2010_mourad_thermo-mechanical characteristics of thermally aged
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Thermo-mechanical characteristics of thermally aged
polyethylene/polypropylene blends
Abdel-Hamid I. Mourad*,1
Mechanical Engineering Department, United Arab Emirates University, Al-Ain, P.O. Box 17555, United Arab Emirates
a r t i c l e i n f o
Article history:Received 11 April 2009
Accepted 20 July 2009
Available online 23 July 2009
Keywords:
Polyethylene/polypropylene blends
Blend ratio
Mechanical properties
Thermal aging
Thermogravimetric analysis (TGA)
a b s t r a c t
Polyethylene (PE), polypropylene (PP) and their blends have attracted a lot of attention due to theirpotential industrial applications. Therefore, the current work has been carried out with the main objec-
tive of investigating the impact of the thermal aging/treatment and blend ratio (composition range) on
the mechanical (tensile and hardness) and thermal characteristics (using thermogravimetric analysis
in a dynamic air atmosphere) of PE, PP and PE/PP binary blends. Samples of PE/PP blends containing
100/00, 75/25, 50/50, 25/75 and 0/100 wt.% were prepared via injection moulding technique and ther-
mally treated/aged at 100 °C for 0, 2, 4, 7, 14 days. The tensile measurements indicated that the yield
strength and the modulus decrease with increasing PE content. It was also observed that PE, PP and their
blends deform in ductile modes. They undergo a uniform yielding over a wide range of deformation,
which is followed by strainhardeningand then failure. The strainto break forpure PE is found to be much
higher than that for pure PP and for their blends, intermediate values have been observed. The hardness
measurements have also revealed that increasing PE content in PE/PP blends reduced the hardness value
of PP, however, thermal aging at 100 °C has not affected the polymers hardness which holds also true for
the tensile properties, showing a good correlation between tested mechanical properties. The thermo-
gravimetric analysis (TGA) in a dynamic air atmosphere and derivative thermogravimetric analysis
(DTA) were conducted to study the thermal degradation and stability of thermally unaged and aged
PE, PP and PE/PP blends in terms of the initial (T d and T d(1%)) and final (T d(99%)) decomposition tempera-tures and maximum decomposition rate temperature (T max). All polymers start to decompose at no less
than 365 °C. As for mechanical properties, the blend ratio has affected the thermal properties however,
aging time has not.
Ó 2009 Elsevier Ltd. All rights reserved.
1. Introduction
In the last few decades, polymers have been widely used mate-
rials in industry and their utilization in engineering applications is
widely growing all over the world. Their versatility makes them
suitable for a whole range of applications, and comes from the
capability of manufacturers to tailor microstructures and therefore
properties through control of the processing conditions. As an
example, the use of plastic pipes in piping systems applications
[1] (pressure vessels and in pipelines for potable water, irrigation,
and sewage) represent an important area in which polymers are
becoming predominant against other materials and has increases
considerably and rapidly. Pipes made out from polymers have sev-
eral special features in comparison to metallic pipes. Their rela-
tively low cost, ease of installation, transportation, and long-term
durability against environmental degradation (harmful environ-
mental attack such as corrosion, rust and higher thermal stresses)
make plastics an attractive alternative to metals in such applica-
tions). Among the most common polymers utilized in such applica-
tions are polyethylene (PE) and polypropylene (PP).
Though, polymers have offered many useful advantages over
metals (they have in general good thermal and electrical insulation
properties, low density and high resistance to chemicals), but they
are mechanically weaker and exhibit lower elastic modulus than
metals. In order to overcome these limitations, numerous studies
have been carried out in the recent years to improve the mechan-
ical behaviour of polymers, e.g. [2–6]. There have been also a large
number of reports describing the methods for producing polymers
with improved properties, e.g., polymer blending, in the form of
rods, sheets and tubes.
Blending of different plastic resins has long been practiced in the
manufacturing industry for various reasons including: (i) tailor-
made blends to meet specific processing and performance require-
ments that cannot be satisfied by a single component; (ii) blending
of polymers can be used in the field of recycling post-consumer
0261-3069/$ - see front matter Ó 2009 Elsevier Ltd. All rights reserved.doi:10.1016/j.matdes.2009.07.031
* Tel.: +971 3 7133574; fax: +971 3 7623158.
E-mail address: [email protected] On leave from Mechanical Design Department, Faculty of Engineering, El-Mataria,
Helwan University, P.O. Box 11718, Cairo, Egypt.
Materials and Design 31 (2010) 918–929
Contents lists available at ScienceDirect
Materials and Design
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wastes to upgrade their properties, (iii) scientific interests; and (iv)
financial incentives [7].
As generally known, having fast-growing application areas,
polyolefin are the most widely used cheap plastic materials [8,9].
Polyethylene (PE) and polypropylene (PP) are of considerable
industrial relevance, especially in the form of a blend. Over the
years, their blends are among those binary systems that have at-
tracted a lot of attention.
Jose et al. [10] investigated the phase morphology, crystallisa-
tion behaviour and mechanical properties of isotactic polypropyl-
ene (i-PP)/high density polyethylene (HDPE) blends. They used
different compositions of blends, namely, i-PP and HDPE (H10,
H20, H30, H40, H50, H60, H70, H80 and H90), where H denotes HDPE
and subscript denotes the percentage composition by weight of
HDPE. They found that the properties are related to each other.
They have found that, as the percentage of HDPE increased the size
of the dispersed HDPE domains increased due to the coalescence
phenomenon [11]. Jose et al. measured the mechanical properties
of the PP/HDPE blends (tensile strength, tensile strength at break,
elongation at break, impact strength, hardness and tear strength).
They also reported that, all the properties except Young’s modulus
and hardness showed negative deviation from the additivity line
and minimum values of mechanical properties are observed for
blends exhibiting co-continuous morphology. This is due to the
incompatibility of these blends. The most important result they
have found is the variation of Young’s modulus with composition,
which shows a positive synergism with maximum corresponding
to 80% PP. This behaviour was explained by considering both the
morphology and crystallinity of the blends.
