10.1.1.136.7889
TRANSCRIPT
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UNIVERSITY OF SYDNEY
DEPARTMENT OF AERONAUTICAL ENGINEERING
ROTOR WAKE INVESTIGATIONUSING THE SMOKE FLOW
VISUALISATION TECHNIQUE
Osvaldo Maximo Querin
March 1993
This thesis is submitted in fulfilment of the requirements for the degree of Master of
Engineering (Research)
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Abstract
Experiments were carried out on a small four bladed rotor at different climb rates.
The smoke-filament technique was used to visualise the rotor tip vortices; video
equipment was then used to record the images produced. The recorded images were
digitised and enhanced to assist in the identification of the vortex location. The
vortex trajectories were compared with established data and with the paths generated
by the general tip vortex path equations. It was found that these equations over-
simplified the vortex trajectories, modelling neither the interaction between vortices
nor their meandering.
The wakes studied showed evidence of vortex interaction. It was found that vortices
close to one another combined in pairs and spun about a common centre as they
moved downstream. A new mean path equation was thus defined which could model
this type of behaviour. An exponential equation was selected to model the mean path.
To assist in the determination of the order which best suited the curve, the least
squares method was used. The meandering of the vortex trajectory about its mean
path was studied and the types of instability present were determined. Three types
of instability were found in tip vortices; short-wave, mutual-inductance and long-
wave. It was discovered that the helical path followed by a hovering rotors tip
vortex was unstable under most flight conditions and that fluid damping suppressed
the magnitude of these instabilities.
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Acknowledgements
I would like to take this opportunity to thank all the members of staff in the
Department of Aeronautical Engineering for their support and guidance over the past
few years, with special mention to Mr John Blackler and Mr John Curtis for those
words of wisdom when I most needed them. I would also like to give special thanks
to K.C. Wong and Alex Tan for putting up with me.
I also want to thank my parents for their support and guidance, and Abbie for her
support, understanding and patience.
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CONTENTS
Page
Abstract ii
Acknowledgements iii
List of Figures vii
List of Tables x
Nomenclature xi
1. INTRODUCTION
1.1 Background 1
1.2 Wake Path Equations 4
1.3 Flow Visualisation Techniques 5
1.4 Aim of this Research 5
1.5 Outline of Research Presentation 6
2. ROTOR WAKE VISUALISATION
2.0 Introduction 7
2.1 Smoke Filament Technique 7
2.2 Water Towing Tank Technique 10
2.3 Small Particles Technique 12
2.4 Schlieren Technique 13
2.5 Shadowgraph Technique 15
2.6 Shadowgraph and Schlieren Applications for Rotors Operating
at Low Mach Numbers 17
2.6.1 Hot-Wire Technique 17
2.6.2 Spark Technique 19
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2.7 Alternative Visualisation Techniques 20
2.7.1 Atmospheric Water Vapour Condensation 20
2.7.2 Hot-Wire Anemometer Tracking 20
2.7.3 Laser Velocimeter Tracking 22
2.8 Discussion 23
3. FLOW VISUALISATION EXPERIMENT
3.1 Experimental Equipment 24
3.1.1 Model Test Rotor 24
3.1.2 Rotor Test Stand 25
3.1.3 Wind Tunnel Facilities 26
3.1.4 Synchronisation Equipment 27
3.2 Experimental Procedure 28
3.3 Discussion 29
4. IMAGE PROCESSING
4.1 Image Digitising 30
4.2 Image Enhancement 31
5. ROTOR WAKE GEOMETRY RESULTS
5.0 Introduction 34
5.1 Wake Results 345.2 Wake Features 35
5.3 Wake Instabilities 49
5.4 Generalised Wake Geometries 53
5.4.1 Tip Vortex Mean Axial Path Equation 53
5.4.2 Axial Path Instability Criterion 56
5.4.3 Tip Vortex Mean Radial Path Equation 63
5.4.4 Radial Path Instability Criterion 64
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6. CONCLUSION 71
REFERENCES 74
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List of Figures
Figure 1 Typical oil smoke generator. 8
Figure 2 Smoke-flow visualisation of tip vortices with two vortex
cores shown. 9
Figure 3 Dye-layer visualisation technique illuminated with flood lights. 10
Figure 4 Dye-layer visualisation technique illuminated with laser sheet. 11
Figure 5 Localised-dye visualisation technique, with dye discharged
from blade tips and illuminated with laser sheet. 12
Figure 6 The Schlieren system. 13
Figure 7 Schematic diagram of the Z configuration Schlieren system. 14
Figure 8 Double-pass Schlieren system. 14
Figure 9 Shadowgraph systems; (a) divergent light rays,
(b) parallel light rays. 15
Figure 10 Typical Shadowgraph set-up for rotor wake visualisation. 16
Figure 11 Improved wide-field shadowgraph set-up using
a single beam splitter. 17
Figure 12 Hot-wire shadowgraph photograph of flow behind a propeller. 18
Figure 13 Spark shadowgraph photograph of flow behind a propeller. 19
Figure 14 Typical arrangement for a radially traversing hot-wire
probe spinning with the rotor. 21
Figure 15 Typical data indicating the position when the vortex core strikes the
hot-wire probe. 21
Figure 16 Typical tip vortex path determination data. 22Figure 17 Dimensioned diagram of the test rotor stand. 26
Figure 18 Arrangement of smoke rake and test stand in wind tunnel. 26
Figure 19 Schematic diagram of the synchronisation equipment. 28
Figure 20 Position of video camera in relation to rotor. 28
Figure 21 Digitised black and white video picture showing
tip vortices, vortex sheets and rotor blade. 31
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Figure 22 Digitised video picture with enhanced false colour
imaging. Vortex sheets, tip vortices and rotor blade
are easily identified. 32
Figure 23 Comparison between experimental and predicted wake
geometries; (a) radial, (b) axial. (Ct = 0.0018) 38
Figure 24 Comparison between experimental and predicted wake
geometries; (a) radial, (b) axial. (Ct = 0.0042) 39
Figure 25 Comparison between experimental and predicted wake
geometries; (a) radial, (b) axial. (Ct = 0.0048) 40
Figure 26 Comparison between experimental and predicted wake
geometries; (a) radial, (b) axial. (Ct = 0.0063) 41
Figure 27 Comparison between experimental and predicted wake
geometries; (a) radial, (b) axial. (Ct = 0.0078) 42
Figure 28 Comparison between the experimental wake of
Bagai et al (1992-b) and predicted wake geometries;
(a) radial, (b) axial. (Ct = 0.0074) 43
Figure 29 Comparison between the experimental wake of
Swanson et al (1992) and predicted wake geometries;
(a) radial, (b) axial. (Ct = 0.0113) 44
Figure 30 Comparison between the experimental wake of
Swanson et al (1992) and predicted wake geometries;
(a) radial, (b) axial. (Ct = 0.0167) 45
Figure 31 Individual vortex trajectories of the four vortices
from the wake of figure 27. 46
Figure 32 Individual vortex trajectories of the two vortices
from the wake of figure 28. 47
Figure 33 Individual vortex trajectories of the three vortices
from the wake of figure 30. 47
Figure 34 Instability mode shapes; the short-wave instability,
the mutual -inductance modes with /k = 5/2 and3/2,
and the long-wave instability with /k = 1/2. The dark
portions are outside the cylinder on the near side; the
light portions are inside. Reproduced from Widnall (1972). 50
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Figure 35 Stability boundaries for helical vortex filaments of finite
core. The value of the ratio of core-to-cylinder radius are
shown on each curve. Above the boundary, the helical
filament of that core size is unstable. Reproduced from
Widnall (1972). 51
Figure 36(a) Axial wake geometry and mean axial path. (Ct = 0.0018) 57
Figure 36(b) Meander of vortex about mean axial path. 57
Figure 37(a) Axial wake geometry and mean axial path. (Ct = 0.0042) 58
Figure 37(b) Meander of vortex about mean axial path. 58
Figure 38(a) Axial wake geometry and mean axial path. (Ct = 0.0048) 59
Figure 38(b) Meander of vortex about mean axial path. 59
Figure 39(a) Axial wake geometry and mean axial path. (Ct = 0.0063) 60
Figure 39(b) Meander of vortex about mean axial path. 60
Figure 40(a) Axial wake geometry and mean axial path. (Ct = 0.0078) 61
Figure 40(b) Meander of vortex about mean axial path. 61
Figure 41(a) Axial wake geometry and mean axial path. (Ct = 0.0074) 62
Figure 41(b) Meander of vortex about mean axial path. 62
Figure 42(a) Radial wake geometry and mean radial path. (Ct = 0.0018) 65
Figure 42(b) Meander of vortex about mean radial path. 65
Figure 43(a) Radial wake geometry and mean radial path. (Ct = 0.0042) 66
Figure 43(b) Meander of vortex about mean radial path. 66
Figure 44(a) Radial wake geometry and mean radial path. (Ct = 0.0048) 67
Figure 44(b) Meander of vortex about mean radial path. 67
Figure 45(a) Radial wake geometry and mean radial path. (Ct = 0.0063) 68
Figure 45(b) Meander of vortex about mean radial path. 68
Figure 46(a) Radial wake geometry and mean radial path. (Ct = 0.0078) 69
Figure 46(b) Meander of vortex about mean radial path. 69
Figure 47(a) Radial wake geometry and mean radial path. (Ct = 0.0074) 70
Figure 47(b) Meander of vortex about mean radial path. 70
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List of Tables
Table 1 Model Rotor Characteristics 25
Table 2 Rotor Test Parameters 35
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Nomenclature
b = Number of blades
c = Blade chord, m
CV = Velocity coefficient, Vz/(R)
CT = Rotor thrust coefficient, T/(2R4)
kR = (Pitch of the helix)-1
k = k/(1+k 2R2)
r = Radial dimension, m
r/R = Non-dimensional radial tip vortex displacement relative to tip-path-
plane
R = Rotor radius, m
T = Rotor thrust, N
Vz = Axial velocity, m/s
z = Axial dimension, m
z/R = Non-dimensional axial tip vortex displacement relative to tip-path-
plane
= Perturbation wave number
/k = Number of waves per cycle of the helix
twist = Blade twist angle, deg
1 = Measured parameter
= Atmospheric density, kg/m3
= Density gradient
x
= Change in density gradient2
x2
= Rotor solidity, bc/R
= Blade azimuth angle, deg
w = Tip vortex age, deg
= Rotor rotational frequency, rad/s
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Chapter
ONE
INTRODUCTION
1.1 BACKGROUND
Helicopters and related types of rotorcraft are versatile machines. Their capabilities
may include level flight, vertical flight and hover. Of these flight regimes, the most
important and critical to the rotorcraft is hover. The reason for this is that hover
performance can in most of these machines dictate their maximum usable payload.
