high strain rate testing and modeling of polymers for...
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HIGH STRAIN RATE TESTING AND MODELING OF POLYMERS FOR USE IN
FINITE ELEMENT SIMULATIONS
Sean S. Teller, Jorgen S. Bergström, Gregory R. Freeburn, Veryst Engineering, Needham, MA
Abstract
Finite element analysis plays a crucial role in modern
engineering problems, enabling engineers to predict the
response of designed parts at any point in the design
process. Specifying a constitutive model that accurately
captures the mechanical response of a polymer material is
paramount to obtaining useful results. In order to
understand the capabilities of commercial FE packages
used to simulate problems involving polymers, we have
tested the uniaxial response of polyamide in tension and
compression over six decades of strain rate. We then
calibrated four constitutive models to the experimental
data: an Abaqus Parallel Rheological Framework model,
the LS-DYNA SAMP-1 model, the ANSYS Bergström-
Boyce model, and the PolyUMod Three Network model.
We compared the performance of the four models in
predicting the experimental data; the Three Network
model had the lowest error. Additionally, we compared
the runtime of a simple test case for each model; the
ANSYS Bergström-Boyce model being the fastest.
Introduction
The Finite Element (FE) method is an important and
widely used tool to design and analyze the response of
solid parts to real world loading conditions [1]. Accurate
specification of the constitutive model is important to
obtain applicable results. Polymers exhibit complex
mechanical behavior, including plastic flow, viscoelastic
flow, hysteresis, and strain-rate dependency. Viscoplastic
constitutive models developed for metals may not capture
the complete response of polymer materials, and models
developed specifically for polymers are often necessary
[1].
In the current work, we aim to examine the most
advanced constitutive models for polymers available in
three consumer FE codes: Abaqus®, ANSYS®, and LS-
DYNA®. Additionally, we examine an advanced
constitutive model available for those FE packages as a
user material through PolyUMod® (Veryst Engineering,
Needham, MA).
To analyze the constitutive models, we performed
uniaxial tension and compression tests on polyamide (PA)
specimens, with applied engineering strain rates from
0.001/s to 1250/s. We then calibrated the constitutive
models to the experimental data by minimizing the error
between experimental data and the model predictions with
MCalibration® (Veryst Engineering). The predictions
from the calibrated constitutive models are compared, as
well as the runtimes and potential tradeoffs for each
model.
Materials and Methods
Tension and compression specimens were waterjet
cut from 3.5 mm thick sheet stock PA (EMCO Plastics,
Cedar Grove, NJ). Low strain rate tests were performed
on ASTM D638 Type IV dogbones, while high strain rate
tests were performed on ASTM D638 Type V dogbones
[2]. Uniaxial compression tests were performed on right
circular cylinders with a 6.3 mm diameter and 3.5 mm
height.
Low strain rate tests (engineering strain rates below
1/s) were performed on an ADMET eXpert 2612 electro-
mechanical universal test machine (ADMET, Inc.,
Norwood MA). We performed uniaxial compression tests
with custom steel compression platens, while we
performed uniaxial tensile tests with wedge-style grips.
We measured specimen strain during compression tests
with a clip-on Epsilon 3542 axial extensometer attached
to the compression platens (Epsilon Technology Corp,
Jackson, WY). Prior to tension testing, specimens were
speckle patterned with black and white paint for use with
a Digital Image Correlation (DIC) system. Images were
captured with a Point Grey Gazelle digital camera (Point
Grey, Richmond, BC, Canada) and sample strains were
computed in post-processing using Correlated Solutions
Vic-2D (Correlated Solutions, Columbia, SC).
We performed high strain rate uniaxial tension and
compression tests with a purpose-built drop tower with
custom tension and compression fixtures, shown in Figure
1. The drop tower is similar in principle to drop towers
described in [3-4] and has been previously described in
[5]. We measured sample force with a dynamic
piezoelectric force transducer, and recorded the data using
an oscilloscope with computer interface. We recorded the
tests at or above 40,000 fps with a high-speed video
camera. We measured specimen strains during uniaxial
tension tests using DIC and Vic-2D software, while we
measured specimen strains during uniaxial compression
tests by tracking the motion of the loading platens using
fiducial markers. We synced specimen strains and stresses
post-experiment using MATLAB® (Mathworks, Natick,
MA).
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Figure 1. Veryst Engineering’s custom built drop tower.
After testing was complete, we calibrated the
constitutive models to the data using MCalibration®
(Veryst Engineering, Needham, MA). The software uses
an internal FE solver to perform single-element
simulations using the applied strain history as the input.