The mechanical behaviour/tensile properties, morphology and
crystallisation from the melt of high density polyethylene
(HDPE)/syndiotactic polypropylene (sPP) blends were investigated
byLooset al. [12]. They found that the mechanical behaviour of the
blends changed drastically compared to pure HDPE and sPP, and
for HDPE concentrations between 10 and 70 wt.%, they found that
no neck formation was observed. Both pure sPP and pure HDPE
showed usual plastic deformation via necking with elongationse% 300–800%. But already for samples containing only 5 wt.%
HDPE, the drawing behaviour of the blends changed, and for the
90/10 blend samples, brittle fracture took place before necking
after approximately 10% elongation. For low concentrations of
HDPE, a synergetic increase in the Young’s modulus with a maxi-
mum of about 20 wt.% HDPE was measuredand for blends contain-
ing more than 20 wt.% HDPE a slight decrease in tensile strength
was observed. The crystallization behaviour of these blends was
characterized by transmission electron microscopy and in situ
Raman spectroscopy. For all investigated sPP/HDPE blends, the
start temperature of the sPP crystallization significantly increased
with increasing HDPE content. The start temperature of crystalliza-
tion increases more than 10 °C when HDPE was present, which re-
flected the favoured nucleation of sPP in the blends.Study and characterization of virgin and recycled LDPE/PP
blends were carried out by Bertin and Robin [7]. First, they made
a model composition of virgin LDPE/PP blend to study the effect
of process parameters and that of different types of compatibiliz-
ers. Second, they applied the results to plastic wastes coming from
industrial post-consumer plastic wastes. By adding compatibilizing
agents, elongation at break and impact strength were improved for
all blends. The effect of these various copolymers was different and
was related to chemical structure. The recycled blends exhibited
suitable properties, which lead to applications that require good
mechanical properties. In the specific case of LDPE/PP blends, EP-
CAR 847 (EPM) was used as a compatibilizer. Its presence in the
blend efficiently improved the elongation at break and decreased
the Young’s modulus [13]. Some EPDM and EPM grafted withmaleic anhydride (EPDM-g-MAH) were tested to compatibilize
LDPE/PP blends [14–16]. Also, the addition of fibers, such as short
polyamide fibers, in LDPE/PP blends allowed the improvement of
tensile, flexural and impact behaviour [17].
The characteristics of polypropylene/polyethylene (PP/PE) bin-
ary blends at the microscopic level have been widely studied by
different researchers over the years. Wong and Lam [18] discussed
the empirical results obtained from a series of DSC and TGA tests
on the selected thermal properties of PP/PE blends. They usedDSC to investigate the effects of different blending ratios of PP
and PE on the melting and crystallinity behaviour of the blend sys-
tems. TGA was used to study the degradation properties of the
blends in terms of their induction time. An empirical equation
was proposed and was proved to offer a convenient means for
the estimation of the overall crystallinity percent of a PP/PE sys-
tem. The TGA study showed that the effect of temperature on
induction time of PP/PE blends followed the trend of the Arrhenius
equation.
One of the most obvious effects brought about by the blending
process is the density of the blends. A Techne Density Gradient Col-
umn was employed by Wong [19] for density measurement. He
found that the density of the blends may be accurately described
by an additive rule that was reported to be applicable for PP/PE
systems.
Blom et al. [20] investigated the mechanical and rheological
properties of PP/HDPE blends. In this investigation, the properties
of two types of PP/PE blends (PP/HDPE and PP/LDPE) were studied.
The PE contents in both types of blends were kept at a low percent-
ageÀ20 wt.%.
In general, in systems composed of two polymers the tensile
strength depends linearly on the concentration of one component,
but antagonistic and synergistic effects were also reported [21].
Incompatible and immiscible polymers may exhibit a broad mini-
mum in tensile strength over the composition [22]. The term
‘immiscible’ means that the Gibbs free energy of mixingDGm is po-
sitive, whereas ‘incompatible’ is defined with respect to properties
and means that the properties of the blend are inferior to those of
the pure polymers. Since polyethylene and polypropylene aregenerally immiscible and incompatible [23,24], their mixtures are
expected to be poor in mechanical properties. However, the high
density polyethylene (HDPE)/isotactic polypropylene (i-PP) blend
is one of the few immiscible systems which has a maximum in ten-
sile strength at a certain composition [22], i.e., it is not incompati-
ble. Moreover, the addition of a small amount HDPE into i-PP
improves the impact strength of i-PP [25], and the addition of a
small amount of i-PP into HDPE enhances the transparency of solid
PE [26] (at the expense of environmental stress cracking resis-
tance). These effects depend on the blend preparation conditions.
For HDPE/i-PP blend samples, a surprisingly high impact strength
compared to the single components was observed at a specific
range of HDPE content. This phenomenon raises questions as to
thestructure, morphology and theinterphasesbetween thecompo-nents and their possible correlation with the impact strength [27].
Mechanical properties, structure and morphology of high den-
sity polyethylene (HDPE) and isotactic polypropylene (i-PP) blends
were studied by Schurmann et al. [27]. Young’s modulus was mea-
sured for blends with a wide range of compositions. Evidently their
values follow the mixing rule over the whole range, and the com-
patibilizer had almost no effect. The impact strength, however,
exhibited a very pronounced deviation from a simple linear depen-
dence [27]. The blends exhibit a maximum in impact strength at
specific mixing ratios. An explanation was found by analysing the
morphology. For a mixing ratio of 60% HDPE/40% i-PP, the impact
strength was twice as high as for the single component i-PP. For
the blends containing a compatibilizer (ethylene–propylene
copolymer), the impact strength became five times higher thanthat of i-PP and 10 times higher than that of HDPE [27].
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Waldman and De Paoli [28] reported the thermomechanical
degradation of (i-PP) and (LDPE), and the effect of the specific deg-
radation processes of each polymer on the degradation of a 1:1
blend of these polymers by using a conrotatory double-screw mix-
er coupled to a torque rheometer. The products were characterized
by Fourier transform infra-red spectroscopy and thermogravimetry
under inert and oxidative atmospheres. Data for the blends were
compared with curves simulated from a combination of the results
for the single polymers. LDPE was shown to form 3–4 times more
carbonyl-containing products than i-PP in the processing condi-
tions used to prepare the blend. The main reason for this difference
was the stabilizers added to i-PP by the producer before its pellet-
ization. Blending with LDPE stabilized i-PP, even at temperatures
well above its melting point.
Kesari and Salovery [29] studied the mechanical behaviour of
ternary blends of polyethylene (PE), isotactic polypropylene (PP)
and ethylene–propylene-diene terpolymer (EPDM). The variation
of the tensile and impact behaviour of compression mould ternary
blends with compression moulding time was reported. The blends
showed variations in tensile and impact behaviour after periods of
compression moulding. These variations resulted from changes in
structure. Changes in the mechanical behaviour were associated
with rearrangements of phase morphology in the blends due to
the compression moulding process. They also reported that ternary
blends of PP/PE/EPDM are complex mixtures of immiscible phases,
crystalline spherulites, and amorphous domains.
