforcement for wood beams under bending loads requires paying attention to
several aspects of the problem such as the number of the composite layers applied on the wood
beams.
Keywords: wood beams, CFRP composites, epoxy resin, bending test.
1. INTRODUCTION
This paper describes an experimental study which was designed to evaluate the effect of
layers number of composite material on the stiffness of the wood beams [3]. By using
composite materials in constructions is expected growth flexural strength and shearing, and
confinement elements tablets (increased wood resistance) [5]. Also, is done raising ductility
areas of plastic joint and meet the requirements of exploitation (decrease arrows and status
cracking). In civil and industrial constructions, working with elements of resistance as beams,
pillars, floor, masonry portal, is necessary strength when they present phenomena of wear and
fatigue. Consolidation and reinforcement is done with items as sheets and carbon fiber plates
[3,6]. Among the composites used in construction include: glass fiber, cellulose fiber,
KEVLAR fiber, carbon fiber and graphite, etc.
This paper describes an experimental study which was designed to evaluate the effect
of layers number of composite material on the stiffness of the wood beams [3]. The type of
reinforcement used on the beams is the carbon fiber reinforced polymer (CFRP) sheet
SikaWrap 230C with E module of elasticity 230 000 N/mm2 and traction resistance 4100
N/mm2 an epoxy resin for bonding all the elements Sikadur 330. Structural epoxy resins
remain the primary choice of adhesive to form the bond to fiber-reinforced plastics [5,7,8,9]
and are the generally accepted adhesives in bonded CFRP–wood connections. Advantages of
using epoxy resin in comparison to common wood-laminating adhesives are their gap-filling
qualities and the low clamping pressures that are required.
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Following the experimental tests we developed a numerical procedure, which can
estimate the failure load of the wood beams reinforced with composite materials. The critical
point of the numerical procedure consists in the selection of the most adequate characteristic
values for wood limit stresses. This step was carried out using values found in other studies
and from a comparison of the values obtained from the failure loads of the un-reinforced
beams.
2. EXPERIMENTAL STUDY
The total number of wood specimens manufactured is nine, eight of which are reinforced,
and one is un-reinforced. The wood part of all beams was formed by dry wood beech which
size is equal to 25 by 50 by 500 mm [3]. Three beams were reinforced using one carbon fiber
sheet of thickness equal to 1.5 mm, width equal to 25 mm and the length is equal to 500 cm.
The finished dimension of these beams is equal to 25 by 101.5 by 500 mm because they are
two beams stick together with one carbon fiber sheet of SikaWrap 230C and Sikadur 330
epoxy resin (fig.1) [10].
Fig. 1 Tension failure of a reinforced wood beam with one CFRP sheet (in the middle)
For carbon fiber sheet, once it is placed on the wood beam, with the epoxy resin, all what
is required is to press the carbon fiber sheet with a simple roller and pull out the air [1,2,4,6].
In addition, the carbon fiber sheet has a very high tensile strength (with respect to its weight),
it is available in any length, no joints are required, low thickness, easy to transport, laminate
intersections are simple, economical application no heavy handling and installation
equipment, available in various modules of elasticity, outstanding fatigue resistance, and it
can be coated without preparation. Moreover, the CFRP are compatible with wood with
respect to its mechanical properties. The bending test results for a reinforced wood beam with
one CFRP sheet are shown in table 1.
Table 1. Results for a reinforced wood beam with one CFRP sheet
Force (daN) 0,4 0,8 1,2 1,6 2,0 2,4 2,8 3,2
Deflection f (mm) 1 1,5 3,9 6,1 8,3 11,6 15 18,3
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Other three beams were reinforced using two carbon fiber sheets of thickness equal to
3 mm, width equal to 25 mm and the length is equal to 500 cm. The finished dimension of
these beams is equal to 25 by 73 by 500 mm because they are two slides of wood up and
down stick by the main wood beam, with two carbon fiber sheets of SikaWrap 230C and
Sikadur 330 epoxy resin (fig.2).