The stress history from the constitutive model is
compared to the stress history of the experimental data,
and the error is calculated as the difference. MCalibration
uses advanced non-linear search algorithms to minimize
the error and find the best fit to the data. MCalibration can
be used to calibrate models with the internal FE solver or
can utilize external solvers, including Abaqus, ANSYS,
LS-DYNA, COMSOL, and MSC.Marc.
Constitutive Models
Polymers, and in particular thermoplastics like PA,
exhibit complex, nonlinear viscoplastic material behavior
including rate-dependence, stress relaxation, and
hysteresis. Most commercial FE packages include
constitutive models that are specifically designed for
modeling the behavior of polymers, though not all
packages do. These models include effects not included in
classic metal plasticity models [1]. Here we outline one
built-in material model available in Abaqus, LS-DYNA,
and ANSYS, though this is not an exhaustive list. These
models were chosen as they provide the best fits to the
experimental data. Additionally, we describe a
constitutive model available in PolyUMod, a user material
library available in most major FE packages [6].
We chose the Parallel Rheological Framework (PRF)
model from Abaqus to represent the data [7]. The PRF
model is a nonlinear viscoplastic model consisting of
parallel networks of nonlinear springs and dashpots as
shown in Figure [2]. We chose a three network
configuration with three Yeoh hyperelastic springs and
two Bergström-Boyce (BB) viscous dashpots. Details on
the implementation of the model can be found in the
Abaqus Analysis User’s Guide [7].
Figure 2. Abaqus PRF model schematic.
We chose MAT_SAMP-1, the Semi-Analytical
Model for Polymers, for constitutive modeling in LS-
DYNA. The constitutive model uses look-up tables to
define a rate-dependent, isotropic, C-1 smooth yield
surface [8,9]. The user can include tension, compression,
shear, and biaxial tension data to create the yield surface,
though only tension data is required. Additionally, all
rate-dependence is specified through the tension load
curves – compression, shear, and biaxial tension load
curves need to be quasi-static test data [8]. For the PA
model, we chose to calibrate the constitutive model with
data from four tests: the 0.001/s compression data, and the
0.001/s, 0.1/s, and 300/s tension data. We used smoothed
and down-sampled raw experimental data to define the
lookup tables. Additionally, we used the ordinate offset
and abscissa scale factors of the LS-DYNA
*DEFINE_CURVE keyword to enable MCalibration to
modify the stress-strain curves to better fit the data [8].
We chose the Bergström-Boyce (BB) nonlinear rate-
dependent constitutive model to model the PA in ANSYS.
Although the model was originally designed for use with
elastomer-like materials, the constitutive model can
capture the response of some thermoplastics better than
many metal plasticity constitutive models [1]. The
constitutive model consists of two parallel networks,
shown in Figure 3. The spring elements are Arruda-Boyce
eight-chain hyperelastic models, and the dashpot is based
on reptational motion of molecules [6,10]. Details on the
implementation model can be found in the ANSYS User’s
Manual [11].
Figure 3. BB model schematic.
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We chose the Three Network (TN) model from the
PolyUMod® library to model the PA. The TN model is an
advanced thermomechanical nonlinear elastic-viscoplastic
model designed specifically for modeling thermoplastics
[1,6,12]. A rheological representation of the model is
shown in Figure [4]. The model consists of three parallel
networks comprised of nonlinear elastic springs and
nonlinear viscous dashpots. All springs are Arruda-Boyce
eight-chain hyperelastic elements, while the dashpots are
reptation-based viscous elements. The hyperelastic
response of network A also contains a term to model the
effects of the second strain invariant, set to 0 in the
current work. Additionally, the shear modulus of Network
B evolves linearly with the plastic strain in Network A,
softening the response post-yield [1,6,12].
Figure 4. PolyUMod TN model schematic.
Experimental Results
Figure 5 presents the results from uniaxial tension
experiments. Figure 5 shows the engineering stress versus
the engineering strain during the test, and the legend
entries show the engineering strain rates during the tests.
For the high strain rate tests, the average engineering
strain is reported as the average loading rate, as the strain
rate is not constant during the experiment due to dynamic
loading effects. All uniaxial tension tests were run to
specimen failure, and stress-strain histories in Figure 5 are
cut when failure is observed during the test. Figure 5
shows viscoplastic behavior of the PA – the yield stress
increases with increasing strain rate, though the Young’s
modulus does not vary significantly. Behavior post-yield
shows some material softening. Additionally, the PA
undergoes a ductile to brittle failure transition in the
strain-rate range investigated here.