Although the polyolefin phases in the ternary blends are immis-
cible, considerable interaction occurs between the phases [30]. For
example, the effect of amorphous ethylene–propylene copolymers
on spherulitic crystallization in isotactic PP was described [31], and
considerable synergism in mechanical behaviour was reported for
PP–PE binary blends. Moreover, the mechanical properties of such
binary blends were very sensitive to processing [32]. Unlike binary
blends of PE and PP which do not show an evidence for adhesion
between dispersed PE droplets and PP matrix, ternary blends with
a random ethylene–propylene copolymer indicated adhesion be-
tween the composite droplets and the matrix [33].Rubbery polymers such as EPDM are frequently added to glassy
or semicrystalline polymers to enhance the impact resistance [30].
Morphological changes that affect the size and composition of the
dispersed phase should alter the mechanical properties. Here we
report the variation of the mechanical properties with the blend
compositions and the thermal treatment period.
In the study of Kukaleva et al. [34], homoPP, coPP and LDPE
were blended with recycled HDPE (wt.% = 75 and higher). They at-
tempted to produce blends of these polyolefins that are suitable for
large-scale moulding and are capable of providing appropriate
physical properties without the use of compatibilisers. The data
from MDSC experiments showed that, only one peak at 130.3 °C
[T m(HDPE)=132.2 °C and T m(LDPE)=106.4 °C] was present in the to-
tal heat-flow curve of 85HDPE/15LDPE blend on melting and oncrystallization, which is unexpected: the miscibility of linear and
branched types of polyethylene is a rare phenomenon. They spec-
ulated that the recycled HDPE was more compatible with LDPE
than virgin HDPE and this might be explained by the less regular
molecular structure and higher polydispersity index of the former
resulting from oxidation and chain scission undergone during
material’s reprocessing. The main conclusion from their MDSC re-
sults was that the presence of some partial miscibility in the solid
state may be suggested in blends–H1/LDPE, H1/coPP, H1/LDPE/
homoPP, but not in the H1/homoPP blend. They also concluded
that the blends were mechanically compatible, i.e., they are capa-
ble of providing compositions with a good balance of stiffness
and toughness. The degree of compatibility was the highest for
the recycled HDPE/LDPE blend, followed by the ternary blend recy-cled HDPE/LD/homoPP and recycled HDPE/coPP blend, and then
the recycled HDPE/homoPP blend. Although the last blend is the
least compatible system, simultaneous crystallization of its com-
ponents and the decreased PP crystallinity in the blend provided
better toughness than normally expected from the HDPE/PP
combination.
Although polymers are, nowadays, widely used in many struc-
tural products given their low costs and ease of processing, the
end use in engineering applications is often restricted by their
macroscopic mechanical performance. Mechanical properties such
as impact strength, tensile strength, Young’s modulus, strength and
elongation at the stretching limit as will as processing properties
need to be optimised. An understanding of polymer crystallinity
is important because the mechanical properties of crystalline poly-
mers are different from those of amorphous polymers. Polymer
crystals are much stiffer and stronger than amorphous regions of
polymer. Therefore, the mechanical response of semicrystalline
polymers is generally greater than of amorphous polymers [35].
This is mainly due to the coexistence of amorphous and crystalline
phase, if two different semicrystalline polymers are mixed, more
complicated mechanical response are expected. The aim of this
study was to lead us to better understand this class of materials.
It is understood that the manufacturing of i-PP is rather difficult
due to its inherent crystallinity which requires high relatively pro-
cessing temperatures. However, blending i-PP may result in an
undesired deterioration of its mechanical behaviour. This repre-
sents a point of motivation for the present research work. Another
reason for the interest in studying PE/PP blends is due to the fact
that complete separation of post-consumer PE and PP is very diffi-
cult, it is necessary to have a good understanding of the behaviour
of PE/PP blends. The huge worldwide annual consumption require-
ments of PE and PP is also thought to be responsible for the contin-
uous research efforts directed towards the various blending issues
of these two thermoplastics. The interests and needs in this area of
polymer science and engineering have grown.
Miscible or compatible blends are called homogeneous blends.
They give rise to a single phase, in which individual components
are mutually soluble in one another. In most cases, compatibleblends have mechanical properties superior to those of incompat-
ible blends. Therefore, a lot of efforts have been made to develop
experimental techniques, such as electron microscopy, light scat-
tering, small-angle X-ray diffraction and dynamic mechanical anal-
ysis, to determine the compatibility of a pair of polymers. On the
other hand, immiscible or incompatible blends are called heteroge-
neous blends. The majority of these blends contain a matrix phase
of rigid resin and a dispersed phase of flexible resin. The character-
istics of the blend will be directly influenced by the chemical struc-
ture, molecular weight, molecular weight distribution of each
component and by the ratio of each component in the blend. They
have many interrelated variables that affect their rheological
behaviour, processability and the mechanical/physical properties
of the finished product. For instance, the method of blend prepara-tion, like the method of mixing and the intensity of mixing, con-
trols the morphology of the blend (e.g., the state of dispersion,
the size of the dispersed phase, and the dispersed phase size distri-
bution), which in turn controls the rheological properties of the
blend. On the other hand, the rheological properties strongly dic-
tate the choice of processing conditions, which in turn strongly
influence the morphology and therefore the mechanical/physical
properties of the finished product. The Miscibility of vLDPE and i-
PP has been addressed in a previous work, sent for publication.
These two polymers have been found to be partially miscible.
The effect of that on the mechanical behaviour is investigated in
the current work.
The conducted literature survey reveal that, in the recent years,
blending of PE and PP polymers is receiving and attracting increas-ing attention from researchers for various reasons including the
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possibility of creating a material or product for new and more
industrial applications to meet specific processing and perfor-
mance requirements that cannot be satisfied by a single compo-
nent. Considering all the above, many attempts have been made
to improve the mechanical properties of polymers by blending.
However, there is a need for further studies that might widen
the scope of knowledge on the influence of blending parameters
on the mechanical behaviour of polymer blends. Furthermore,
most of the studies addressed the issue of thermally unaged/un-
treated polymers, however, the work related to thermally aged
blends is very lacking. This study is thus carried out to investigate
the effect blending ratio PE/PP and thermal aging on the mechan-
ical properties of PE/PP blends. Tensile and hardness tests were
conducted on injection molded and thermally aged PE/PP blend
samples to study the influence on the mechanical properties (elas-
tic moduli, strengths, percent elongations, and hardness values)
and to determine their macroscopic response. All these efforts have
offered additional information to the pool of existing knowledge
and experience accumulated by other workers in similar fields.
