Strain Induced Anisotropic Properties of Shape Memory Polymer
Transcript of Strain Induced Anisotropic Properties of Shape Memory Polymer
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IOP PUBLISHING SMART MATERIALS AND STRUCTURES
Smart Mater. Struct. 17 (2008) 055021 (7pp) doi:10.1088/0964-1726/17/5/055021
Strain induced anisotropic properties ofshape memory polymer
Richard Beblo and Lisa Mauck Weiland1
Department of Mechanical Engineering and Material Science, University of Pittsburgh,
660 Benedum Hall, Pittsburgh, PA 15261, USA
E-mail: [email protected] and [email protected]
Received 17 March 2008, in final form 30 June 2008
Published 10 September 2008
Online at stacks.iop.org/SMS/17/055021
AbstractHeat activated shape memory polymers (SMPs) are increasingly being utilized in ambitious,
large deformation designs. These designs may display unexpected or even undesirable
performance if the evolution of the SMPs mechanical properties as a function of deformation is
neglected. Yet, despite the broadening use of SMPs in complex load bearing structures, there
has been little research completed to characterize how the material properties change upon
application of large strain. The following is an experimental investigation into the strain
induced anisotropic properties of the SMP Veriflex. It is found that under large uniaxial strain
the SMPs stiffness in the transverse direction can be reduced as much as 86%, while the
toughness in the axial direction may increase by an order of magnitude in some cases.
A generalized analysis suggests that this trend should be expected for any SMP.
1. Introduction
Since their development in the late 1960s and early 1970s,
engineered polymers such as shape memory polymers (SMPs)
have been widely researched for their capability to recover
from large amounts of strain as well as their ability to switch
between relatively low and high moduli [13]. Their unique
characteristics have made them attractive for several design
concepts which rely on the polymers ability to soften, be
deformed by relatively low force, and then harden as a
new shape capable of carrying loads, possibly over several
cycles. Such characteristics are possible through the use of an
elastic segment and a transitioning segment. Above the glasstransition temperature Tg, the elastic segment dominates the
material response, while below Tg, the transitioning segment
crystallizes, dominating the material response.
In the biomedical field, SMPs have been proposed
as stents for the treatment of cardiovascular disease and
aneurysms [4, 5]. Biodegradable formulations have also
been developed for use as internal sutures, aiding in
minimally invasive surgeries [6]. The automotive industry
is implementing designs using SMPs in active air dams and
aerodynamic control actuators for improved fuel economy
and performance [7]. Further, SMPs are being considered
in the aeronautical and astronautical fields in morphing1 Author to whom any correspondence should be addressed.
aircraft wing structures as a skin allowing large in-plane
deformations of the wing. The design goals of the latter
are to create a class of military aircraft capable of multi-
mission roles [8, 9]. In efforts to augment such designs, novel
heating and cooling schemes have been developed, including
magnetic nanoparticles [10, 11], both reducing the need for
large and complex heating and cooling systems and improving
the response time of the polymer.
Heat activated SMPs are divided into categories based
on their chemical makeup, the most common of which are
polystyrene, polyurethane, and epoxy based polymers [12].
The constitutive response of SMPs is best described by
considering four discrete temperature regions as illustrated by
figure 1. In the lowest temperature regime, or the glassy state,
the small strain approximation is reasonable; hence a constant
elastic modulus is typically assumed, such as in the generalized
form of Hookes law,
i =1
E
i
j + k
, i j =
i j
G, (1)
where is the strain, E is the Youngs modulus, is the
stress, is Poissons ratio, G is the shear modulus, is the
shear stress, is the shear strain, and i , j , and k are any even
perturbation of an orthonormal basis. In the two transition
regions, time dependent temperature equations are deriveddescribing the assumed isotropic moduli of the polymer. For
0964-1726/08/055021+07$30.00 2008 IOP Publishing Ltd Printed in the UK1
http://dx.doi.org/10.1088/0964-1726/17/5/055021mailto:[email protected]:[email protected]://stacks.iop.org/SMS/17/055021http://stacks.iop.org/SMS/17/055021mailto:[email protected]:[email protected]://dx.doi.org/10.1088/0964-1726/17/5/055021 -
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Figure 1. Heat activated shape memory polymer cycle.