Fig. 2 Tension failure of a reinforced wood beam with two CFRP sheets and two slides of wood (up and down)
The bending test results for a reinforced wood beam with two CFRP sheets and two slides of
wood are shown in table 2.
Table 2. Results for a reinforced wood beam with two CFRP sheets (up and down)
Force (daN) 0,4 0,8 1,2 1,6 2,0 2,4 2,8 3,2
Deflection f (mm)
1 2,2 3,9 4,8 61 8,9 12,7 13,3
The last three beams were reinforced using two carbon fiber sheets of thickness equal to 3
mm, width equal to 25 mm and the length is equal to 500 cm. The finished dimension of these
beams is equal to 25 by 113 by 500 mm because they are two beams stick together with two
carbon fiber sheets of SikaWrap 230C and an epoxy resin Sikadur 330, with a density of 1,31
kg/dm 3 , from Sika-Romania, and another slide wood beam in the middle of the beam (fig. 3).
The bending test results for a reinforced wood beam with two CFRP sheets and a wood slide
in the middle of the beam are shown in table 3.
Fig. 3 Tension failure of a reinforced wood beam with two CFRP sheets (in the middle of the beam) and one
slide of wood
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Table 3. Results for a reinforced wood beam with two CFRP sheets (in the middle)
Force (daN) 0,4 0,8 1,2 1,6 2,0 2,4 2,8 3,2
Deflection f (mm)
1,3 1,9 2,1 2,7 3,2 4,6 5,8 7,6
The specimens tested were not subjected to lateral instability during loading. The total load on
the beam was applied equally at one point equidistant from the reactions (the half length of
the beam).
We use the bending device of the universal machine for mechanical tests which has the
distance between the rollers l = 460 mm. Standard samples was dry beech wood beam
with a rectangular section of 25x50 x500 mm (bxhxl).
After we study those examples we observe that the reinforced wood beam with two CFRP
sheet and a wood slide in the middle (fig.3) is the most resistant and has a good elasticity
breaking into a 10,5 mm deflection. Also, we can say that the number of composite material
layers influences the stiffness of the wood reinforced beams.
CONCLUSIONS
It is proposed to use an inexpensive and easily processed material that is wood.
As a rigid material with good strength and relatively low cost, we use a composite. A
several un-reinforced and reinforced wood beams were tested in order to find their flexural
capacity. CFRP materials were conditioned in an environment of 65±5% relative humidity
and temperature of 20±2°C as this is the service environment in which CFRP reinforced
beams are expected to be used. The results indicate that the behavior of reinforced beams is
totally different from that of un-reinforced one. The reinforcement has changed the mode of
failure from brittle to ductile and has increased the load-carrying capacity of the beams.
Observations of the experimental load–displacement relationships show that flexural strength
increased and middle vertical displacement decreased for wood beams reinforced with CFRP
composite plates, compared to those without CFRP plates. Also, we can say that the number
of composite material layers of carbon sheet and their positions influence the stiffness of the
wood reinforced beams.
Acknowledgments
The author is grateful to the Building Velmix Ltd, Tg-Jiu, Romania, without whose financial
support the present work could hardly be conducted.
REFERENCES
[1] Abdel-Magid B, Dagher HJ, and Kimball T. The effect of composite reinforcement on
structural wood. In: Proceedings – ASCE 1994 materials engineering conference,
Infrastructure: new materials and methods for repair, San Diego, CA, November 14–16; 1994.
[2] Camille A. Issa, Ziad Kmeid. Advanced wood engineering: glulam beams. Department of
Civil Engineering, Lebanese American University, Byblos, Lebanon. Construction and
Building Materials 19 (2005) 99–106.