Thermogravimetric analysis (TGA) is a helpful technique for
studying the thermal decomposition of polymers and its applica-
tion can be expanded to the determination of the kinetic features
of degradation. Detailed survey on the TGA for PE, PP in both nitro-
gen and air atmospheres are presented by Mourad et al. [36].
In this study, blends of very low density polyethylene (vLDPE)
and isotactic polypropylene (i-PP) were used to prepare vLDPE/i-
PP samples of 100/0, 75/25, 50/50, 25/75, 0/100 weight ratios.
The samples were thermally aged by oven method for periods of
0.0, 2, 4, 7, and 14 days. The main objective of this work is to study
the thermo-mechanical performance of thermally aged vLDPE/i-PP
blends.
2. Materials and experimental procedure
2.1. Materials
The polymers used in this study are commercially available and
provided in the form of pellets with the courtesy of DSM, Inc., The
Netherlands. It has been confirmed that they are very low-density
polyethylene (vLDPE) and isotactic polypropylene (i-PP). The com-
pany did not provide further details such as molecular weight dis-
tribution, melt flow index (MFI) and density. for the purpose of
confidentiality. The basic physical properties of the polymers se-
lected for the study are: density (g/cm3) values are 0.893 and
0.930 and melt flow index (MFI) (g/10 min) values are 9.505 and
4.425 for vLDPE and i-PP, respectively.
2.2. Preparation of molded strips
Injection moulding technique was used for fabricating themolded strips which will be subjected to aging process. Vertical
injection moulding apparatus (Test Sample Moulding Press-hand
operated model-supplied by Norwood Instruments Ltd.) with a cyl-
inder of 20 mm bore and 180 mm length was used. The correct
amount of pelletized material was fed into the cylinder/barrel of
apparatus. This charge was pushed forward into the cylinder by
the motion of a plunger or ram, at which point the charged mate-
rial melts to form a viscous liquid (plasticize). Next, the molten
plastic was impelled, again by ram motion, through a nozzle into
the enclosed molt cavity; pressure was maintained until the
molded strip has solidified under a forced air cooling using electric
fan. The mould assembly (tool) was opened, the strip was ejected.
Finally, the mould was assembled for the next strip injection. Four
strips can be produced from each batch/blend ratio. The entirecycle was repeated for the subsequent mixture. The operation
variables or parameters that to be precisely controlled included
mould and cylinder temperatures, injection pressure and the
mould temperature at strip ejection. This is to ensure that the pure
polymers and their blends all had similar thermal history, so as to
minimize any possible effects on the subsequent tests due to pro-
cessing discrepancy in the upstream preparation work. The mould
(with cavity dimensions of 80Â 25Â 1 mm) is fabricated and used
to produce rectangular strips with the cavity dimensions.Salient
points in preparing the molded strips are as follows.
The respective virgin pellets of PE and PP were first carefully
weighed separately and manually mixed at various fractions, to
produce mixtures of 20 grams each, Five different mixtures and
strips of PE/PP (wt.%) were obtained (100/0, 75/25, 50/50, 25/75,
0/100). The machine was provided with two-zone digital tempera-
ture controller for barrel and mould. The barrel and mould temper-
atures are controlled by digital controller and leave to stabilize
before dispatch. The barrel temperature is controlled at 180 °C
for pure PE and 190 °C for pure PP, while the mould temperature
is controlled at 115 °C. Sufficient time (approximately from 8 to
10 min) was allowed for the material to plasticize. The molten
material was carefully mixed mechanically using a specially de-
signed stirrer. The molten polymer, or melt was injected into the
closed mould cavity where it cooled and solidified. When the tool
temperature reaches %75 °C (within approximately 10 min), the
tool (mould assembly) is opened with care from its location so that
the product could be removed, Forced air cooling with electric fan
was used while cooling and solidification process of the molded
material. This process improved the ease with which the strip
can be removed from the mould cavity and the quality of the
molded strip as well. When moulding was complete, the cylinder
liner was removed and cleaned in a suitable solvent. Then the pro-
cess is repeated for the next batch (blend ratio).
2.3. Aging process
This was performed by the oven method as described by theASTM 0573-99. The molded stripes were placed in a preheated
oven at 100 °C (OSK 9500 M-Electric Oven-Type C-OGAWA-SEIKJ-
Co. Ltd.). The aging interval began at the time the specimens were
placed in the oven and continued for time intervals of 2, 4, 7 and
14 days at 100 °C. At the end of each aging interval, the strips were
removed from the oven, cooled to room temperature on a flat sur-
face and allowed to stand for not less than 24 h prior to further
processing. Then samples were characterized after the aging
process.
2.4. Tensile testing
A dumbbell test samples in accordance with ISO 527 (con-
formed also to IEC 923/01 and ASME D 638) were punched fromthe aged injection molded strips. Two or three (if possible) speci-
mens were punched side by side from each strip using a hydraulic
press. All specimens have a gauge length of 17 mm, width of 4 mm,
thickness of 1 mm and overall length of 50 mm.
The dumbbell shaped specimens were tested according to ISO
527. The tests were carried out on a 30 kN Zwick universal testing
machine (MTMT1-FR0303THA1k) under displacement controlled
conditions. They were stretched at a constant cross head speed of
25 mm minÀ1 until they fail. All tests were carried out at a room
temperature (23 ± 5 °C) and atmospheric pressure. The total length
between the grips is about 34 mm for the used dumbbells and the
rate of separation was 25 mm minÀ1. At least two valid results are
to be achieved in order to calculate the tensile properties; other-
wise the test is repeated and any unsatisfactory test result was ig-nored. The average value of the results is presented.
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The tests were conducted to determine the tensile properties
(e.g., modulus of elasticity E , yield strength ry and elongation at
break) of the material. The Young’s modulus E is determined as
the tangent modulus at 1% strain; which is almost the tangent
slope to the first portion of the curve and also as the secant mod-
ulus at 2% strain. In the absence of a distinct yield point, yield
strength is defined as the 0.5%-offset stress r0.5. Also it was deter-
mined at the initial peak load on the curves; if exists.
2.5. Hardness testing
Hardness was measured using shore durometer type D. In mea-
surements the recommendations of the standard SFS-ISO 868:E
was used for hardness test. All tests were conducted at room tem-
perature and atmospheric pressure. Test specimens of 1 mm thick-
ness were cut from the aged and unaged injection molded strips.