instance, from conservation of energy theory, the internal
energy can be expressed as [13]
u
t =
mnD
mn +r
q
m,m, (2)
which can then be related to the Youngs modulus, where
is the density, u is the internal energy, t is time, D is a
deformation rate tensor, r represents internal heat generation
per unit mass, q represents the heat flux across the boundary,
and m and n are indicial indices. The first term on the right-
hand side of the equation is referred to as the stress power, and
it accounts for the mechanical work done to the polymer. In the
highest operating temperature regime, or the elastic region, the
material response is viscoelastic, for which there are several
accepted models including Maxwells model,
Totalt
= Dt
+ St
= + 1
Eddt
, (3)
where is the viscosity, and the subscripts D and S
indicate damper and spring related quantities, respectively.
Moreover, several mathematical models of varying complexity
and accuracy have been proposed. There are two basic
methodologies utilized in the development of constitutive
models describing SMPs. The first employs the use of
piecewise functions, breaking up the response of the polymer
into the four distinct regimes illustrated by figure 1 and
outlined in equations (1)(3). Such methods have been used
by Barot et al, and have proven accurate under most loading
conditions with the exception of being ill-suited to modelplastic strain below Tg [14]. Bhattacharyya et al have also
proposed a model paralleling this methodology [15]. The
second approach used to model SMPs makes assumptions such
as the polymer being isotropic under all conditions in order to
derive a single constitutive equation, for example the model
proposed by Tobushi et al [16]:
=
E+ m
y
k
m1
k+
+ 1
b
c 1
n
s
+ , T (4)where the dot denotes a time derivative, m, b, and kare material
parameters, the subscripts y and c represent yield and creeplimits respectively, s denotes unrecoverable quantities, T is
temperature, and , and are the viscosity, retardation time,
and the coefficient of thermal expansion respectively. Strictly
speaking, the assumption of isotropy is not true; however,
the resulting single thermoviscoplastic constitutive equation
is useful for many applications where 3D modeling is not
required. Such models as those developed by Tobushi et al
[15, 16] are useful for unidirectional loading environments andmultiple-cycle modeling. Diani et al have also proposed a
single equation constitutive model capable of 3D predictions;
however, the model assumes the polymer to be isotropic below
Tg and that all strain is elastic, and is thus incapable of
modeling plastic deformation in the glassy state [17]. Other
models proposing single equation constitutive relations include
those by Liu et al [18] and Lin et al [19].
Extensive experimental studies have also been performed
characterizing the thermomechanical properties of SMPs,
including changes in stiffness with respect to temperature and
strain recovery capabilities [2022]. Gall et al have reported
the storage and release of internal stress through a typical
shape memory cycle of a composite of epoxy based SMP and
dispersed SiC particles [23]. An SMPs ability to recover from
nearly any amount of applied strain has been quantified as well
as its creep characteristics under continuous loading [24, 25].
Tobushi et al have conducted experiments indicating that
the shape recovery characteristics of a polyurethane SMP
foam are time and temperature dependent [25]. Yang et al,
studying an ether based polyurethane SMP, have reported the
effect of prolonged moisture exposure on the glass transition
temperature [26, 27]. Applications and material characteristics
of thin film SMP have also been reported [28, 29]. Poilane
et al, for example, have confirmed macroscale test results of
thin films of SMP using nanoindentation, bulge, and membranepoint deflection test techniques [28], while Tobushi et al
have proposed using such thin film SMPs as passive choke
devices for engines and customizable utensils for disabled
patients [29].