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[3] Ianăşi C. Research on reducing the risk of damage for the resistance elements of wooden
building, 2nd WSEAS International Conference on RISK MANAGEMENT, ASSESSMENT
and MITIGATION (RIMA '13) Brasov, Romania, June 1-3, 2013, pp. 161-164, ISSN 2227-
460X
[4] Yeou-Fong Li, Yao-Ming Xie, Ming-Jer Tsai. Enhancement of the flexural performance
of retrofitted wood beams using CFRP composite sheets. Construction and Building Materials
23 (2009) 411–422.
[5] Plevris N, Triantafillou T. Creep behavior of FRP-reinforced wood members. J Struct.
Eng. – ASCE 1995;121(2):174–86.
[6] Plevris N, Triantafillou T. FRP-reinforced wood as structural material. J Mater Civil Eng
– ASCE 1992;4(3).
[7] Tingley DA, Leichti RJ. Reinforced glulam: improved wood utilization and product
performance. Paper presented at Technical Forum – Globalization of wood: supply, products,
and markets. Portland (Oregon): Forest Products Society; 1993.
[8] Triantafillou T, Deskovic N. Innovative prestressing with FRP sheets: mechanics of short-
term behavior. J Eng Mech – ASCE 1991; 117(7):1652–72.
[9] Triantafillou T, Deskovic N. Prestressed FRP sheets as external reinforcement of wood
members. J Struct Eng – ASCE 1992; 118(5):1270–84.
[10] www.sika.ro
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INDEX AUTHORS
Nr.
crt
Name and Surname, Institution Pagina
1. ADÎR Ancuta
Grigore Cerchez Technological College, Bucharest
Nr.1: 64
2. ADÎR George
University POLITEHNICA of Bucharest,
Nr.1: 64
3. ADÎR Victor
University POLITEHNICA of Bucharest,
Nr.1: 64
4. ALBULESCU Radu Gabriel
Oil Equipment Company of Ploiesti, Romania
Supliment Nr1:
59
5. ALDEA Mihaela
University ‖1 Decembrie 198‖ of Alba Iulia
Nr.1: 227
6. AMZA Gheorghe
Polytechnic University of Bucharest, Romania,
Department of Materials and Welding Technologies,
Supliment Nr1:
51, 67
7. APOSTOLESCU Zoia
Polytechnic University of Bucharest, Romania,
Department of Materials and Welding Technologies,
Supliment Nr1:
51, 67
8. BABIS Claudiu Polytechnic University of Bucharest Romania,
Department of Materials and Welding Technologies,
e-mail: [email protected]
Supliment Nr1:
84
9. BÂLDEA Monica University of Pitesti, Romania,
Nr.1: 195
Supliment Nr1:
150, 333
10. BĂLTEANU Ancuţa University of Pitesti, Romania
Supliment Nr1:
333
11. BĂRBĂCIORU Iuliana Carmen ‖Constantin Brâncuşi‖ University, Tg. Jiu
Nr.1: 200, 207
12. BOCA Maria Loredana ―1 Decembrie 1918‖ University of Alba Iulia
Nr.1: 78
13. BOGDAN Constantin P.
Universitatea din Craiova Nr.1: 240, 247
14. BRĂNICĂ Diana Nicoleta (MILOSTEANU), University Politehnica of Bucharest
Supliment Nr1:
219
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15. BULAC Ion
Doctor, University of Pitești
email: [email protected]
Nr.1: 97, 103
16. BUNECI Mădălina Roxana University Constantin Brâncuşi of Târgu-Jiu
Nr.1: 213, 220
17. CHIVU Oana
Polytechnic University of Bucharest, Romania,
Department of Materials and Welding Technologies,
Supliment Nr1:
76, 84
18. CIOFU Florin University "Constantin Brâncuşi" of Târgu-Jiu,
Supliment Nr1:
46
19. CIORTEA Elisabeta Mihaela
University ‖1 Decembrie 198‖ of Alba Iulia,
Nr.1: 227
20. CÎRŢÎNĂ Daniela
„Constantin Brâncuşi‖ University of Tg-Jiu Supliment Nr1:
313
21. CIRTINA Liviu Marius Constantin Brâncuşi University of Târgu Jiu, Romania,
Supliment Nr1:
294
22. CIZER Laura ―Mircea cel Bătrân‖ Naval Academy
Supliment Nr1:
18, 24
23. DELIU Florențiu ―Mircea cel Bătrân‖ Naval Academy
Supliment Nr1:
18
24. DIMITRESCU Andrei
Universitatea Politehnica Bucuresti, Facultatea IMST,
Departamentul T.M.R.