Performance predictions, therefore, become a crucial element in the development and
analysis of rotorcraft.
The methods used to predict performance have expanded dramatically over the past
four decades. Momentum theory has been the simplest and most basic approach,
(Gessow et al 1985), in which the rotor was treated as an infinitesimally thin actuator
disk with uniformly accelerated air throughout. As more accurate performance
predictions became necessary, performance charts, such as those of Tanner (1964),
were produced for a large range of standard rotor blades and configurations. When
limitations in these charts became evident due to increases in the number of blades
and their loadings, the need for more general methods became necessary.
To achieve this task, the individual blade elements had to be considered. The analysis
which followed consisted of balancing momentum and two-dimensional aerofoil
theories to derive inflow and resulting lift and in-plane forces at each blade element.
This produced what is commonly known as blade element theory (Gessow et al 1985,
Stepniewski et al 1984). However, the performance predicted by this method was
still extremely optimistic. The reason for this was that although blade characteristics
had been accounted for, the influence of the real rotor wake with tip and sheet
vortices on the blades had not. To partially account for such an effect, researchers
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at the time introduced a Tip Loss Factor which assumed complete loss of lift over
a small percentage of the blade at the tip. Three dimensional tip effects and wake
non-uniformity caused by finite number of blades, however, limited the usefulness
of this method for detailed rotor analysis.
To solve the three dimensional problem with a finite number of blades, the rotor
wake had to be incorporated. This was originally done by using vortex theory. This
theory described the wake as a series of cylindrical vortex sheets representing the
radial variation of circulation. This was essentially the approach taken by Goldstein
(1929) and Lock (1931) with propellers and later the work of Willmer (1959), Piziali
et al (1962) and Miller (1962) with helicopter rotors improved this representation of
the wake. Their combined work redefined the representation of the wake into a mesh
of discrete line vortices. However, the spatial positioning of the wake elements was
still uniform with wake contraction and the interaction between wake elements still
not considered.
The work of Miller (1962) and Willmer (1959), which used an undisturbed prescribed
wake model, was followed by the work of Landgrebe (1969). In his work, although
for forward flight, the rotor was represented by numerous discrete vortex elements.
The wake was divided into a series of near and far wake regions. The analysis was
then achieved by the implementation of the classical Biot-Savart law with numerical
integration techniques. This method has been the most widely used means of
predicting performance for the past three decades. The work of Gray (1956, 1972)
and Landgrebe (1972), on the identification of the true path of tip vortices and vortex
sheets led to the incorporation of Landgrebes (1969) forward flight wake analysis
to the hover flight condition (Landgrebe, 1972).
Blade tip vortex trajectories were represented by Landgrebe (1972) as simple
analytical equations. The axial tip vortex path was modelled by two linear equations
which produced what is normally termed the classical two sloped linear path1. The
1Equation 1 of this presentation
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radial path was modelled with a first order exponential equation2. The work of
Kocurek et al (1977) improved these equations by considering parameters not
included in Landgrebes (1972) work.
Incorporation of the precise mean path of the wake as vortex filaments and of the
rotor blades as either segmented vortex filaments or vortex panels, led to the
development of Prescribed-Wake models for performance predictions (Kocureket al
1977, Reddy 1979). Limited availability of tip vortex trajectories produced by newly
designed rotors meant that a more generalised approach was required, in which the
vortex path did not have to be known. Free-Wake analysis methods were developed
(Clark et al 1970, Miller 1981, 1982), in which the tip vortex path was determined
by the time history of the induced velocities everywhere in the wake generated by
these vortex filaments.
Both Prescribed and Free-Wake methods have in the past two decades been
extensively used and improved to achieve better performance prediction accuracy.
But the studies of Reddy et al (1987) and Mba et al (1991), have shown that
performance predictions fall to within 5% by these two methods. Such apparent low
levels of uncertainty could lead to as much as 20% error in the estimation of
maximum payload (Clark et al, 1969). In trying to determine the parameters which
might cause such errors, the work of Reddy (1986) has shown that rotor thrust and
induced power are highly sensitive to small variations in tip vortex geometry. As
both methods depend greatly on the position of the wake, and as Free-Wake methods
place restrictions on the wake settling rates (Mba et al, 1991), one of the main causes
of such errors has been attributed to the inability of current wake vortex path models
to faithfully simulate the radial and axial tip vortex paths 3.
2Equation 6 of this presentation.
3In the work of Mba (1991), the vortex path was allowed to convect freely for the first revolution
of the rotor. Further downstream trajectories of the tip vortex were assumed to maintain the sameradial position with the axial rate equal to that at the end of the first revolution.
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1.2 WAKE PATH EQUATIONS
The current empirical equations used to describe tip vortex paths had their origins in
the work of Gray (1956, 1992) on single bladed rotors. He found that both the axial
and radial tip vortex paths could be easily represented by simple algebraic
expressions with very few measured parameters. The axial and radial paths of Grays
equation (1992) had the same format as equations 1 and 6 of this presentation.
However his radial equation had the extra term added to it. TheBe
1
sin()
multi-bladed nature of rotorcraft was considered by Landgrebe (1972) when he
derived the general forms of the parameters in Grays (1992) equations to account
for a wide range of rotor design and operating conditions4
. The extra term in Graysradial path equation may have been omitted due to blade aspect ratio on tip-shape
effects. The equations and parameters proposed by Landgrebe (1972) were only
simple generalised representations of the tip vortex trajectory during the first
revolution of the blade which produced it, neglecting the instabilities which arise
further downstream.
The work of Kocurek et al (1977) was able to incorporate the effects of number ofblades and twist to the parameters of the generalised equations of Landgrebe (1972).
The equations thus defined have remained unchanged and are still used as the
governing equations for the prediction of tip vortex paths of hovering rotors5. As
these equations are linear for the axial vortex path, and first order exponential for the
radial path, they produce a tip vortex structure which is everywhere symmetrical. The
research of Norman et al (1987) had demonstrated that hovering rotor wakes could
not be assumed to be symmetrical. The photographs reproduced in their publication
(Norman et al, 1987) revealed the instabilities in the tip vortices, the relationship
between tip vortex instability growth and increase in rotor thrust and the
asymmetrical structure of the vortex wake.