While each of the above models and experimental studies
is well suited for its intended purpose, none appropriately
addresses the anisotropies that occur at high strains in
SMPs. Moreover, the anisotropies that arise in polymers
in general when subjected to large strain have been well
documented. For instance, refer to the classic works of
Treloar et al [30] and Flory et al [31] involving rubber
elasticity. More recent experimental studies continue tosupport this expectation. For instance, Arruda et al [32] have
conducted experiments similar to those presented below on
polycarbonate and polymethylmethacrylate specimens. Strain
induced orientated crystallization has also been studied and
modeled, and has been found to cause similar anisotropies in
polyethylene terephthalate (PET) by Rao et al [33]. Below
Tg, strain hardening in polycarbonate has been observed by
Govaert et al, revealing a sinusoidal-like relationship between
the yield stress and the angle between the investigated direction
and the direction of alignment [34]. HAPEX, a substitute
for bone having an isotropic tensile strength of 18 MPa,
after being oriented through an extrusion process, has been
found to become anisotropic, with tensile strengths of 80 and9 MPa in the direction of and perpendicular to the direction
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of extrusion, respectively, by Bonner et al [35]. Experiments
proving strain induced alignment of microdomain structures
in polystyrene-block-polybutadiene-block-polystyrene (SBS)
triblock copolymers have been conducted with the use of x-
ray scattering techniques and transmission electron microscopy
by Aida et al [36]. While the phenomenon of polymer chain
alignment due to strain and its effect on mechanical propertieshas been well researched, differences between polymer
systems substantiate the need for the direct experimental
investigation of this effect in shape memory polymers. At
least as significant is the need to ensure that end users of
SMPs become alert to this generalized phenomenon, as this
discussion is relatively absent from current SMP literature.
The following work is an experimental investigation
into the effect large strains have on the styrene based SMP
Veriflex (a product of Cornerstone Research Group, LLC)
above and below the glass transition temperature Tg. The
experiments outlined in this work explicitly aim to quantify
these anisotropies to aid in the design of structures requiring
both morphing capabilities and multi-directional loading.
Following the experimental results, a generalized modeling
construct for anticipating the observed anisotropies is offered
to further reinforce the expectation that similar anisotropies
should be expected to evolve in other SMP (or any polymer)
formulations.
2. Experimental procedures
Veriflex is a cross-linked thermoset copolymer manufactured
in two parts: a resin and a hardener. Once mixed, the polymer
can be cast into any shape as well as machined after curing.
The manufacturer reports a glass transition temperature Tg of62 C.
2.1. Sample preparation
The resin and hardener are mixed per the manufacturers
specifications. A medium vacuum, approximately 27 Hg, ispulled on the sample until there are no remaining air bubbles
from mixing, while avoiding excess vacuum as this will remove
styrene from the mixture. The uncured polymer is then poured
into a steel mold conforming to the ASTM D638-03 type IV
specimen standard. The mold, treated with a manufacturer
supplied mold release, is then placed in a laboratory ovenat 75 C for 39 14
h. The extended 314
h as compared to
the manufacturers specifications compensates for the thermal
capacity of the mold.
In the creation of the samples for characterizing axial
response, the resulting 25 mm thick molded polymer is cut into
4 mm thick specimens for the standard isotropic tensile tests.
Each specimen is sanded with 200 then 600 grit sandpaper to
remove all tool marks and ensure a flaw free test sample.
In the creation of samples that are preconditioned with
axial strain, the 25 mm thick molded polymer is heated well
above Tg to 80C, strained, and cooled to below Tg prior
to slicing. Each specimen is then sliced and sanded per the
method above. Some of these samples are tested in thiscondition to characterize any changes in axial response as a
result of preconditioning; the remainder are further conditioned
for transverse characterization.
Samples for characterizing transverse response are sliced
from the preconditioned dog-bones such that only the
traditional gage length remains. This results in rectangular
specimens, as opposed to the preferred dog-bone style;
however, use of a video extensometer to monitor deformationonly in the central portion of the sample minimizes the edge-
effect error associated with this sample type.