Supliment Nr1:
5, 12, 106
25. DINU Bogdan ORACLE SA, Bucharest,
Supliment Nr1:
250
26. DINU Marius Bogdan University ―POLITEHNICA‖ of Bucharest,
Faculty of Electronics, Telecommunications and Information Technology,
Department of Electronic Devices, Circuits and Apparatus
Supliment Nr1:
39, 243
27. DOBROTĂ Dan
Constantin Brancusi University of Targu Jiu, Romania,
Department of Systems Engineering and Management Technology,
e-mail: [email protected]
Supliment Nr1:
59, 84
28. DRAGOMIR Adrian Ioan
Auto Repair Company of Brasov, Romania Supliment Nr1:
51, 59
29. DRAGOMIRESCU Cristian
Univ. Politehnica Bucharest,
email: [email protected]
Supliment Nr1:
93
30. DUMITRESCU Iosif Department of Industrial Mechanical Engineering and Transport,
University of Petroşani, [email protected]
Nr.1: 110, 120
31. DUMITRIU Mădălina
Department of Railway Vehicles, University Politehnica of Bucharest
Nr.1: 129, 137
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32. FLOREA Traian Academia Navală „Mircea cel Bătrân‖
Nr.1: 84, 91, 165,
178, 183
33. FLOREA Traian Vasile A.P.M. Agigea of Constanta, ROMANIA
Nr.1: 157, 165
34. GHIMIȘI Ștefan
Constantin Brâncuși University of Targu Jiu
Supliment Nr1:
222, 294
35. GRIDAN Horia Constantin Brâncuși University of Targu Jiu
Supliment Nr1:
294
36. IANCU Cătălin
Engineering Faculty,‖C-tin Brâncuşi‖ Univ. of Tg-Jiu,
Supliment Nr1:
229
37. IANĂŞI Cătălina
Engineering Faculty,‖C-tin Brâncuşi‖ Univ. of Tg-Jiu,
Nr.1: 261
38. ILINCIOIU Dan
University of Craiova, Faculty of Mechanics,
Department of Applied Mechanics and Civil Constructions, Calea Bucuresti
Street, no. 107, Craiova,Code 200512, Romania,
Nr.1: 27
39. IONESCU Simona e-mail: [email protected]
Nr.1: 33, 43
40. IONICI Cristina
University ―Constantin Brâncuşi‖ of Tg-Jiu,
Supliment Nr1:
154, 158
41. IOVAN Stefan West University of Timisoara, Computer Science Department,
Railway Informatics SA, Bucharest,
Supliment Nr1:
32, 39, 250, 264
42. IOVANOV Miodrag
―Constantin Brâncuşi‖ University of Târgu-Jiu
Nr.1: 234
43. IOVANOV Valeria Victoria
Technical College No. 2, Târgu-Jiu
Supliment Nr1:
270, 276, 282
44. ISTRATE Mihaela
Faculty of Mechanics and Technology ,University of Pitesti
e-mail: [email protected]
Nr.1:195
Supliment Nr1:
150
45. ITU Răzvan Bogdan
Department of Industrial Mechanical Engineering and Transport,
University of Petrosani,
Nr.1: 110, 120
46. ITU Vilhelm
Department of Industrial Mechanical Engineering and Transport,
University of Petroşani,
Nr.1: 110, 120
47. IVANUS Cristian TAROM SA, Bucharest
Supliment Nr1:
32, 264
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48. LUCA Liliana
Constantin Brancusi University of Targu-Jiu
Nr.1: 18
49. MĂRĂȘESCU Daniel Academia Navală „Mircea cel Bătrân‖
Nr.1: 84, 91
50. MARC Gheorghe
―1 Decembrie 1918‖ University of Alba Iulia,
Nr.1: 78
51. Marius STAN
Petroleum - Gas University of Ploiesti
Nr.1: 71
52. MARTINEZ Francico Cavas
Polytehnic University of Cartagena Supliment Nr1:
158
53. MIHUȚ Nicoleta – Maria
Constantin Brancusi University of Targu Jiu
Supliment Nr1:
46, 289
54. MIRIŢOIU Cosmin-Mihai University of Craiova, Faculty of Mechanics
Department of Vehicles, Transports and Industrial Engineering