4Equation 2 of this presentation.
5Equations 3 and 8 of this presentation.
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Further investigation of hovering rotor wakes using the shadowgraph technique of
Swanson et al (1992) have corroborated the claim that tip vortex instabilities were
dependent on rotor thrust levels. The work of Swanson et al (1992) had also
formulated a relationship between tip vortex core growth rate and thrust coefficient
and another between vortex core growth rate and vortex age.
1.3 FLOW VISUALISATION TECHNIQUES
From the early years of rotorcraft research, flow visualisation investigations had been
carried out on rotor wakes in most flight regimes to observe and understand the
structure and behaviour of their tip vortex trajectories. The methods used for this type
of research have been various, some achieving great success. These were: Smoke-
filament technique (Gray 1992, Williams et al 1988, Landgrebe 1972), water-tank
technique (Jenks et al, 1987), small particle technique (Timm, 1965), schlieren
technique (Landgrebe 1972, Tangler et al 1973), shadowgraph technique (Norman et
al 1987, Swanson et al 1992, Bagai et al 1991, 1992(a), 1992(b)). Of these methods,
the smoke-filament and shadowgraph techniques have been the most successful.
However, in recent years, the shadowgraph technique has become the most widely
used. This has been due to its ability to accommodate large scale rotors operating at
Mach numbers greater than 0.45. Its success can be observed in the work of Norman
et al (1987) and Swanson et al (1992).
The smoke-filament technique has been shown by the results of this research to work
exceptionally well for rotors operating at low Mach numbers (M
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The aim of this thesis has been to study the radial and axial tip vortex paths of rotors
experiencing hover and axial flow using the smoke visualisation technique.
Compare the experimental tip vortex paths with trajectories generated by the
general equations formulated by Gray (1992), Landgrebe (1972) and Kocurek (1977).
Select an equation type which could better represent the mean vortex axial and
radial trajectories and determine its coefficients for the tested rotor configurations6.
Determine the meander of the vortex trajectories about their mean path, ascertain
the forms of instabilities present and determine their characteristics.
1.5 OUTLINE OF RESEARCH PRESENTATION
The proposed aims stated in the previous section have been substantially
accomplished. The different sections of this presentation describe more fully how this
was achieved.
The smoke flow visualisation technique was selected after careful consideration of
the experimental requirements and available resources. Chapter two examines in
detail the most common visualisation techniques and their suitability for the
requirements of this research.
Descriptions of available facilities, equipment used and the model test rotor have
been described in chapter three, together with detailed explanations of modifications
to the smoke filament technique and a full description of the experimental procedure.
The images produced by the smoke filament technique were recorded on video tape.
The processes involved in retreating each video frame and their enhancement
procedures to reveal the position of the tip vortex core were described in chapter
four.
The results of this research were described in chapter five, where the data obtained
was analysed to realise the aim of this work.
6 This study does not attempt to obtain a generalised tip vortex path equation, it only attempts to
determine a type of equation which could better represent the tip vortex mean path.
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Chapter
TWO
ROTOR WAKE VISUALISATION
2.0 INTRODUCTION
To understand the behaviour of rotor wakes, observations must be made of the basic
elements which constitute its structure, such as the tip vortex and vortex sheet. Such
observations have been made by researchers for many years (Lightfoot 1958, Landgrebe1972, Gray 1992). Visualisation techniques have been developed or reconfigured to
reveal the three dimensional characteristics of rotor wakes. This chapter describes the
suitability of the different visualisation techniques to rotor research.
2.1 SMOKE FILAMENT TECHNIQUE
This technique, used for low subsonic flow speeds, consisted of introducing into the
flow field one or more fine, turbulent free smoke filaments which follow the flow's path.
When illuminated, the smoke filaments reveal to the observer some characteristics of
the flow path.
The most common and safest method of smoke production requires kerosene or an
eucalyptus oil-based solution to be heated to boiling point and the vapours produced
mixed with air. On mixing, this produces a white cloud of smoke. A typical oil smoke
generator can be seen in figure 1.
The method of introducing smoke into the rotor's wake is very dependent on what part
of the flow the observer is interested in examining. The most common way of doing this
required the use of either a single tube (Williams et al, 1988) or a multi-tubed smoke
rake (Lightfoot 1958, Landgrebe 1972). Such a device allowed the smoke to be emitted
into the wake in a single plane. When illuminated with a stroboscopic light source, the
tip vortices and the trailing vortex sheets could be observed (figure 2). This method,
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Figure 1 : Typical oil smoke generator.
however, only allowed a two dimensional slice of the wake to be viewed at any one
time. To obtain a complete three dimensional image of the flow, pictures would need
to be taken at different azimuth positions and the results processed to construct a three
dimensional model of the wake.
A more direct way of viewing the full three dimensional wake can be achieved by
introducing smoke through the tip of the rotor blade. This can be done by forcing smoke
through ducts inside the blade, incorporated during the manufacturing process, and
exiting onto the tip. As the smoke leaves the blade tip, it becomes entrapped by the
strong tip vortex and travels downstream with it (Gray, 1992), revealing the wake
structure. The images produced resemble those obtained by either the schlieren or
shadowgraph techniques (Tangleret al1973,Norman et al1987). The rate at which
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smoke is introduced into the flow must be carefully regulated to diminish the effects of
flow injection into the tip vortex core. The work of Rinehart (1971) has shown that such
injections reduce the vortex swirl velocity component and their circulation strength as
they travel downstream. These effects alter the trajectory of the vortex, thus making the
results not representative of the rotor under investigation. Alternatively, the blade tips
could be manufactured to have a cavity filled with a porous material impregnated with
Titanium or Stannic Tetrachloride. Holes drilled at the tip would allow air to come into
contact with the solution, producing a dense white smoke which would escape from the
tip with negligible alteration to the vortex path.
Figure 2 : Smoke-flow visualisation of tip vortices,
with two vortex cores shown.
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Figure 3 : Dye-layer visualisation technique illuminated with
flood lights.
2.2 WATER TOWING TANK TECHNIQUE
The use of water in preference to air as the working medium has the advantage of no
recirculation problems, very low levels of turbulence and the capability of stratification
by means of a salinity gradient. The work of Jenks (1987) and Gad-el-Hak (1987) had
been aimed at investigating rotors in the forward flight regime and although the hover
flying regime would present obvious problems, rotors could still be studied at different
rates of climb. Figure 3 illustrates a possible arrangement for such a study. Towing tanks
of the types used by Jenks et al(1987), in which the water is stagnant and the model
moves, the recirculating type used by Sarpkaya (1971), where the water circulates and
the model is stationary, or the gravity fed type used by Werle (1986), where the water
flows by gravity draining, could all be used for this analysis. In these tanks, visualisation
of the flow would be better achieved by using food colour or fluorescent dyes. To
illuminate it, conventional flood lights or sheet laser light (Kogan et al1987) could be
used, the former providing overall views of the flow, the latter allowing for more detail
investigation of the flow region.
Introduction of the dyes into the flow field could be achieved in one of two ways, as
dye-layers or locally. If the dyes were introduced as layers, they would need to be placed
into the water as horizontal sheets prior to towing of the model. To achieve this a stable
density stratification would be necessary. Such a process would involve depositing
individual layers of water of slightly different density (controlled by the addition of salt),
one at a time in the tank. The water, once, settled would allow the layers to partially
diffuse into each other, establishing a continuous vertical gradient. To form the
horizontal sheet, a small diameter string saturated with dye crystals would be placed into
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Figure 4 : Dye-layer visualisation technique illuminated with a
laser sheet.
the tank and towed at a very low speed, allowing for the dye to be washed away from
the string as the water flows around it.
To introduce the dyes locally, they could either be pasted on to the rotor blades or be
discharged at the blade tips. If pasted, part of the blade would be covered with a dye
paste, and during the run this would dissolve directly off the blade and into the wake.
If discharged, the dyes would need to be introduced into the flow through small orifices
at the blade tips. These techniques require fresh water tanks (no density gradient),
having the advantage of allowing for large number of tests per day.