2.2. Experimental setup
All tests are conducted with a screw driven MTI universal
load frame under displacement control. Characterization of
axial response is performed at a strain rate of 2 mm per
minute to avoid viscous effects, resulting in a maximum
starting strain rate of 4.5% per minute for unconditioned
samples. Characterization of transverse response is performed
at a rate of 0.25 mm per minute, resulting in a maximum
starting strain rate of 3.5% per minute for conditioned samples.Ambient tests are conducted at room temperature, 23 C, usinga 2 kN Transducer Techniques load cell. Tests above Tg(reported to be 62 C) are conducted at 80 C using a 1 kNTransducer Techniques load cell. A Bemco FTU3.0-100x600
UTM temperature/humidity chamber is used for environmental
control. A Messphysik ME46-450 video extensometer is used
to monitor axial and transverse deformation, with contrast
lines drawn directly on the samples. Specimen dimensions
are recorded with digital calipers, accurate to 0.01 mm.
Experimental results are reported as true stress/strain values.
3. Experimental results
Tables 13 and figure 2 summarize the experimental results
and include statistical errors as calculated using Students
t-distribution; per ASTM D638-03, at least five tests are
performed per reported measurement. Figure 2 is presented
using representative true strain values measured from the
original isotropic state before testing or any preconditioned
strain is applied. This method results in the curves for the 40%
and 70% preconditioned cases being offset (figure 2). This
reporting strategy allows a direct comparison of the total strain
applied to the sample beginning from the isotropic state. For
the characterization of transverse response in preconditionedsamples, this strategy results in an initial offset to a negative
strain due to the Poisson effect.
While offsetting for preconditioning in the figures enables
a convenient visual of the total linear deformation away from
the isotropic state, this strategy may obscure the meaning
of in-service performance. All tabulated results correspond
with zeroed initial conditions for all tested samples. Table 1
provides a summary of the measured material properties as
functions of preconditioning, temperature, and direction. Here,
the Youngs modulus of the specimens tested below Tg is
defined as the slope of the linear portion of the stress/strain
curve as seen in the top left and top right graphs in figure 2;
the slope is measured between the strains of 0.25% and 1.0%.The Youngs modulus above Tg is reported as the initial slope
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Figure 2. Representative stressstrain curves with offsets to illustrate preconditioning: axial testing below Tg (top left); transverse testingbelow Tg (top right); axial testing above Tg (bottom left); transverse testing above Tg (bottom right).
Table 1. Experimentally determined Youngs modulus, yield stress, and Poissons ratio.
Youngs modulus (MPa) Yield (MPa)Below Tg (23
C) Below Tg (23 C) Poisson ratioPreconditioned
strain (%) Axial Transverse Axial Transverse Axial
0 1140 71 13.0 1.2 0.4840 1300 50 190 15 15.6 1.1 11.3 2.0 0.4770 1270 120 160 51 14.6 1.2 9.5 0.4 0.38
Above Tg (80C) Above Tg (80 C)
Preconditionedstrain (%) Axial Transverse Axial Transverse Transverse
0 0.44 0.046 NA 0.4840 0.96 0.08 0.51 0.04 NA NA 0.4770 1.56 0.03 0.10 0.01 NA NA 0.38
of the stress/strain graph at the beginning of the test, as seen in
the bottom left and bottom right graphs in figure 2; the slope
is measured between the strains of 0% and 25%. Poissons
ratio is defined as the ratio of transverse strain to axial strain
in the same stress/strain region as that used to calculate the
Youngs modulus, where the video extensometer employed
tracks the response in both directions throughout any given test.
There is only modest variation in the Youngs modulus in the
axial direction, with all experimentally determined values in
the range of the manufacturers reported value of 1241 MPa.
Similarly the yield stress, taken as the onset of the non-linear
response, is relatively insensitive to preconditioning in the
axial direction.
However, the Youngs modulus in the transverse directionis seen to decrease by as much as 86%, falling from 1140 MPa
initially to 160 MPa with 70% strain preconditioning. The
yield stress is also observed to fall off by 30% in this case.
No yield stresses are reported above Tg because, although the
response is not linear to failure, there is no onset of plastic
deformation; this is consistent with the polymers rubber-like
behavior in the soft state and its ability to recover from nearly
any applied strain up to failure.