Calea Bucuresti Street, no. 107, Craiova,Code 200512, Romania,
Nr.1: 27
Supliment Nr1:
112, 119, 213
55. MORARIU Cristin Olimpiu Department of Manufacturing Engineering, Technological Engineering and
Industrial Management Faculty, Transilvania University of Brasov, Romania,
e-mail: c.morariu@unitbv. ro
Nr.1: 57, 178
56. MOROIANU Corneliu
Email address: [email protected] Nr.1: 157, 165, 183
57. NEACSA Marin
University POLITEHNICA of Bucharest,
Nr.1: 64
58. NICULA Dana
Dunărea de Jos University of Galați Supliment Nr1:
222
59. NIOAȚĂ Alin
Engineering Faculty,
‖Constantin Brâncuși‖ University of Târgu-Jiu,
Supliment Nr1:
46, 126, 133
60. NIŢOI Dan
Universitatea Politehnica Bucuresti, Facultatea IMST,
Departamentul T.M.S.
Supliment Nr1:
12, 106
61. NITOI Dan Florin Polytechnic University of Bucharest, Romania,
Department of Materials and Welding Technologies
Supliment Nr1:
67
62. NOVAC George
―Mircea cel Batran‖ Naval Academy, Constanta
Nr.1: 145, 151
63. PARIS Adrian Stere
Univ. Politehnica Bucharest
email: [email protected]
Supliment Nr1:
93, 99
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270
64. PASARE Minodora Maria
University ―Constantin Brancusi‖ of Tg-Jiu
Supliment Nr1:
138
65. PǍTRAŞCU Mariana (ANTONESCU) e-mail: [email protected]
Nr.1: 33, 43
66. PECINGINĂ Irina Ramona „Constantin Brâncuşi‖ University of Tg-Jiu
irinacornescu yahoo.com
Supliment Nr1:
313
67. PECINGINA Olimpia
Universitatea ―Constantin Brancusi‖ ,Tg-Jiu Nr.1: 240, 247
68. PETRESCU Valentin
Lucian Blaga University of Sibiu, Romania,
Department of Industrial Engineering and Management
Supliment Nr1:
67
69. PIRGHIE Ana-Camelia
Stefan cel Mare University of Suceava,
Department of Mechanics and Technology,
Nr.1: 49
70. PIRGHIE Cristian
Stefan cel Mare University of Suceava,
Department of Mechanics and Technology
Nr.1: 49
71. PLESEA Valeriu
„Constantin Brâncusi‖ Universiy of Tg.-Jiu
e-mail: plesea_valeriu@ yahoo.com
Supliment Nr1:
142
72. POPESCU Constantin
Polytechnic University of Bucharest Supliment Nr1:
162, 173, 182, 195
73. POPESCU George
Constantin Brâncuşi University of Tg-Jiu
Supliment Nr1:
325, 329
74. POPESCU Iulian
University of Craiova
Nr.1: 3,10,18
75. PRUIU Anastase Academia Navală „Mircea cel Bătrân‖
Nr.1: 84, 91, 157,
165
76. RADU Serghei Barklav Company,
Supliment Nr1:
18, 24
77. RĂDULESCU Constanţa
,,Constantin Brancusi‖ University of Tg-Jiu,, România
Supliment Nr1:
46, 294, 301
78. ROSCA FARTAT Gabi
e-mail: [email protected]
Supliment Nr1:
162, 173, 182, 195
79. ROŞCA Vâlcu
Department of Applied Mechanics and Civil Constructions,
Calea Bucuresti Street, no. 107, Craiova,Code 200512, Romania,
Supliment Nr1:
213
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271
80. ROŞU Catălin
University of Craiova,
S.C. DICO Romania S.R.L., Pieleşti, Cîrcea Street, No. 2, Romania,
Supliment Nr1:
206, 213
81. SAMOILESCU Gheorghe ―Mircea cel Bătrân‖ Naval Academy,
Supliment Nr1:
18, 24
82. SASS Ludmila University of Craiova
Faculty of Mechanics, [email protected]
Nr.1: 3,10
83. SPORIȘ Adriana Academia Navală „Mircea cel Bătrân‖
Nr.1: 84, 91, 157,
165, 178, 183
84. STAN Marius
Petroleum - Gas University of Ploiesti