For rotor flow investigation with the dye-layer technique, figure 3 shows an arrangement
which could be implemented relatively easily. The rotor would need to be set
perpendicular to the towing direction, with its plane of symmetry coinciding with the
dye layer. When towed forward, the flow would be illuminated by either flood lights or
a laser sheet. If using flood lights, these would have to illuminate the dye-layer from
above (figure 3), but if the laser sheet were used, it would have to coincide with the dye
layer (figure 4). The camera would need to be positioned perpendicularly above the dye
layer (figures 3 & 4). If the localised dye technique were used, the dye would become
entrapped by the tip vortex, forming a helix like structure (figure 5) as the rotor is towed
through the tank. Although both illumination techniques could be used, the sheet of laser
light is preferred as it permits the helix to be viewed or filmed in different planes
parallel to the rotor's spinning axis (figure 5). As before, the camera would be located
perpendicularly above the sheet of laser light, focused on this plane. Due to the complex
nature of the flow, both means of dye introduction require the camera's shutter speed to
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be greater than the rotational speed of the rotor. This would be to enable the film to
capture the flow at various azimuthal blade positions.
Figure 5 : Localised-dye visualisation technique, with dye
discharged from blade tips and illuminated with a
laser sheet.
2.3 SMALL PARTICLES TECHNIQUE
In this technique, small solid particles would be introduced into the airstream and
observed by reflected or scattered light. The particles, however, would need to have low
inertia to follow the local direction of the fluid motion and not be affected by gravity.
In early work done on rotor wakes (Timm 1965), moderate success was achieved in
visualising the effects of obstacle-induced flow recirculation by using very small sugar
pine or spruce sawdust. Although in the work of Timm (1965), this technique worked
well, it had major disadvantages. The small size of the seeding particles created a lot of
debris which may remain floating in the air for some time. Such a situation could cause
health problems if the people operating the experiment were not suitably protected.
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Figure 6 : The Schlieren system.
2.4 SCHLIEREN TECHNIQUE
The basic Schlieren system, developed in 1864 by Tepler, is presented in figure 6.
Diverging light from a point source at A is converted into a parallel beam and passed
through the region of fluid to be viewed. The parallel beam then passes through another
lens and is focused at B, generating an image of the flow on the screen. Variations in the
working fluid's density cause the light rays to deviate from their original paths,
deflecting away from the focal point. When a knife edge is inserted at the focal point B,
rays that were deflected in one direction from the parallel would be prevented from
reaching the viewing screen. This elimination of rays from the image resulted in a
variation of illumination at the screen, which is proportional to the first derivative of the
density variation in the working fluid (Merzkirch 1987, Clancy 1978, Pope et al1965,
Pankhurst et al1965). Although the knife edge could be used in any orientation, if
placed perpendicular to the flow axis the density gradients will lighten or darken the
screen depending on their sign and on which side of the focal point B, the knife edge is
located. However, if orientated parallel to the flow, half the image would depict one
illumination pattern based on the density gradient whereas the other half would show
the reverse pattern for the same density gradient.
For rotor work investigation, more complex arrangements would be required. In the
work of Tangleret al(1973) a modified version of the ' Z ' configuration was used with
great success (figure 7). In such an arrangement, the lenses of figure 6 would be replaced
by two spherical or parabolic mirrors, enlarging somewhat the field of view. If greater
sensitivity were required, so that the vortex sheet could be viewed, the ' Double - Pass
Schlieren System ' could be used (figure 8). This system consists of a conical light
source passing twice through the working fluid.
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Figure 7 : Schematic diagram of the 'Z ' configuration Schlieren system.
Figure 8 : Double-pass Schlieren system
This system is very good for the visualisation of rotor wakes operating in the transonic
region (0.65 < M < 1.2), however its major drawback would be restrictions on the field
of view imposed by the size of the mirrors. Although this may be sufficient for rotors
of small diameter (Tangleret al1973), it would be inadequate for viewing wakes
generated by full scale rotors. If the wide-field schlieren system were used (Burton
1949) problems would be encountered in the manufacture of the large precision ruledgrids required.
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Figure 9 : Shadowgraph systems. (a) divergent light rays, (b) parallel light rays.
2.5 SHADOWGRAPH TECHNIQUE
The shadowgraph system, developed by Dovk in 1880, is the simplest optical
visualising process dependent on changes of the fluid refractive index, and has two
configurations. The optical elements required for configuration 1 (figure 9(a)) are a
high-intensity point light source (spark-electrode discharge (Bagai et al1992)) and a
retroreflective screen. For configuration 2, (figure 9(b)) the same equipment as for
configuration 1 would be used plus a lens or mirror. Both configurations could be used
for rotor wake visualisation, however, due to the large diameter of rotors, configuration
1 is better suited and more widespread (Bagai et al1992, Norman et al1987, Swanson
et al1992, Light et al1992).
The principle of the shadowgraph technique may be described as follows: As light rays
pass through a fluid medium of varying density, they will be deflected in proportion to
the density gradients (M/Mx). In regions where these gradients are constant, all light rays
will be deflected by the same amount and the light intensity at the screen will be
constant. In regions of the fluid where the gradients change, the deflection of light rayswill not be constant, altering the light intensity on the screen. Where the density
gradients increase (M /Mx > 0), the light rays will diverge, decreasing the illumination2 2
of the screen. Where the density gradients decrease, the light rays converge, increasing
the illumination on the screen.
For rotor wake investigation, it is customary to use configuration 1, with photographic
and video cameras to record the wake for quantitative analysis. Different optical
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Figure 10 : Typical shadowgraph set-up for rotor wake visualisation.
arrangements of the equipment can be observed in figures 10 and 11. The shadowgraph
arrangement of figure 10 has been successfully used in the past (Norman et al1987,
Swanson et al1992, Light et al1992), however in such systems the optical path of the
camera is "off-axis" to the incident light beam, resulting in the reflected light rays
travelling at slightly different angles to the incident rays. This causes two serious
problems. Firstly it produces a 'ghost' image which in some instances can obscure the
area of flow under scrutiny. Secondly, as the off-axis distance is increased, the intensity
of the reflected light back to the camera decreases almost exponentially with increasing
observation angle. It has been determined by Bagai et al(1992-a) that a change in the
observation angle by one degree would reduce the intensity of the light received by the
camera by a factor of 16.
To solve the problems associated with the off-axis alignment of the camera and light
source, Bagai et al(1992-a) performed experiments with the shadowgraph arrangement
of figure 11, with great success. By introducing a beam splitter they were able to achieve
a light intensity 4 times greater than for the previous arrangement, with the added effect
of permitting the use of higher camera shutter speeds and/or smaller lens apertures.
This technique has been very successful in visualising rotors operating at Mach numbers
greater than 0.65, and as research shows it has been the most frequently used technique
for full or near full scale rotor visualisation in recent years. However, as a distinctive
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Figure 11 : Improved wide-field shadowgraph set-up using a single beam splitter
(Bagai et al1992-a).
density gradient variation is required, the method doesn't suit rotors operating at low
Mach numbers (M < 0.3).
2.6 SHADOWGRAPH AND SCHLIEREN APPLICATIONS FOR ROTORSOPERATING AT LOW MACH NUMBERS
For studies on rotors operating at low Mach numbers, the density variation through the
wake becomes too low to be detected by methods dependent on changes in the fluid
refractive index. In the work of Townend (1931), two techniques were developed which
artificially altered the density of the fluid, permitting the shadowgraph and schlieren
systems to be used. The drawback of the system, however, is that forced changes in the
density of the fluid may cause its flow pattern to be altered.
2.6.1 Hot-Wire Technique
The technique consists of placing into the air stream a grid of fine electrically heated
wires. Their high temperature causes the density of the air passing over them to be
decreased, producing very fine streamlines of refractive index different to that of the
surrounding air. When such a pattern is illuminated by a stroboscopic light source in
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Although figures 12 and 13 were of flow generated by a propeller, they were7
displayed vertically to assist the reader in determining how the flow generated by ahovering rotor would appear when visualised using these techniques.
18
synchronisation with the spinning rotor, it would reveal a two dimensional view of the
wake, in a similar manner as the smoke filament technique. Figure 12 has been
reproduced from the work of Townend (1931), showing such a view .7
The grid recommended by Townend (1931) and Pankhurst et al (1965) should be
manufactured from platinum wire approximately 0.05 mm in diameter and between 13
to 26 mm long, with the individual wires set about 13 mm apart. The wire should be
heated to a dull red colour, requiring a 14 V battery and approximately 1 Amp for a flow
speed of approximately 10 m/s.
Figure 12 : Hot-wire shadowgraph photograph of flow
behind a propeller, (Townend 1931).