The surface of the specimen was examined carefully to make sure
that it was flat and clean. At least three test specimens were pre-
pared for each condition and at least five readings have been re-
corded for each specimen. The average value of the fifteen
readings, for each condition, is presented.
2.6. Thermogravimetric analysis (TGA)
The thermal decomposition/degradation was studied by ther-
mogravimetry in a PERKIN ELMER thermogravimetric instrument
(TGA 7). Samples of a mass ranged between 10 and 20 mg were
cut from both aged and unaged strips. The samples were heated
from room temperature up to 600 °C (873 K) in a dynamic air
atmosphere with a flow rate of 60 ml minÀ1 and a heating rate of
10 °C/min in the thermal analyser. The degradation (% weight loss)
of the samples was monitored and measured as a function of tem-
perature and analyzed with the TGA analysis program. The first
derivative of the weight loss (i.e., derivative thermogravimetric
analysis DTA/derivative thermogravimetry DTG) of the weight loss
was recorded simultaneously. The TGA thermograms and their firstderivatives (DTA) were then plotted. Hence, the onset of degrada-
tion or initial decomposition temperature T d(1%) (the temperature
at which 1% of weight has been lost), the final decomposition tem-
perature T d(99%) (the temperature at which 99% of weight has been
lost), and the maximum decomposition rate temperature T max (the
temperature at which the rate of mass loss is at a maximum were
evaluated for each sample. Another initial/onset decomposition
temperature T d obtained directly from the thermogravimetric
instrument (TGA 7). T d is obtained at the intersection of the two
tangents of the 1st and 2nd portions of the thermogramme. The
method is demonstrated in the results section.
3. Results and discussion
3.1. Tensile and hardness testing
Stress–strain curves show the response of the tested materials
to applied stress. They reveal important information such as
Young’s modulus, yield strength and yield strain. Accurate knowl-
edge of these parameters is paramount in engineering design.
These curves allow us explore the different stages in the curves
as the strain is increased.
It was observed while conducting the tensile tests on the spec-
imens of PE, PP and their blends that all tested specimens exhibited
necking and cold drawing. The region of necking are evident for all
pure PE, PP and their blends tested specimens. It was noted also
that all specimens remained transparent as they were stretched.
Stress–strain data from a tension test on PE, PP and their blendssamples and for different aging durations (2, 4, 7 and 14 days) are
plotted in Figs. 1–5. The figures show all data to fracture and the
initial part of the data were also plotted (not presented here) at a
sensitive strain scale (up to 50% strain) to facilitate the measure-
ments of the modulus of elasticity. The values of modulus of elas-
ticity E (based on tangent and secant methods), yield strength ry
(based on 1st zero gradient and offset methods), percent yield
strain ey, tensile strength at break r f and percent strain at break
e
f for the tested samples have been obtained (and collected in a
0
2
4
6
8
10
12
14
16
18
0 100 200 300 400 500 600 700 800 900 1000 1100 1200
Strain (%)
S t r e s s ( M P a
)
0:10025:7550:5075:25100:0
Fig. 1. Stress–strain curves for untreated PE/PP blends.
0
2
4
6
8
10
12
14
0 100 200 300 400 500 600 700 800 900 1000 1100 1200
Strain (%)
S t r e s s
( M p a )
0:10025:7550:5075:25100:0
Fig. 2. Stress–strain curves for PE/PP blends of 2 days thermal treatment.
0
2
4
6
8
10
12
14
16
18
0 100 200 300 400 500 600 700 800 900 1000 1100 1200
Strain (%)
S t r e s s ( M p a )
0:10025:7550:5075:25100:0
Fig. 3. Stress–strain curves for PE/PP blends of 4 days thermal treatment.
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table, which is not presented here) from the curves for the purpose
of analysis.
Figs. 6–10 show the stress strain curves for all PE/PP (wt.%) per-
centages (100/0.0, 75/25, 50/50, 25/75, 0.0/100) and for the differ-
ent aging durations. Figs. 7 and 10 show two distinctive tensile
behaviours for pure PP and PE. For pure PP (Fig. 10), after signifi-
cant yielding in the 1st part of the stress–strain curve, the stress
drops to the drawing stress (in the 2nd part) and remains constant
in the 3rd region up to a certain value of engineering strain when
work hardening commences again. In the last, 4th part, almost lin-
ear hardening is evident. It is seen in the graphs that the 1st partrepresents almost linear behaviour. At the end of this part, the
stress has reached an instability limit. After reaching this maxi-
mum load (1st peak load), a reduction in area appears somewhere
along the gage section. Rather than being stationary, as in the case
of metals, the neck travels along the gage length to produce a ‘‘sec-
ond specimen” of reduced cross section and increased gage length.
A further increase in the displacement tends to untangle the long
molecules that cause the stress to decrease (2nd part) to the level
of the drawing stress. In the 3rd region, the deformation is such
that it can develop through the untangling of the molecules with-
out incurring any further increase in the stress. The molecules be-
come untangled and to accommodate further elongation the
molecules have to be stretched which causes an almost linear in-
crease in stress level (4th part). This trend of tensile behaviour isobserved regardless the period of thermal aging.
Not all polymers undergo the elongation and the necking pro-
cess described above for pure PP. For pure PE the necking process
is closer to that found in metals than that of polymers. The
stress–strain diagrams for pure PE (Fig. 6) show that the stress
never decreases and the specimen fracture at a particular strain.Here the neck forms before the maximum load is reached at a
0
2
4
6
8
10
12
14
16
18
0 100 200 300 400 500 600 700 800 900 1000 1100 1200
Strain (%)
S t r e
s s ( M p a )
0:100
25:75
50:50
75:25
Fig. 4. Stress–strain curves for PE/PP blends of 7 days thermal treatment.
0
2
4
6
8
10
12
14
16
18
0 100 200 300 400 500 600 700 800 900 1000 1100 1200
Strain (%)
S t r e s s ( M p a )
0:100
25:7550:5075:25100:0
Fig. 5. Stress–strain curves for PE/PP blends of 14 days thermal treatment.
0
2
4
6
8
10
12
14
16
18
0 100 200 300 400 500 600 700 800 900 1000 1100 1200
Strain (%)
S t r e s s ( M p a )
14 days
4 days
2 days
0 day
Fig. 6. Stress–strain curves for untreated and thermally treated pure PE samples.