Also evident from figure 2, and summarized in table 2,
is the sometimes substantial increase in failure strain upon
application of strain preconditioning. Below Tg there is a
significant increase in the failure strain in the axial direction. In
fact, with preconditioning, the SMP is capable of withstanding
nearly as much strain below Tg as it is above Tg. Accounting
for the preconditioned strain, the maximum strains at failurein the axial direction below Tg for the 40% and 70%
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Table 2. Failure strain as a function of preconditioned strain (zero offset).
Axial TransversePreconditionedstrain (%) Minimum (%) Maximum (%) Minimum (%) Maximum (%)
0 5.2 31.2 5.2 31.2Below Tg (23
C) 40 67.7 82.3 36.6 47.6
70 11.4 61.2 23.5 32.30 110.9 119.1 110.9 119.1
Above Tg (80C) 40 58.3 138.4 78.0 85.8
70 29.1 40.2 168.1 176.4
Table 3. Modulus of toughness as a function of preconditioned strain.
Axial (MJ m3) Transverse (MJ m3)Preconditionedstrain (%) Minimum Maximum Minimum Maximum
0 0.9 4.6 0.9 4.6Below Tg (23
C) 40 15.1 20.0 2.7 5.070 1.8 13.9 1.0 2.0
Above Tg (80C) 0 0.47 0.57 0.47 0.57
40 0.18 1.27 0.20 0.2870 0.04 0.15 0.08 0.12
preconditioned cases become 123% and 130%, respectively,
which is comparable to the isotropic above Tg case having a
maximum failure strain of 120%.
Directly related to the amount of strain the polymer
is capable of withstanding before failure is the modulus of
toughness, presented in table 3. As is evident, below Tg the
modulus of toughness in the axial direction is increased by
more than an order of magnitude with strain preconditioning.
4. Discussion
An SMP is frequently employed for its ability to sustain large
strain. More specifically, an SMP is often considered desirable
for design because it may be warmed, subjected to substantial
deformation with low forces, and then locked into the new,
load carrying configuration at a lower temperature. This shape
may be expected to support complex loads. The foregoing
experimental procedure employs strain preconditioning as a
means to explore the load carrying capability of the newly
locked-in shape.
Based on the experimental results of the previous section,for simple uniaxial design strategies it is appropriate to treat
the Youngs modulus as a constant below Tg. Further, while
the stiffness above Tg increases by a factor of three over the
range of preconditioning considered, as compared to the cold
state stiffness it may be appropriate to also treat this value of
Youngs modulus as a constant for uniaxial loading. However,
in SMP based designs carrying complex loads, the foregoing
clearly illustrates that assuming constant, isotropic stiffness
values above and below Tg would be ill-advised. Similarly, any
design that relies on SMP toughness may display unexpected
performance; in fact, in the case of toughness the material may
be under-utilized.
The following explanation is offered for the observedanisotropic response. It is proposed that during the
preconditioning above Tg the energy required for shear
between two adjacent polymer chains is greatly reduced,
allowing them to slide relative to one another and partially
align. This proposition is consistent with the partial polymer
chain alignment reported for other polymer systems at large
strains [20]. Once cooled, the response of the polymer in the
axial (aligned) direction will be dominated by the deformation
of the polymer chain covalent bonds. This is expected to
correspond with an increase in stiffness, but more importantly,the amount of energy required to break these aligned covalent
bonds will become significant.
Consider next the response in the transverse direction. It
can be argued intuitively that, if partial alignment results in
a stronger material in the aligned direction, then the cross-
links that enabled this alignment are necessarily less able to
support load. However, this intuitive argument alone fails to
adequately address the substantial degradation in transverse
stiffness. In addition, however, this point may also be argued
from Boltzmann statistical thermodynamics first principles.