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2.6.2 Spark Technique
In this technique, a series of electric sparks are discharged into the flow causing small
volumes of air to be heated, and as was done for the Hot-Wire Technique, the paths of
these volumes could be tracked using the Shadowgraph or Schlieren Methods. These
volumes may be considered to be small enough to be thought of as particles. By using
synchronised stroboscopic light, the path of these particles could be determined, hence
supplying a time scale along the streamline from which the velocity at any point could
be determined. Again, as for the Hot-wire technique, the pictures produced represent a
two dimensional slice of the rotor's wake. Figure 13 has been reproduced from the work
of Townend (1931), showing such a view.
Figure 13 : Spark shadowgraph photograph of flow
behind a propeller, (Townend 1931).
Generation of the sparks could be achieved by the use of an ignition coil or an alternator.
In the work of Townend (1931), the latter method was found to be more favourable,
using a 0.5 h.p. alternator delivering 150 V at 2000 RPM. The output from the alternator
was then passed through a series resistance of about 100 ohms to a transformer which
stepped the voltage 100 times. The electrode was manufactured from oxidised piano
wire with a spark gap of approximately 9.5 mm.
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2.7 ALTERNATIVE VISUALISATION TECHNIQUES
The following direct and indirect methods of flow visualisation have not been widely
used, nor provide results of the calibre of the above mentioned techniques. However,
their unique means of producing quantitative wake trajectory data warrants a mention
in a review of different wake visualisation techniques.
2.7.1 Atmospheric Water Vapour Condensation
Under certain ideal conditions, the flow generated by a full scale rotor may be viewed
with the naked eye. The work of Jenney et al(1968) and Felkeret al(1986), has shown
that tip vortices could be seen on days of high humidity, with rotors operating in the
Ttransonic speed region (0.65 < M < 1.2) and at high thrust coefficients ( C > 0.16 ).
Under these conditions the water vapour in the air is condensed by the low-pressure
inside the vortex core, remaining visible for up to one and a half revolutions of the rotor.
2.7.2 Hot-Wire Anemometer Tracking
The methods described thus far comprise the direct flow visualisation techniques, where
one or more characteristics of the flow can be viewed by the observer as it happens. The
Hot-Wire Anemometer Tracking Technique, however is an indirect flow visualisation
method. In this technique, a hot wire probe is traversed radially through the wake at
different planes downstream of the rotor's tip path (figure 14). During each traverse it
records the radial position, axial distance behind the tip path, azimuthal position of the
blade with respect to the probe and the velocity profile signal. As the tip vortex can not
be seen, its location is determined when its core strikes the hot wire probe, producing
a very distinct dip (figure 15) in the velocity signal. On compilation of all the vortex
locations, the full tip vortex path can be reconstructed.
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Figure 14 : Typical arrangement for a radially traversing
hot-wire probe spinning with the rotor.
Figure 15 : Typical data indicating the position when the
vortex core strikes the hot-wire probe
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The only problem with this technique can be attributed to the unsteady nature of the tip
vortex. Due to the meandering of such vortices as they travel downstream, they become
almost impossible to locate, a problem experienced by Caradona et al(1981) when
using this technique.
2.7.3 Laser Velocimeter Tracking
This is also an indirect flow visualisation technique. In a similar way as for the Hot-
Wire technique, the velocity profile signal is measured at different radial and axial
positions. The vortex location is determined by the same dip in the velocity signal.
However, the velocity profile at each azimuth angle could be reconstructed from the
recorded signal to provide not only the tip vortex coordinates but also its size,
magnitude, and rate of growth or decay. This is illustrated in the results of figure 16,
obtained by Pouradieret al(1981). The technique, although more sophisticated than the
Hot-Wire, still has problems determining the vortex paths after one revolution due to
their meandering.
Figure 16 : Typical tip vortex path determination data.
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2.8 DISCUSSION
This chapter has given a brief overview of the many flow visualisation techniques which
could be applied to rotor wake investigation. In deciding the most suitable experimental
technique for this work, test parameters, equipment availability and rotor characteristics
were some of the factors considered.
The work of Caradona et al(1981), Light et al(1992) and Bagai et al(1991) have
shown that from the time a vortex is formed until the following blade passes over it, its
trajectory is approximately steady. But once the vortex from the following blade
develops the radial and axial paths of the previous vortex show a more erratic behaviour.
As this is the region of the flow of most interest in this study, both the Hot-Wire
Anemometer and Laser Velocimeter Tracking techniques could not be used.
Limitations on rotor size due to available wind tunnel facilities (see section 3.1.3), and
on the size of the drive unit (section 3.1.2) have restricted the operation of the rotor to
Tlow thrust coefficients (C < 0.01) and low Mach numbers (M < 0.25). These values
were too low for the Atmospheric Water Vapour Condensation, Schlieren and
Shadowgraph techniques. Although the Hot-Wire and Spark techniques could have beenused to assist the latter two techniques in revealing the wake, the density variation
within the working fluid caused by the nature of these techniques may have altered the
vortex trajectories.
The Small Particle Technique, although suitable for the test conditions, creates vast
amounts of debris, and as a Water Towing Tank was not readily available, the Smoke
Filament technique was selected as the technique for the visualisation of the model
rotor.
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Chapter
THREE
FLOW VISUALISATION
EXPERIMENT
3.1 EXPERIMENTAL EQUIPMENT
The facilities available at the time this project was initiated were not sufficient toaccommodate full scale investigation of rotor systems. For this reason, the decision was
made to use a small scale model rotor such as those used by Landgrebe (1972), Gray
(1992) and other researchers. Visualisation results obtained from such model rotors have
been successfully used by Landgrebe (1972), Gray (1992) and Kocureket al(1977) to
generate general vortex tip path equations for performance prediction of full scale rotors.
3.1.1 Model test rotor
The visualisation program involved subjecting the rotor to hover and positive climb
rates. Introduction of axial flow onto the rotor could only be achieved in the wind tunnel
of the Department of Aeronautical Engineering at the University of Sydney (section
3.1.3). Its size restricted the overall dimensions of the model rotor. Since the effect of
changing the parameters was not intended to be studied, a standard rectangular blade
with a NACA 0012 section was used. Table 1 lists the characteristics of the rotor system
tested.
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TABLE 1 : Model Rotor Characteristics
Number of Blades, b 4
Rotor Radius, R (m) 0.3145
Blade Chord, c (m) 0.0381Blade Root Cut Out (m) 0.08
Blade Twist (Deg) 0o
Blade Aspect Ratio, AR 6.15
Rotor Solidity, 0.1542
Blade Aerofoil NACA 0012
Blade Pitch Setting (Deg) 10o
Blade Taper Ratio 1.0Blade Tip Square
3.1.2 Rotor test stand
Testing of the rotor in the wind tunnel was achieved by the use of a test stand designed
and fabricated in the Department of Aeronautical Engineering. It was attached to the
wind tunnel balance, allowing the rotor thrust to be measured via the balance dragcomponent along the wind tunnel axis. For torque measurements, a strain gauge support
arm prevented the rotation of the drive relative to the test stand, however problems
associated with the size of the support arm prevented any such readings from being
taken.
The drive unit consisted of a 50 Watt electric motor with a speed adjustable up to 3000
RPM. The speed was controlled accurately by a variable voltage transformer. The
overall dimensions of the test stand are given in figure 17.
The rotor was mounted 0.8 m ahead of the wind tunnel supports to minimise any
interference effects between the rotor wake and the supports. This gave sufficient time
for the tip vortices in the wake to develop, become unstable and interact before
interference from the supports occurred.
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Figure 17 : Dimensioned diagram of the test rotor stand.
Figure 18 : Arrangement of smoke rake and test stand in wind tunnel.
3.1.3 Wind tunnel facilities
The experiments were carried out in the Department of Aeronautical Engineering's 7ft
x 5ft wind tunnel. It is a closed circuit tunnel operating at low speed, with atmospheric
pressure in the test section. For these experiments the normal closed test section wasremoved and the tunnel run in an open jet configuration, as shown in figure 18.
Introduction of the smoke into the flow was achieved by positioning the smoke rake
before the contraction region of the tunnel. This reduced any turbulence present as the
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27
smoke exited the rake. It was positioned vertically (figure 18), and facing downstream
towards the rotor. Its vertical position had to be altered every time the flow conditions
were changed. This allowed the smoke to highlight the tip and the trailing edge sheet
vortex.