0
2
4
6
8
10
12
14
16
18
0 100 200 300 400 500 600 700 800 900 1000 1100 1200
Strain (%)
S t r e s s ( M p a )
14 days
7 days
4 days2 days0 day
Fig. 7. Stress–strain curves for untreated and thermally treated 75% PE/25% PPblend samples.
0
2
4
6
8
10
12
14
16
18
0 100 200 300 400 500 600 700 800 900 1000
Strain (%)
S t r e s s ( M p a )
14 days
7 days4 days
2 days0 day
Fig. 8. Stress–strain curves for untreated and thermally treated 50% PE/50% PP
blend samples.
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certain axial position. As in the case of pure PP, pure PE samples ex-
hibit the same tensile behaviour trend regardless the period of
thermal aging.
The tensile test curves for pure PP (Fig. 10) show a clear yield
point where the slope of stress–strain curves reached zero. In con-trast, a clearly observable yield point was not able to be obtained
for pure PE stress–strain curves (Fig. 6), as no maximum/peak point
was observed. The clearly observed yield point for pure PP disap-
pears gradually as polyethylene weight percent increases (Figs.
1–5). This observation might reveal that the two polymers are par-
tially miscible. Therefore, and for the purpose of unification, the
yield strength for all PE, PP and their blends are defined as the
0.5% offset stress, which is the stress determined by the intersec-
tion of the stress–strain curve and an imaginary line parallel to
the onset gradient of the stress–strain curve shifted to the 0.5%
strain value. Tensile yield strength is also determined from themaximum point/peak point (if present) where the slope of
stress–strain curve reached zero.
When comparing yield strengths which are determined for dif-
ferent blend ratios, interesting trends are observed. It is found from
Fig. 11 (which shows the variation of ry with PE content) that ten-
sile yield strength decreases with increasing PE ratio. This is as a
consequence of the lower yield strength of pure PE (r0.5% = 1
MPa) than pure PP (r0.5% = 5.2 and rpeak = 10 MPa) and the partial
miscibility of the two polymers. Although, the peak stress of pure
PP samples increase by as much as 2.3 MPa (23%), the results indi-
cate that the thermal aging has not affected significantly the yield
strength of blends. Moreover, there is no clear trend of variations of
the yield strength with the thermal aging period.
The tensile modulus (based on both tangent and secantmethods) is plotted as a function of PE content for various thermal
0
2
4
6
8
10
12
14
16
18
0 100 200 300 400 500 600 700 800
Strain (%)
S t r e s s ( M p a )
14 days
7 days4 days
2 days
0 day
Fig. 10. Stress–strain curves for untreated and thermally treated pure PP samples.
0
1
2
3
4
5
6
7
8
0 25 50 75 100
PE weight (%).
Y i e l d s t r e n g t h ( M P a ) .
14 days
7 days
4 days
2 days
o day
Fig. 11. Variation of offset yield strength r0.5 with PE content for untreated and
thermally treated blends.
0
100
200
300
400
500
600
0 25 50 75 100
PE weight (%).
M o d u l u s o f
e l a s t i c i t y ( M P a ) .
14 days
7 days
4 days
2 days
o day
Fig. 12. Variation of modulus of elasticity (tangent) with PE content for untreated
and thermally treated blends.
0
2
4
6
8
10
12
14
16
18
0 100 200 300 400 500 600 700 800
Strain (%)
S t r e s s ( M p a )
14 days
7 days
4 days
2 days
0 day
Fig. 9. Stress–strain curves for untreated and thermally treated 25% PE/75% PP
blend samples.
0
100
200
300
400
500
600
0 25 50 75 100
PE weight (%).
M o d u l u s o f e l a s t i c i t y ( M P a ) .
14 days
7 days
4 days
2 days
o day
Fig. 13. Variation of modulus of elasticity (secant) with PE content for untreated
and thermally treated blends.
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treatment periods in Figs. 12 and 13. the values for pure PP
(255 MPa using 1% strain tangent and 225 using 2% strain secant)
are much higher than that for PE (50 MPa and 42 MPa using the
same two techniques), i.e., five times. The tensile modulus, as yield
strength, decreases with an increase in PE content. However, the
periods of thermal aging have no significant effect on the modulus
(Figs. 14 and 15) as in the case of yield strength.
The yield strain of untreated and thermally treated pure poly-
mers and their blends was found to vary in the range 2%:3.5% with
no specific trend of variation with PE content. It was also observedthat PE, PP and their blends deform in ductile modes similar to rub-
ber. They undergo a uniform yielding over a wide range. This yield-
ing is followed by strain hardening and failure. The test data show
that the strain to brake of pure PE is much higher than pure PP and
intermediate values for their blends have been observed. Never-
theless, some specimens have been observed to fail prematurely.
We infer that the origin of the decrease in modulus and yield
strength lies in the blend structure. In contrast to our observation
for PP, Lee et al. [37] reported that PP polymer prepared by metal-
locene catalyst undergoes brittle failure. This behaviour is ob-
served during the stretching of PP films of 0.1 mm thickness
prepared by hot pressing for 5 min at 190 °C under one metric
ton. The polyolefin films were characterized after 3 days of physi-
cal aging of room temperature. These films develops localisedstress whitening (necking) in a small region (usually) less than
2 mm, followed by the abrupt failure of the region in the brittle
failure of PP, crazing (or at least craze-like deformation) is thought
to play a major role. There observations agree with our observation
for PE. They reported that films of polyethylene copolymers pre-
pared by metallocene deform in ductile modes similar to rubber.
Some others investigators reported also that the strain-to-break
of the PE films [38–40] is much higher than PP films.
In the present work, a Shore Durometer type D hardness tester
was used. The average value of the fifteen readings, for each condi-
tion, has been presented in Figs. 16 and 17 show the effects of the
blending ratio and aging time on the hardness of different samples.
Fig. 16 shows that the measured hardness values for pure PP at dif-
ferent aging times are larger than that of PE and their blends have
intermediate values. Generally, aging time has not affected thehardness as shown in Fig. 17. These observations are correlated
to the observation of the tensile tests.
The tensile and hardness tests results indicate the presence of
some partial miscibility in the PP and PE blends. This has been ob-
served by Mourad et al. [36] through differential scanning calorim-
etry (DSC) and thermogravimetric analysis (TGA), in a dynamic
nitrogen atmosphere. The results show that, addition of PE had
caused the crystalline melting temperature heat of fusion and per-
centage crystallinity of PP main crystalline peak to decrease. Sim-
ilar observations have been also reported in [41,42].