If it is assumed that rotation about a given polymeric bond
is unrestricted, then the Helmholtz free energy is strictly a
function of the entropy, where the entropy is given as
S(r) = c + kln P(r), (5)
where c is a constant of integration, k is Boltzmanns constant,
and P(r) is the probability density function defining the
distance between polymer chain cross-links. One relatively
simple way to explore this is via the three-chain rule, which
essentially assumes that in the virgin state the polymer chains
will tend to align with each of the Cartesian axes [30],
S= 3
S(ro) + 2S(ro1/2) 3S(ro)
, (6)
where S is the change in entropy associated with an applieddistortion, is the number density of network chains, r0 is the
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root mean square of the distance between cross-links and =L/L i is the relative length of the sample upon deformation.
The first parenthetical term of equation (6) corresponds with
the axial response; the second parenthetical term corresponds
with the transverse response; the final parenthetical term
corresponds with the virgin state. The nominal stress f and
corresponding modulus [ f] of the system are then expressedas [37]
f = T
S
T
f= f
2 , (7)
where T is the temperature. For the general case presented
here, a normal distribution function, such as equation (8), is
utilized for P(r), the chain length probability density function.
P (r) = 1
2exp
(x )
2
22
, (8)
where is the standard deviation, is the expected value,
and x becomes r0 in the axial direction and r01/2in the transverse direction, as indicated in equation (6).
Substituting equation (8) into equation (5) and subsequently
into equation (6) yields
Saxial
= kr0
2(r0 ) (9)
Stransverse
= kr0
22
r0
1/2
, 3/2 (10)
where the entropic response with respect to distortion is
considered for the respective axial and transverse directions. In
this form, it is relatively easy to envision that the magnitude of
the axial term will increase with increasing axial deformation as all other terms in the expression are positive constants.
Further manipulation of equations (9) and (10) via equation (6)
only serves to multiply the expressions by terms that will
cancel in the resulting ratio of interest,
faxial =
2
r03 2
r0 1/2
ftransverse . (11)
Because r0 and are necessarily positive and is greater
than 1 for our tensile preconditioning, the numerator will
be larger than the denominator, yielding a coefficient greater
than 1. This supports the experimental observation that themodulus in the transverse direction is smaller than in the axial
direction with increasing strain. Further, because the terms in
the numerator are of higher order than the denominator, the
transverse properties decrease relative to the axial properties at
a correspondingly increased rate.
The details of the above discussion may be easily
manipulated. For instance, considerable detail could
be introduced to accommodate the multiphased nature of
Veriflex in comparison to the rubber elasticity basis of this
development; the Johnson family of distributions might have
been employed [38]; or more formally developed orthotropic
constitutive equations may have been offered [39]. In
addition, it should be noted that the above theory is knownto have increasingly significant errors above extension ratios
between 2 and 2.5, depending upon the polymer system [30].
However, despite the simplistic application of statistical
thermodynamics, the characteristic qualities of the analysis are
fixed. Thus first principles support the observed, substantial
degradation in transverse stiffness with the introduction of
preconditioning. The significance of choosing this highly
generalized construct is that it may be reasonably argued thatthe experimentally observed anisotropic trends in Veriflex
should be expected in any SMP, and for that matter, any
polymer employed in large strain applications.
5. Conclusions
With shape memory polymers being aggressively considered
for high strain applications, it is becoming increasingly
important that their three-dimensional characteristics be
quantified. When first partially aligning the polymer chains
with strain preconditioning above Tg, such as is likely tooccur in high strain applications, substantial variations in the
fundamental material properties are observed. These include
substantially decreased transverse stiffness and substantially
increased axial toughness (in some cases an order ofmagnitude). While the above results may necessitate the
use of somewhat more complex material models during the
material design process, the ability to manipulate directional
material stiffness and toughness could also become a powerful
design tool in itself. The foregoing offers insight into how the
property variation will manifest itself. Moreover, because the
physical mechanisms proposed for the observed response are
argued from principles applicable to any polymer material, theexperimental trends presented in this report are not expected to
be limited to the specific case of Veriflex.
Acknowledgments
The authors would like to acknowledge Dr Clark, for
his assistance and expertise; HRL Laboratories, LLC, for
their knowledge of shape memory polystyrenes and aid in
sample preparation techniques, and CRG Industries, LLC, for
supplying Veriflex and counsel.
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