3.1.4 Synchronisation equipment
Synchronisation of the blade cycle with the video recording camera was accomplished
using generally available electronic equipment. Figure 19 shows the layout of the test
stand and synchronisation equipment. To determine the rotational speed of the rotor, a
low intensity laser beam was aimed at a photoelectric cell. Its trajectory was close to the
rotor hub which had a small protruding arm parallel and offset from its rotational axis,
so that the beam could be interrupted once every revolution. Each interruption of the
beam caused the photoelectric cell to produce a step pulse which was transmitted to a
cathode-ray oscilloscope (CRO). The time between each pulse could be measured from
the CRO providing the rotational speed of the rotor. Also, the CRO was programmed
to produce a time delayed output signal which triggered the stroboscopic light source
at any intermediate azimuth angle for a complete revolution of the rotor. The flashes of
light produced by the stroboscopic unit were of high intensity and very short duration,less than 1/1000 of a second.th
The video camera used was a standard CCD model with reasonable low light level
recording capability and an effective shutter speed of about 1/25 of a second. Theth
combination of flash and shuttering speeds meant that the light sensitive elements of the
camera were illuminated for only a small fraction of the frame scan. The signal
amplitude was slightly low, but the frame was relatively free of the blurring that would
occur if a more intense strobe or continuous illumination was used.
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Figure 19 : Schematic diagram of the synchronisation equipment.
Figure 20 : Position of video camera in relation to
rotor.
3.2 EXPERIMENTAL PROCEDURE
Upon completion of the calibration process on the electronic flash equipment, the flow
visualisation and recording of the flow patterns was a reasonably simple procedure. The
most important step, however, was in the alignment of the video camera. It was locateda distance of 3 metres away from the rotor axis. It was set perpendicularly to the flow
direction and in the plane of the injected smoke (figure 20).
For each experiment, a calibration grid made of 30 mm squares was placed just behind
the rotor in the vertical plane passing through the rotor axis. The calibration grid was
recorded before and after each experiment was completed. Both records were used to
determine if the camera alignment had been altered during the experiment, and as a
position reference for the location of the vortex cores in the final processed images.
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Once the calibration grid was recorded, the rotor was set at the required rotational speed,
and when used, the wind tunnel was also set to the required speed. The smoke
streaklines were then introduced into the flow and illuminated by the synchronised
strobe light as they passed through or near the rotor. These illuminated flow patterns
were continuously recorded by the video camera.
Recordings were made at blade azimuth angle steps of between 10 and 15 for up to oneo o
full rotor revolution. At each azimuth setting the video recorded for an average of one
and a half minutes. This provided multiple frames of information for each required data
point and allowed the unsteady flow effects to be investigated and revealed in fine
detail.
3.3 DISCUSSION
The method of flow visualisation described in this chapter, although tedious and time
consuming, provided the most detailed information on the wake structure. When
reconstructing the axial and radial paths of the tip vortices, each vortex could be traced
back to the blade which generated it, thus enabling the path of each vortex to be
observed and studied individually, providing quantitative information on its oscillatorymotion, its instability, and its interactions with adjacent vortices.
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Chapter
FOUR
IMAGE PROCESSING
4.1 IMAGE DIGITISING
The recorded video images were played back through a standard video recorder and
appropriate frames were selected for processing. Individual frames were captured using
analog to digital conventional hardware connected to the serial port of a standard IBMcompatible personal computer.
The video digitising hardware was assembled locally within the Department of
Aeronautical Engineering and was based on a simple integrated circuit design (Circuit
Cellar Inc. 1987), using the CA3306 Flash A/D converter chip. The video signal was
scanned and its amplitude digitised to a stream of integer data. Each video frame
captured had a resolution of 256x244 picture elements (pels). Each element represented
a grey level with amplitudes in the range from 0 to 63. A sample digitised frame is
shown in figure 21. This equipment was chosen because of its simplicity and economy.
Once the digitised images had been transmitted to the computer they were stored as disk
files. A set of about 250 to 300 images were required to obtain an accurate vortex map
for a given rotor configuration. The first image processed was that of the reference grid.
A mapping was obtained between the grid points and the image picture elements. Using
this map, pel locations were translated into coordinate locations in the (YZ) vertical
plane passing through the axis of the rotor. The grid covering the whole video image
was mapped so that any picture distortions over the image area due to the camera or the
digitising process could be accounted for.
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Figure 21 : Digitised black and white video picture showing tip vortices,
vortex sheets and rotor blade.
4.2 IMAGE ENHANCEMENT
Several image processing techniques were applied to the captured video pictures in
order to enhance the images and thus more accurately locate the vortex cores. Several
initial methods used were based on edge detection filtering algorithms, such as that of
Seit et al(1988) and a much simpler outline algorithm described in the reference text
by Gonzales et al(1987). Using these processes, regions having a high intensity gradient
were brightened whereas regions of approximately constant amplitude were set to near
black. The result was typically an outline of the significant components contained within
the picture.
Because of the contrast between the dark vortex core and the bright smoke in the
rotating flow surrounding the core it was felt that the filtering technique would be most
appropriate. Pictures processed by this technique showed accurately the outline of the
rotor blade and the outlines of the smoke streaklines upstream of the rotor but were
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32
inconclusive in highlighting the vortex cores. In many cases only the initial blade tip
vortex could be seen with the successive helical spirals disappearing from the picture.
On closer examination of the video intensity levels near the vortices it was found that
the contrast between the core and the surrounding smoke rapidly diminished due to what
is assumed to be diffusion of smoke in the core.
A second processing technique was attempted by using false colour imaging of the
pictures. A computer program was written to convert the grey level image files into false
colour pictures (figure 22). The display hardware used on the computer was a Video
Graphics Array (VGA) so the limit of only 16 basic colours could be displayed.
However, by using the extra resolution of the VGA display (640x480), both VGA
display pages and a sequence of ditter patterns, it was possible to cover the range of 64
intensity levels within the original digitised frame.
Figure 22 : Digitised video picture with enhanced false colour imaging. Vortex
sheets, tip vortices and rotor blade easily identified.
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The screen images were further modified using the built-in hardware palette features of
the VGA display. The user could choose to have any one of the 16 screen colours
selected from a range of 64 RGB levels. In this way the smoke regions surrounding the
vortex cores were highlighted using false colour representation and thus the location of
the vortex was more easily distinguished.
Once the pattern of the circular vortex core had been recognised, its centroid position
was recorded as a row/column pel location and approximate diameter measured. Using
the digitised grid map the pel location was converted to a coordinate location (YZ) in
the plane perpendicular to the axis of the rotor. A single data point for the shed vortex
helix was obtained by combining the digitised coordinate location with the azimuth
angle for that particular frame. By superimposing all the vortex data points from one
frame with those of other frames recorded around a blade circuit, the path of each shed
vortex can be constructed in three dimensions.
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The axial flow speed relative to the lowest velocity coefficient value of 0.042 was8
2 m/s. Such a small axial velocity component would classify the rotor asexperiencing near pure hover conditions.
34
Chapter
FIVE
ROTOR WAKE GEOMETRIES
5.0 INTRODUCTION
The results obtained in this research were compared with the tip vortex path data
found in the work of Swanson et al(1992) and Bagai et al(1991, 1992-b). Blade tip
vortex axial and radial path data were plotted and compared with the paths generatedby the generalised vortex path equations of Landgrebe (1972) and Kocureket al
(1977). The paths which had evidence of vortex interaction were re-plotted with each
tip vortex marked; these were analysed and fitted with a mean path curve. The
meandering about this mean path was also plotted to determine the forms of
instability present.
5.1 WAKE RESULTS
Tip vortex path data for rotors in the hover regime was readily available from other
sources (Swanson et al1992, Bagai et al1992-b). For this reason experiments were
carried out with the rotor subjected to different rates of axial flow.
The hover tip vortex path data used came from the work of Bagai et al(1991, 1992-
b) and Swanson et al(1992). Most of their results had significant degrees of scatter
present to which the authors gave little significance. In wakes experiencing axial
flow, the tip vortex paths did not exhibit the scatter present in the hover wakes.
Hence experiments performed for this study were carried out at five different
vvelocity coefficients (C ), ranging from 0.042 to 0.18
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Table 2 : Rotor Test Parameters
v T TCase Figure C C C / Source
1 23 0.1 0.0018 0.012 Present Work
2 24 0.081 0.0042 0.027 Present Work 3 25 0.075 0.0048 0.031 Present Work
4 26 0.060 0.0063 0.041 Present Work
5 27 0.042 0.0078 0.051 Present Work
6 28 - 0.0074 0.08 Bagai et al(1992-b)
7 29 - 0.0113 0.099 Swanson et al(1992)
8 30 - 0.0167 0.146 Swanson et al(1992)
5.2 WAKE FEATURES
The tip vortex path data presented here show the important characteristics which the
equations formulated by Landgrebe (1972) and Kocureket al(1977) do not describe.