3.2. Thermogravimetric analysis (TGA)
The thermogravimetric analysis (TGA) in a dynamic air atmo-sphere and derivative thermogravimetric analysis (DTA) were
0
100
200
300
400
500
600
0 2 4 6 8 10 12 14
Aging time.
M o d u l u s o f e l a s t i c i t y ( M P a ) .
100:0 75:25 50:50 25:75 0:100
Fig. 15. Independence of modulus of elasticity (secant) from the aging time for
different PE/PP blend samples.
50
55
60
65
70
75
80
100/0 75/25 50/50 25/75 0/100
Blending ratio
H
a r d n e s s
0 days
2 days4 days
7 days
14 days
Fig. 16. Variation of hardness with blending ratio.
0
100
200
300
400
500
600
0 2 4 6 8 10 12 14
Aging time.
M o d u l u s o f e
l a s t i c i t y ( M P a ) .
100:0 75:25 50:50 25:75 0:100
Fig. 14. Independence of modulus of elasticity (tangent) from the aging time for
different PE/PP blend samples.
40
45
50
55
60
65
70
75
80
0 2 4 7 14
Aging time, days
H a r d n e s s
100/0
75/25
50/50
25/75
0/100
Fig. 17. Hardness variation with aging time.
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performed on all thermally unaged and aged neat polymers and
their blends in order to investigate the effect of blending ratio
and the aging time on the thermal decomposition. The thermo-
gravimetric curves are grouped into five collective figures each of
which for a particular aging time. The same was done for the deriv-
ative thermogravimetry (DTG) curves. All measurements were
made in duplicate with good repeatability. The TGA in a dynamic
nitrogen atmosphere has been investigated by Mourad et al. [36].
3.3. Decomposition temperatures T d(1%), T d, T max and T d(99%)
A typical thermogravimetric analysis (TGA) and the derivative
thermogravimetry (DTG) curves, obtained from the apparatus,
showing the different decomposition temperatures are shown in
Fig. 18. The figure shows also how the onset/initial degradation
temperature based on the machine definition T d (°C) (at the inter-
section of the two tangents of 1st and 2nd TGA curve), the maxi-
mum rate of decomposition temperature T max (°C) (at the DTG
curve peak), the final decomposition temperature T d(99%) (°C) (atwhich 99% of weight has been lost). Another initial decomposition
temperature at which 1% of the sample weight has been lost also
calculated from the raw data of the TGA thermogramme. T d(99%)
identifies the temperature at which the polymer starts to degrade
at an early stage and eliminates the discrepancy that might occur
due to the construction of the two tangents while calculating T d.
Three representative TGA thermogram groups, for thermallyunaged and aged (for 2 and 14 days) blends are shown in Figs.
19–21. It is seen that all TGA curves are single-stage mass decrease
(loss) curves (e.g., single-stage decomposition). The T d(1%), Td, Tmax
and T d(99%) decomposition temperatures for all blends are summa-
rized in Table 1. It is seen that all samples started to decompose at
no less than 365 °C. Although the thermal stability in the industrial
applications depends on operating temperature and exposure time,
this relatively high temperature might indicate the thermal stabil-
ity in a wide operating temperature range. A higher corresponding
decomposition temperature (i.e., 380 °C), in a dynamic nitrogen
atmosphere, for the same blends has been reported by Mourad
et al. [36] which shows less thermal stability in the real service
conditions. Table 1 shows also that the T d, T d(1%) and T max decompo-
sition temperatures of neat unaged PP are relatively higher thanthat for neat unaged PE. However, the T (d99%) is found to be
Fig. 18. A typical apparatus TGA thermogramme (in a dynamic air atmosphere) and its first derivative (DTG) for thermally aged (for 14 days) pure PP showing onset of
decomposition T d (390.33 °C) and max decomposition rate (415.91 °C) temperatures.
0
20
40
60
80
100
120
0 100 200 300 400 500 600 700
0.0/100
25/75
50/50
75/25
100/0.0
W e i g h t ( % )
Temperature (oC)
Fig. 19. TGA thermograms (in a dynamic air atmosphere) of degradation (weight
loss) as a function of temperature for thermally unaged blends (0.0 days).
0
20
40
60
80
100
120
0 100 200 300 400 500 600 700
0.0/100
25/75
50/50
75/25
100/0.0
W e i g h t ( % )
Temperature (oC)
Fig. 20. TGA thermograms (in a dynamic air atmosphere) of degradation (weight
loss) as a function of temperature for thermally aged (for 2 days).
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relatively higher for neat PP than PE. These observations of the
decomposition temperatures reveal that the PP has a relatively
higher thermal stability than PE. Fig. 22 shows the variation of
the in air atmosphere initial decomposition temperature T d(1%)
with PE content within thermally unaged and aged blends. The
thermally unaged and aged pure PE samples have relatively higher
T d(1%) than pure PP samples and the blends of PE%/PP% (75%/25%,
50%/%/50% and 25%/75%) have intermediate values. It is worth not-
ing also that, the 50%/50% blend has relatively lower values than
other two blends. This behaviour is consistent for all thermally un-
treated and treated samples as shown in Fig. 22. As the content of
either PE or PP increases (i.e., 75%/25% and 25%/75%), decomposi-tion is slightly retarded and hence the T d(1%) increases if compared
with pure PE samples. This may be explained on the basis that the
two polymers are partially miscible and is also consistent with the
fact that PE and PP decompose to structure like products and the
lower values of 50%/50% blend may be a consequence of the co-
continuous phase effect. Fig. 23 shows the independence of T d(1%)
from the aging time within thermally unaged and aged blends
(i.e., the aging time has not influenced the T d(1%) of various ther-
mally unaged and aged polymers. Table 1 shows also that the pre-
vious observations for T d hold true for T d(1%).
Fig. 24 demonstrates that the unaged and aged pure PE samples
have relatively higher maximum decomposition rate temperature
T max than pure PP samples as for T d(1%). Also, the trend of variation
of T max with PE content is almost similar to that for T d(1%). Further-more, the results demonstrated that, T max is independent of aging
0
20
40
60
80
100
120
0 100 200 300 400 500 600 700
0.0/100
25/75
50/50
75/25
100/0.0
W
e i g h t ( % )
Temperature (oC)
Fig. 21. TGA thermograms (in a dynamic air atmosphere) of degradation (weight
loss) as a function of temperature for thermally aged (for 14 days).
Table 1
The decomposition temperatures in air atmosphere for unaged and aged blends.