Figure 6 presents the results from the uniaxial
compression experiments. The figure shows the
engineering stress versus the engineering strain during the
test, and the legend entries show the engineering strain
rate during the loading portion of the test. Cyclic uniaxial
compression tests were performed to examine the
unloading behavior of the material and to characterize the
stress relaxation that occurs in the material. Figure 7
shows an exemplar stress history for the 0.1/s cyclic
uniaxial compression experiments. The specimens were
loaded cyclically to 2.5%, 5%, 10%, 25%, and 50%
engineering strain. Prior to unloading, strain was held
fixed for 10 seconds to characterize the stress relaxation
of the PA. As shown in Figure 7, the material exhibited
substantial stress relaxation in 10 seconds. After stress
relaxation, specimens were unloaded to a low load (5N) at
the same engineering strain rate as the loading. Similar to
the tension experiments, the PA shows rate dependent
yield stress but little change in Young’s modulus.
Figure 5. Results for tension tests on PA samples.
Figure 6. Results for compression tests on PA samples.
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Figure 7. Exemplar stress history for a uniaxial cyclic
compression test.
Calibration Results
Constitutive model input files are not included due to
space limitations.
Abaqus PRF Model
Figures 8 and 9 present the results from the
constitutive model calibration for the Abaqus PRF model
in uniaxial tension and compression, respectively. The
figures show engineering stress versus engineering strain.
Experimental data is represented by solid lines, while
model data are shown as dashed lines. Additionally, the
coefficient of determination (R2) is shown on the plot.
These conventions are used in the remainder of this paper.
As shown in Figure 8, the Abaqus PRF model captures
the response of PA in tension quite well and has an R2 of
0.93. The strain-rate dependence of the yield stress is
captured well, as is the post yield behavior. In
comparison, the model is significantly less accurate in
compression with an R2 of 0.67. This is mainly due to the
unloading behavior of the PRF model – the model
overpredicts the unloading response of the material
significantly. The strain-rate dependence of the material
and post-yield behavior is captured well.
LS-DYNA SAMP-1 Model
Figures 10 and 11 present the results from the
constitutive model calibration for the LS-DYNA SAMP-1
model in uniaxial tension and compression, respectively.
The figures show engineering stress versus engineering
Figure 8. Calibration results for the Abaqus PRF model in
tension.
Figure 9. Calibration results for the Abaqus PRF model in
compression.
strain. The SAMP-1 model accurately captures the
monotonic uniaxial tension data, including the strain rate
dependence of the yield stress, yielding a high R2 value of
0.94. In uniaxial compression, the model accurately
captures the strain-rate dependence of the yield surface,
though over-predicts the unloading response of the
material. The model does not include viscoelastic effects
and assumes that unloading is elastic [9]. This brings the
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R2 value for compression tests to 0.64, though monotonic
data are well-captured.
Figure 10. Calibration results for the LS-DYNA SAMP-1
model in tension.
Figure 11. Calibration results for the LS-DYNA SAMP-1
model in compression.
ANSYS BB Model
Figures 12 and 13 present the results from the
constitutive model calibration for the ANSYS BB model
in uniaxial tension and compression, respectively. The
figures show engineering stress versus engineering strain.
The uniaxial tensile response of the model accurately
captures the strain-rate dependency of the yield stress at
all strain rates and the post-yield behavior with an R2
value of 0.92. In uniaxial compression, the model captures
the strain-rate dependence of the material but over-
predicts the unloading behavior compared to the
experimental behavior, with an overall R2 value of 0.75.
Figure 12. Calibration results for the ANSYS BB model
in tension.
Figure 13. Calibration results for the ANSYS BB model
in compression
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PolyUMod TN Model
Figures 14 and 15 present the results from the
constitutive model calibration for the PolyUMod TN
model in uniaxial tension and compression, respectively.
The figures show engineering stress versus engineering
strain. As shown in Figure 14, the TN model accurately
captures the response of PA in uniaxial tension with an R2
value of 0.94. Additionally, in uniaxial compression the
model captures the data well with an R2 value of 0.82.
This is mainly due to the TN model more accurately
predicting the cyclic uniaxial compression behavior,
particularly the stress relaxation and unloading to near-
zero load.
Figure 14. Calibration results for the PolyUMod TN
model in tension.
Discussion
Table 1 presents results comparing the coefficient of
determination for each calibrated model, showing the
results for all experiments, tension experiments only, and
compression experiments only. Table 1 shows that the TN
model more accurately predicts the experimental data
compared to the other models in both tension and
compression. The largest difference is due to the
improved performance in cyclic compression compared to
the other models, though tension results also show minor
improvements.