The most predominant feature can be observed in the wakes of rotors in pure hover.
The data of figures 27(b) through 30(b), representing the axial vortex paths, does not
in most cases follow the classical two sloped linear path. Instead, the axial vortex
path exhibited a smooth transition, from its trajectory immediately after being
generated to that after the following blade passed over it.
Once the vortex had passed its transition region, it maintained an almost constant
axial displacement rate for approximately 0.5 revolutions. Then the vortex could
follow one of two different axial paths, denoted by the forked shape of figures 27(b)
through 30(b). The significance of this was better understood when the paths of each
individual vortex filament was plotted (figures 31,32 and 33). These figures show
that as vortices are shed, they pair up with adjacent vortices and spin about a
common centre some distance between the two. As they move downstream, the
vortex cores move closer to each other, until they appear to both merge and diffuse.
In figures 31, 32 and 33, where this phenomenon can be observed, the axial paths
cross over each other approximately 1.13 and 1.33 revolutions after the vortex
formation.
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The tip vortex data reproduced from other sources (figures 28,29 & 30) did not
include the individual trajectories of each tip vortex produced by each rotor blade.
These vortex paths, however, behaved similarly to the vortex trajectory of the wake
with the lowest velocity coefficient (figure 27). The vortex path of figure 27 was
generated by combining the trajectories of all four vortices in the wake. To better
understand the behaviour of the wakes of the other researchers, a 'reverse' procedure
was performed on some of their data. The paths were very carefully studied and the
individual path of the three tip vortices of the wake of figure 30 were extracted and
re-plotted in figure 33. This figure shows the interaction between adjacent vortices.
In figure 33(b) the axial path of the vortex from blade 2 interacts with that of blade 3.
However at different times the vortex from blade 3 may interact with that of blade 1,
and that the vortex from blade 1 may interact with that of blade 2. Although it was
impossible to identify which blade generated each vortex, the selected arrangement
indicated that the axial crossing of the vortices generated by blades 2 and 3 occurred
after approximately 1.2 revolution in very good agreement with the experimental
results of this study.
In the work of Gray (1992), Landgrebe (1972) and Kocureket al(977), the radial
paths appeared to possess only smoothly defined trajectories. The hover tip vortexpaths presented here, however, enclosed a region formed approximately 0.75
revolutions after the vortex formation. When each individual radial vortex path was
plotted (figures 32(a), 33(a)), adjacent vortices crossed over each other between 0.67
and 0.75 revolutions after being formed, approximately half the time taken for the
axial paths to cross over. This is indicative of the spin rate of the two entrapped
vortices. On more careful examination of figure 31(a), the rate of spin diminished as
the vortices moved closer together and further downstream. This is verified by the
next vortex radial cross-over which occurred between 0.88 and 1.08 revolutions after
the first crossing, alternatively, the spin rate has slowed down by between 35% and
44%. The reason for such a reduction in rotational speed is not known, but a
proposed cause might be that as vortices become entrapped in each other's field, their
strength and similar rotational sense produce a detrimental interaction , causing them
to loose strength and diffuse.
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When the tip vortices were subjected to axial flow (figures 23 through 26), both the
radial and axial paths were significantly changed. The two-gradient axial trajectories
vanished and were replaced by a single path of almost constant gradient, but far
greater than those predicted by the equations of Landgrebe (1972) and Kocureket al
(1977). Such a change in the axial path was expected as the vortices experience axial
flow which carries them downstream at a constant speed, with a stabilising effect on
the wake structure.
The radial vortex paths are also significantly affected by the axial flow. Figures 23(a)
through 26(a), show that the vortices follow the general trajectory predicted by the
generalised equations for 0.125 revolutions after being formed, then the vortex
becomes affected by the axial flow and the radial paths are diverted away from its
predicted path. They become more linear, with a very small contraction gradient
which appeared to be dependent in the velocity and thrust coefficients. These paths
no longer cross over one another and are very stable, with a considerable less scatter
of points than in the pure hover case.
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Figure 23(b) : Comparison between experimental and predicted wake
geometries; (a) radial, (b) axial.
Figure 23(a)
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Figure 24(b) : Comparison between experimental and predicted wake
geometries; (a) radial, (b) axial.
Figure 24(a)
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Figure 25(b) : Comparison between experimental and predicted wake
geometries; (a) radial, (b) axial.
Figure 25(a)
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Figure 26(b) : Comparison between experimental and predicted wake
geometries; (a) radial, (b) axial.
Figure 26(a)
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Figure 27(b) : Comparison between experimental and predicted wake
geometries; (a) radial, (b) axial.
Figure 27(a)
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Figure 28(b) : Comparison between the experimental wake of Bagai et al
(1992-b) and predicted wake geometries; (a) radial, (b) axial.
Figure 28(a)
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Figure 29(b) : Comparison between the experimental wake of Swanson et al
(1992) and predicted wake geometry; (a) radial, (b) axial.
Figure 29(a)
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Figure 30(b) : Comparison between the experimental wake of Swanson et al
(1992) and predicted wake geometry; (a) radial, (b) axial
Figure 30(a)
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Figure 31(b) : Individual vortex trajectories of the four vortices from the wake
of figure 27.
Figure 31(a)
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Figure 32(b) : Individual vortex trajectories of the two vortices from the wake
of figure 28.
Figure 32(a)
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Figure 33(b) : Individual vortex trajectories of the three vortices from the wake
of figure 30.
Figure 33(a)
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5.3 WAKE INSTABILITIES
The presence of instabilities in rotor wakes have always been known to exist. In the
work of Landgrebe (1972), Gray (1956), Kocureket al(1977), Swanson et al(1992)
and Bagai et al(1992-b), these instabilities had been revealed by the visualisation
methods employed, and appeared to be related to the rotor's thrust. However, no
detailed experimental analysis appeared to have been done which attempted to
explain the causes and modes of these instabilities.
Theoretical studies have, however, been carried out on the stability of curved,
(Betchov 1965), and helical, (Widnall 1972), vortex filaments. The analysis of
Betchov (1965) showed that helical vortex filaments were unstable for perturbation
wavelengths longer than 2 times the local radius of curvature of the unperturbed
filament and stable for shorter waves. The work of Widnall (1972) verified this mode
of instability, but in performing a more thorough study of helical vortex wakes,
discovered two additional modes influenced by the entire vortex filament.
The investigation performed by Widnall (1972) on the stability of a helical vortexfilament following small sinusoidal displacements of its centre-line, consisted of
evaluating the self-induced velocities at the filament due to these perturbations.
These were then used kinematically to determine the resulting motion of the filament
and thus the growth rate of the perturbations. The results obtained showed three
distinct types of instabilities present in helical vortex filaments:
(1) Short-Wave Instability, where the number of oscillatory waves percycle (/k') is very high.
(2) Mutual-Inductance or Low-Wave Number Instability, where the
number of oscillatory waves per cycle are less than the pitch of the
helix (kR).
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(3) Long-Wave Instability, where successive turns of the vortex pass
within the distance of one radius from each other, ie: where the pitch
3of the helix is greater than or equal to 3 / .1
A sketch of the typical mode shapes for the various instabilities is given in figure 34,
2showing the short-wave instability, the mutual-inductance modes with /k' = / and5
2 2/ , and the long-wave instability with /k' = / . With the mutual-inductance3 1
instability the neighbouring filaments attempt to roll-up around one another in much
the same way as hovering rotor vortices do.
Figure 34 : Instability mode shapes; the short-wave instability, the
2 2mutual-inductance modes with /k' = / and / , and the5 3
2long-wave instability with /k' = / . The dark portions are1
outside the cylinder on the near side; the light portions are
inside. Reproduced from Widnall (1972).
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From his analysis, Widnall (1972) was able to obtain stability boundaries as function
vof helix pitch (kR), number of waves per cycle (/k') and vortex core radius (r /R).
These results for various core size ratios can be seen in figure 35. The general trends
for the stability boundary for a given core size were determined by Widnall (1972) to
be as follows:
For kR below some critical value two instability modes are present, the
Short-Wave mode and the Local-Induction instability; with increasing kR
(decreasing pitch), the Mutual-Inductance modes become unstable; with
further increases in kR the Mutual-Inductance modes merge and the helix is
unstable for almost all wavelengths. It is always stable for /k'/ 1 and there
is an upper boundary for the short-wave instability for any vortex core size.
In the limit of very, very small core sizes, wave numbers smaller than the
local circumference are unstable.