Nr.1: 71
Supliment Nr1:
236
85. STANCIOIU Alin
University Constantin Brancusi of Targu Jiu
Supliment Nr1:
320
86. STĂNESCU Alexandru
Universitatea Politehnica Bucuresti,
Facultatea IMST, Departamentul T.M.R.
Supliment Nr1: 5
87. STǍNESCU Constantin D. Polytechnic University of Bucharest
e-mail: [email protected]
Nr.1: 33, 43
Supliment Nr1:
162, 173, 182, 195
88. STANIMIR Alexandru
University of Craiova, Faculty of Mechanics,
Department of Vehicles, Transports and Industrial Engineering,
Calea Bucuresti Street, no. 107, Craiova,Code 200512, Romania,
Supliment Nr1:
206,, 213
89. SURDU Ionela Ramona
Universitatea Politehnica din Bucuresti
E-mail: [email protected]
Supliment Nr1:
340
90. TǍRǍBUŢǍ Doina (ENE)
e-mail: [email protected]
Nr.1: 33, 43
91. TĂRÂŢĂ Daniela Florentina
University of Craiova, Faculty of Mechanics,
Department of Vehicles, Transports and Industrial Engineering, Calea
Bucuresti Street, no. 107, Craiova,Code 200512, Romania,
Supliment Nr1:
206
92. TÂRCOLEA Constantin Univ. Politehnica Bucharest,
email: [email protected]
Supliment Nr1:
93
93. TĂTAR Adina
„Constantin Brâncuşi‖ University of Tg-Jiu
Nr.1: 174
Supliment Nr1:
307
94. TĂTARU Ion
University of Craiova, Faculty of Mechanics,
Department of Applied Mechanics and Civil Constructions,
Calea Bucuresti Street, no. 107, Craiova,Code 200512, Romania,
Nr.1: 27
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272
95. TEMPEA Iosif
University Politehnica of Bucharest
Supliment Nr1:
219
96. TEODORESCU Marius Cornel
Oil Equipment Company of Ploiesti, Romania
Supliment Nr1:
51, 59
97. TOMESCU Cristian INCD INSEMEX Petrosani,
e-mail: critom05@ yahoo.com
Supliment Nr1:
142
98. UNGUREANU Viorica Mariela
Constantin Brancusi University of Targu Jiu, Romania Nr.1: 207
99. VLAICU POPA Marius Eremia SNLO Tg.- Jiu,
e-mail: m.vlaicu @ yahoo.com
Supliment Nr1:
142
100. ZAHARIA Sebastian Marian
Department of Manufacturing Engineering,
Technological Engineering and Industrial Management Faculty,
Transilvania University of Brasov, Romania, e-mail:
Nr.1: 57
Supliment Nr1:
257
101. ZAMFIRACHE Marius
University of Craiova, Faculty of Mechanics,
Department of Vehicles, Transports and Industrial Engineering, Calea
Bucuresti Street, no. 107, Craiova,Code 200512, Romania,
Supliment Nr1:
206, 213
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INDEX KEYWORDS
A
Autodesk Inventor Professional analysis
automation algorithm
aluminium alloy
auto pieces Aluminium alloy
annulus spacer annulus bellows
angular displacement artefact
assessment analysis
analytics accelerated reliability testing
air atom
Avogadro analytical modelling
B
brick elements boundary lubrication
ball bearings, brazing
business analytics, brandjacking
business intelligence bending moment
big data big data
biotechnologies biomass
Boltzmann biodiesel
burning
C
computer simulation censored data
cardan joint cardan transmission
correlating cutting and loading machine
critical speed crankshaft
cloud computing cloud enterprise
cloud governmental cyber attack
corrosion carbon steel
crack testing current density
correlation coal
copper compression
calandria tub Candu reactor,
calandria tube channel closures.