PE/PP (wt.%) aging times (day) T d (°
C) T d(1%) (°
C) T max (°
C) T d(99%) (°
C)0.0/100 0.00 381 308 427 573
2.00 381 306 417 574
4.00 385 304 412 582
7.00 376 303 404 576
14.00 390 302 400 578
25/75 0.00 379 306 425 573
2.00 375 305 415 574
4.00 380 302 412 580
7.00 370 302 402 582
14.00 382 300 399 580
50/50 0.00 376 297 394 570
2.00 365 296 392 567
4.00 375 295 390 581
7.00 377 295 385 583
14.00 369 293 380 585
75/25 0.00 372 297 420 567
2.00 369 294 417 5734.00 368 295 412 580
7.00 371 295 407 575
14.00 375 293 395 583
100/0.0 0.00 372 290 398 568
2.00 368 289 397 577
4.00 370 289 392 575
7.00 367 291 391 578
14.00 367 288 391 580
T d = the onset of degradation temperature based on the machine definition (°C);
T d(1%) = the initial/onset decomposition temperature at 1% sample weight loss (°C);
T max = the maximum rate of decomposition temperature (°C); T d(99%) = the tem-
perature at which 99% of weight has been lost.
260
270
280
290
300
310
320
330
340
0 25 50 75 100
0 day
2 days
4 days
7 days
14 days
T d ( 1 % ) ( o C )
PE content (wt %)
Fig. 22. Variation of the in air atmosphere initial decomposition temperature T d(1%)
with PE content within thermally unaged and aged blends.
260
270
280
290
300
310
320
330
340
0 2 4 6 8 10 12 14
0 %
25 %
50 %
75 %
100 %
T d ( 1 % ) ( o C )
Aging time (day)
Fig. 23. Independence of the in air atmosphere initial decomposition temperature
T d(1%) from the aging time within thermally unaged and aged blends.
300
320
340
360
380
400
420
440
460
480
500
0 25 50 75 100
0 Day
2 Days
4 Days
7 Days
14 Days
T m a x
( o C )
PE content (w%)
Fig. 24. Influence of the in air atmosphere maximum decomposition rate temper-
ature T max from theblendPE content withinthe various thermally unaged andaged
blends.
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time which is analogous to that for T d(1%). Similar results have been
reported by Mourad et al. [36] for the same blends in dynamic
nitrogen atmosphere.
The values of the T d(1%) and T d are very critical in the design and
processing of polymeric components, since they could indicate
which would be the processing and manufacturing temperatures
without continuing or initiating a process of decomposition, espe-
cially in blends of recycled material. The results obtained regarding
the initial temperature of the decomposition process show that the
introduction of VLDPE results in the degradation beginning at
slightly lower temperatures.
Table 1 illustrates also that, the T d(99%) for unaged pure PP(573.4 °C) is little higher than that for unaged pure PE (567.7).
The values for unaged and aged samples vary within difference
range of 17 °C (3% of the maximum value). This reflects again al-
most an independent variation of T d(99%) from PE content and aging
time.
The decomposition temperature range (DT = T d(99%) À T d(1%)) is
calculated and presented in Table 2, from which it is clear that
the degradation temperature range varies from DT = 267 up to
DT = 293 °C. The pure and unaged PP sample has the lowest degra-
dation temperature range (265 °C) among all samples. This is also
consistent for all aging times, because of the higher T d(1%) it has and
almost same T d(99%) value as other blends. The 50% PE/50% PP blend
of 14 days aging time has the maximum degradation temperature
range, this is due to its lower value of T d(1%) (early start of decom-position) and almost same T d(99%) as other blends. This is also pos-
sibly due to a cooperative effect resulting from less dominance in
either of the blend components. Similar observation has been re-
ported for dynamic nitrogen atmosphere [36].
For all examined blends, residues were not obtained, based on a
sample weight of 9 mg:10 mg, as seen in the TGA thermograms of
Figs. 18–21. This illustrates that nearly all the sample weight sub-
jected to degradation was transformed into volatile material and
the decomposition led to a complete vaporization of the sample.
This could be because the investigated material is of organic
nature.
4. Conclusions
The main goal of this work was to investigate the effect of ther-
mal aging and blend composition on the thermo-mechanical
behaviour of unblended vLDPE and i-PP and their blends. Based
on the results of this study the following main conclusions could
be drawn:
All tested specimens exhibited necking and cold drawing. Strain
to break/percentage elongation (e%) for pure vLDPE samples was
much higher than that for pure i-PP samples and their blends
had an intermediate performance.
Two distinctive tensile behaviour trends were observed for
vLDPE and i-PP samples and an intermediate behaviour trend
was observed for their blends.
Addition of vLDPE to i-PP caused the modulus of elasticity andyield strength of i-PP to decrease.
The addition of vLDPE to the i-PP by the weight ratio of 25:75
reduced the percentage crystallinity by ca. 20% [36] while
retaining almost the same values for the modulus of elasticity
and yield strength. Further addition of PE content dramatically
diminished the mechanical performance of the i-PP. It is highly
recommended that no further addition of PE should take place
beyond the 25% mark, while it is equally important to further
study the structure–property relationship for blends of less PE
content in later studies.
The tested thermal aging periods had no influence on tensile and
hardness behaviour of pure and blend samples.
The decomposition temperatures from the TGA in a dynamic air
atmosphere illustrate that all samples started to decompose at
no less than 365 °C.
The tested thermal aging periods had no influence on the ther-
mal behaviour of pure and blended polymers, However, the PE
content has found to have some influence on the thermal stabil-
ity/decomposition temperatures.
The decomposition temperatures variations with blend ratio and
aging time in both dynamic nitrogen [36] and air atmospheres
are analogous,
The thermo-mechanical properties reveal that the i-PP and
vLDPE are partially miscible/compatible and the resulting
blends were not fully homogeneous. These results are supported
by the observation of other investigators [41,42].
Acknowledgements
The author appreciate the help of Eng. Jayarajan Kadachi and
Mr. Francis Corriea of DUCAB company, Jabel Ali, Dubai, in con-
ducting the tensile tests and also the assistance of Eng. R. Akkad
in plotting the tensile curves.
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Table 2
The decomposition temperature range (DT ) for thermally unaged and aged samples.
PE/PP ratios DT = (T d(99%) À T d(1%)) (°C)
(0 day) (2 days) (4 days) (7 days) (14 days)
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25/75 267 269 278 280 280
50:50 273 272 286 289 293
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100/0.0 279 288 286 286 292
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