Figure 35 : Stability boundaries for helical vortex filaments of finite core. The
value of the ratio of core-to-cylinder radius are shown on each curve.
Above the boundary, the helical filament of that core size is unstable.
Reproduced from Widnall (1972).
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These statements imply that irrespective of vortex core size or helix pitch, helical
vortices are inherently unstable, the mode of instability dependent on the form of the
disturbance applied and on the helix's own structure. In relating these instability
criterion to rotor wakes, the following criterion for vortex stability were suggested:
(1) All rotor wakes in the hover or climb regime experience some sort of
tip vortex instability.
(2) Although in the work of Betchov (1965) and Widnall (1972),
damping effects were not accounted for, wakes experiencing Short-
Wake, Mutual-Inductance and Long-Wave instabilities, may beaffected by fluid damping to the extent of having the instabilities
suppressed completely or maintained but in a quasi-stable state.
(3) Increases in rotor thrust have been proven by Swanson et al(1992), to
cause the tip vortex core size to increase significantly, whilst having
comparatively small effects on the pitch of the helix. This means that
a wake with vortices in a quasi-stable state could become unstable
when the thrust is increased.
(4) Rotors producing high thrust have large vortex core sizes which result
in Mutual-Inductance instabilities becoming predominant, causing
adjacent vortices to pair up and spin together.
(5) Very heavily loaded rotors have completely unstable wakes with all
modes of instabilities present.
(6) The growth in size of the vortex core as it travels downstream has
been shown by the work of Thomson (1988) and Swanson et al1992.
This means that vortices formed under quasi-steady conditions could
become unstable and diffuse as they move further downstream.
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(1)
(7) Helical vortices excited with a perturbation occurring once per cycle
(/k' / 1) are inherently stable. It is therefore apparent that single
bladed rotors, which have a Mutual-Inductance induced disturbance
of once per revolution, should have very stable wakes. The
experimental results of Gray (1972) on single bladed rotors, show that
the axial and radial paths were very smooth and suffer from no major
2oscillatory motions, existing for over 3 / revolutions, far more than1
in any multi-bladed rotor.
5.4 GENERALISED WAKE THEORY
When observing figures 23 through 30, it become obvious that the semi-empirical
equations of Landgrebe (1972) and Kocureket al(1977) are in most instances unable
to accurately predict the vortex path. For these reasons one of the major tasks of this
research has been to identify equations which could better represent the mean vortex
path.
This research did not at any stage attempt to define generalised equations for
different rotor characteristics or working conditions. Such a task would require
extensive research, and facilities not available to the author. Instead, the forms of
these equations has been identified.
5.4.1 Tip vortex mean axial path equation
The vortex axial path equations in current use are:
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(2)
(3)
for Landgrebe's model:
for Kocurek's model:
where:
These equations have provided very good linear approximations for the axial vortex tip
path. However, they over simplify the complex nature of the vortex trajectory, because:
(1) They assume the vortex axial path to be linear.
(2) They imply that the rate of change of the gradient along the vortex path
to be zero everywhere, except where the following blade passes over it.
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(4)
(5)
At such a time and for an infinitesimal amount of time it has a positive
value.
(3) They assume the vortices to have no instabilities or fluctuations about
their mean path.
(4) They do not account for vortices pairing up and spinning.
For this reason, it became necessary to find new semi-empirical equations which could
better represent the vortex axial path. The characteristics of such a path were discovered
to be better modelled by exponential equations. The two forms selected were:
where:
= Wake Azimuth angle relative to blade (Radians)
= Function Ln(+1),1 was added to the angle to accommodate for = 0r
A,B,C,.. = Constants determined using the least squares method.
To determine the coefficients A,B,C,..., etc., the least squares method was used . It is
envisaged that when sufficient wake vortex data becomes available, general equations
accommodating all rotor characteristics and flight conditions may be derived.
When these equations were compared with the experimental axial vortex path, equation (5)
provided the better approximation to the mean path. The reason for this was that it
required two to three terms less than equation (4), providing a smoother mean axial vortex
path rather than an equation which tried to follow every data point.
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In pure hover conditions, the axial paths of the tip vortices cross over each other. Hence
two equations representing the wake may be required for each set of rotor parameters.
These coalesce into one curve, as axial flow is introduced into the flow.
The maximum number of terms necessary to provide a reasonable mean path using
equation (5) has been determined to be between three and five. Typical values of these can
be seen in the figures of the following section.
5.4.2 Axial path instability criterion
Each of the wakes listed in table 2 have been individually analysed to determine theinstabilities in the axial path of the vortices and how these became affected by the
introduction of axial flow. The individual vortex filaments of each wake were fitted with
their mean path curve, followed by a plot of the meandering about their mean path. This
was defined as the ratio between the difference of the actual axial vortex position and the
mean axial path to the rotor radius, plotted as a function of the azimuth angle. Due to the
large number of filaments produced, only one from each wake has been reproduced in the
following figures. These include the axial vortex path data, the mean path curve, the
coefficients of the equation, and the meandering about the mean path.
The important trends to observe in these figures is the meandering. From the analogies
described in section 5.3 of this presentation, the axial paths show evidence of Short-Wave,
Mutual-Inductance and Long-Wave instabilities. Figure 41(b) shows the once-per-blade
passage excitation induced by the forming vortex, clearly indicating the Mutual-Inductance
effect. Figures 36(b) through 40(b) show more clearly the Short-Wave instability which in
most instances appears to grow as the vortex moves downstream. Mutual-Inductance and
Long-Wave instability can also be seen. Both forms of instability appear to become much
more erratic after the vortex has been in existence for more than 1.25 revolutions. As the
axial flow is increased, the Short-Wave instabilities become affected by the fluid's
damping, leaving the Mutual-Inductance instability prominent, although also affected by
the damping.
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Figure 36(a) : Axial wake geometry and mean axial path.
Figure 36(b) : Meander of vortex about mean axial path.
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Figure 37(a) : Axial wake geometry and mean axial path.
Figure 37(b) : Meander of vortex about mean axial path.
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Figure 38(a) : Axial wake geometry and mean axial path.
Figure 38(b) : Meander of vortex about mean axial path.
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Figure 39(a) : Axial wake geometry and mean axial path.
Figure 39(b) : Meander of vortex about mean axial path.
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Figure 40(a) : Axial wake geometry and mean axial path.
Figure 40(b) : Meander of vortex about mean axial path.
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Figure 41(a) : Axial wake geometry and mean axial path.
Figure 41(b) : Meander of vortex about mean axial path.
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(6)
(7)
(8)
(9)
(10)
5.4.3 Tip vortex mean radial path equation
The tip vortex mean radial path equations in current use are:
for Landgrebe's model:
for Kocurek's model:
These equations, although providing a good first order exponential approximation to the
radial paths of the vortex filaments, did not model some of the important characteristics of
the vortex radial path, such as:
(1) The unstable path of the radial vortex path.
(2) The interactions and pairing between adjacent vortices.
(3) The trajectories of each individual blade tip vortex.
(4) The effect of induced axial flow in the wake to the radial vortex path.
In selecting the equation which could better represent the radial vortex path, exponential
equations were the better suited. The two forms selected were:
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where:
= Wake Azimuth angle relative to blade (Radians)
= Function Ln(+1), 1 was added to the angle to accommodate = 0r
A,B,C,.. = Constants determined using the least squares method.
As for the axial equations it is hoped that the coefficients may in future be determined as
functions of rotor parameters and flying conditions. However for the present work the least
squares method was used to find the mean path for each individual vortex filament. The
form of the exponential equation chosen was equation (10), requiring only two or three
terms to give the smoothest mean path, compared with equation (9) which required five tosix terms.
5.4.4 Radial path instability criterion
As for the axial component of the path, all vortex filaments for each of the wakes listed in
table 2 were analysed and only one from each wake was included in the figures which
follow. These figures contained the radial vortex path, the mean radial path curve and
equation, and their meander about the mean path. As before the meander was defined as the
ratio between the difference of the actual radial vortex position and the mean radial path to
the rotor radius, plotted as a function of azimuth angle.
The behaviour of the vortices radially shows evidence of all three types of instabilities.
Long-Wave instabilities could observed in figures 31(a) through 33(a), where adjacent
vortex filaments interact and spin about one another.
When the meandering about the mean path was studied, both Short -Wake and Mutual-
Inductance were observed to be present. However, the Mutual-Inductance appeared to be
heavily damped. The Short-Wave instability was also damped but maintained in an almost