Although the accuracy of the constitutive models is
important to an FE problem, solution time must be
considered as well. More complex models generally
increase computing time for the problem and must be
considered. A simple FE model of an ASTM D638 Type
Figure 15. Calibration results for the PolyUMod TN
model in compression.
IV dogbone was created to run in each program to
compare the runtimes of the models. The models use
similar mesh geometries, loading conditions, boundary
conditions, and solver settings. Table 2 contains the
results for the model runtimes from these simulations. The
PolyUMod model was run in all solvers so that
comparisons can be made between models and between
FE programs. The TN model has a faster run time than the
Abaqus PRF model, but a slower run time than the LS-
DYNA SAMP-1 and the ANSYS BB models, though all
models have similar run times within the FE solver.
Table 1. Coefficients of determination for each model for
all load cases, tension, and compression.
An additional consideration for constitutive models is
in solver and element type support. The Abaqus PRF
model is supported for both implicit and explicit solvers
and all element types [7]. The LS-DYNA SAMP-1 model
is only available in the explicit solver [8]. Similarly, the
ANSYS BB model is only available in the implicit solver
[11]. Last, the implementation of the LS-DYNA SAMP-1
model is limited in that the material model is based on
lookup tables – the model does not include any
viscoelastic effects, and extrapolating outside the strain
Model
R2
All Tens. Comp.
Abaqus PRF 0.78 0.93 0.67
LS-DYNA SAMP-1 0.77 0.94 0.64
ANSYS BB 0.75 0.92 0.61
TN 0.87 0.94 0.82
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rates tested does not yield a change in material response
[8-9].
Table 2. Coefficients of determination for each model for
all load cases, tension, and compression.
Model
Runtime (m:ss)
LS-
DYNA
Explicit
Abaqus/
Explicit
Abaqus/
Standard
ANSYS
Implicit
Abaqus
PRF N/A 1:25 1:42 N/A
LS-DYNA
SAMP-1 3:58 N/A N/A N/A
ANSYS BB N/A N/A N/A 0:17
TN 5:59 1:00 0:52 0:52
In contrast, the PolyUMod TN model is supported by
all three commercial FE packages studied here. This
includes both implicit and explicit FE solvers for Abaqus
and LS-DYNA, though only the implicit solver of
ANSYS is currently supported [6]. In addition to solver
support, the TN model is available for all element types.
The ability to use a particular model in multiple solvers
may be beneficial – the TN model is available for use in
all products, so switching FE packages is not an issue for
the end user. The BB model is available, in some form, in
all the FE packages studied here, though the specific
implementations are different and may require material
recalibration or verification [6-8,11].
Conclusions
We tested PA in uniaxial tension and compression
over six decades of engineering strain-rates and calibrated
material models to the experimental data using
MCalibration. All calibrated models captured major
features of the material response, though unloading
response of material models native to Abaqus, ANSYS,
and LS-DYNA was less than satisfactory. The PolyUMod
model best captured the unloading response. All models
had similar runtimes in the native FE solver, including the
TN model. Additionally, the PolyUMod constitutive
model had significant advantages in element type and
solver capabilities – it is available for explicit and implicit
solvers and all element types. Overall, the PolyUMod TN
model is best suited to model the response of the PA.
References
1. J. Bergström, Mechanics of Solid Polymers, (2015).
2. ASTM International. ASTM D638-14, Standard Test
Method for Tensile Properties of Plastics (2014).
3. S. Gurusideswar, R. Velmurugan, N Gupta, Polymer,
86, 197-207 (2016).
4. C. Roland, J. Twigg, Y. Vu, P. Mott, 2007. Polymer,
48, 574 – 578 (2007).
5. S. Teller, E. Schmitt, J. Bergström, ASME IMECE
Proceedings (2016).
6. PolyUMod® 4.4.3, Veryst Engineering, LLC (2016).
7. Abaqus® (2016), Abaqus Documentation, Dassault
Systèmes, Providence, RI.
8. LS-DYNA® Theory Manual, 2016 June 25, LSTC Inc.
9. S. Kolling, A. Haufe, M. Feucht, P. Du Bois, LS-
DYNA Anwenderforum (2005).
10. J. Bergström, M. Boyce, Journal of the Mechanics
and Physics of Solids, 46, 931-954 (1998).
11. ANSYS® Documentation, Release 16.1, ANSYS, Inc.
12. J. Bergström, J. Bischoff, International Journal of
Structural Changes in Solids, 2, 31-39 (2010).
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