carbon footprint CAD,
complex erosion cloud offline
cloud-based CNC
costs customers,
(α,β)-cut and core of a
intuitionistic fuzzy sets
D
dewaxing dewaxing probe
dynamic study dynamic behaviour
deflections data loss
data theft durability
diffusion dependability
design data compression technique
data capture technique data mining
data warehousing design of experiment
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discount dissociation
droplet discrete groupoid
E
elastomer Embedded
engine room engine
exhaust efficiency
electric field eigenfrequency
eigenfrequency electric strength
energy end fitting
eruptions environmental
efficiency economicity
electrons effective listening
external environment employees
emissions from oil equivalence relation
F
finite element analysis functional parameters
finire speed filtering
finite element force
fuel channel fuel bundle
feeder coupling feeder coupling
force of electrostatic repulsion fuel combustion
function
G
greenhouse gas gaussian model
geometric optimization
H
hunting heat affected zone
I
isolated defect irreversibility
indenter innovation
integrated management system information sources
internal environment Intuitionistic fuzzy sets
K
kinematic analysis kinematic pair
Korovkin Khalimsky topology
L
life losses
low temperatures linear displacement
lifecycle large volume of data
liniar space Lyapunov operators
M
mechanism with three RRT dyads movement laws
mechanisms for scissors metallic structure
mesh mechanism
molecular dynamics modeling
manufacturing lines mission critical
monitoring marine
measurements marine
multiple role station modulator
materials selection manufacturing systems
mass per unit length microhardness
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models methane
maintenance manganese
milling tool modeling
mathematics minning activities
managers mathematical relation
mathematical modeling
N
nanotribology NDT
nuclear operators
O
open source open cloud
orbit
P
particular cases pipeline
power pneumatic system
power sensor plating
phishing pipes
parts of the oil industry
positioning system
polypropylene core processing objects
potential difference predictive control
pump pressure tube
pressure tube positioning assembly
processing pallets
product plan
pollution particles
plasma pollutants
parameters program
primary seals positive operators
pseudorandom number generator Petri nets
R
rehabilitation reliability
reliability testing refrigerator compressor
railway vehicle regeneration
rebuilding rotary motor
reliability regenerable
Reduction of environmental pollution road transport
Q
quadrilateral mechanism quality
quality indicator
S
sustainability scraper conveyer
suspension Stirling,
solar and wind energy separator
statistics software
steel fabric support
sandwich bars stiffness
steel sintered sintering process
shortening shield plugs
sawdust SolidWorks
sustainability safe
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snapshot skills
sedimentable powders subatomic processes
T
trajectories two conductive elements
tetrahedral elements technical deviations
transfer object technological process
topological groupoid transport
U
ultrasound ultrasonic field
ultrasonic motors underground areal waters.
V
ventilations vertical vibrations
valve vibration
visualization
W
wears welding
water vapours working space
working fluid web hosting
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