on the measurement of fracture toughness of soft biogel
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On the Measurement of Fracture Toughness ofSoft Biogel
H.J. Kwon, Allan D. Rogalsky, Dong-Woo KimDepartment of Mechanical and Mechatronics Engineering, University of Waterloo,200 University Avenue West, Waterloo, Ontario, Canada N2L 3G1
In this study, the rate dependent energy dissipationprocess and the fracture toughness of physical gelswere investigated using agarose as a sample material.Both the J-integral and Essential work of Fracture(EWF) methods were examined. To assess the quasi-static fracture toughness of gels, linear regression wasperformed on critical J (Jc) values at different loadingrates resulting in a quasi-static Jc value of 6.5 J/m2.This is close to the quasi-static EWF value of 5.3 J/m2
obtained by performing EWF tests at a quasi-staticloading rate (crosshead speed of less than 2 mm/min).Nearly constant crack propagation rates at low loadingrates, regardless of crack length, suggest viscoplasticchain pull-out is the fracture mechanism. At high load-ing rates failure was highly brittle, which is attributedto sufficient elastic energy accumulation to precipitatefailure by chain scission. We conclude that in physicalgels quasi-static fracture toughness can be evaluatedby both the J-integral and EWF methods provided theeffects of loading rate are investigated and accountedfor. POLYM. ENG. SCI., 51:1078–1086, 2011. ª 2011 Society ofPlastics Engineers
INTRODUCTION
Hydrogels can be classified by the types of crosslinks
joining chains together [1]. In chemical gels, the cross-
links between polymer chains are made of covalent
bonds, while physical gels are linked by secondary bonds
that are much weaker and more prone to break down
under applied mechanical stress. In most of them the net-
work is formed by biopolymers [2], e.g., proteins (gelatin,
elastin) or polysaccharides (agarose, alginates). Biopoly-
mer-based gels have been attracting substantial interest
motivated by their wide use in biomedical applications
such as drug delivery and tissue engineering [3, 4]. All
these implementations call for the accurate assessment
and control of their mechanical properties such as elastic
modulus and fracture behavior.
Elastic properties of gels have been extensively stud-
ied, both in the small- [2, 5] and large-deformation
regimes [6, 7]; while fracture studies have been mainly
concerned with crack nucleation [8] and ultimate strength
measurements [6, 7]. There are relatively few studies on
the fracture toughness (the material resistance to the prop-
agation of cracks and associated rate dependent energy
dissipation), partly due to the difficulty of applying con-
ventional fracture mechanics schemes to soft hydrogels.
Despite this, there is a fair degree of consensus regarding
the differences in fracture behavior between physical and
chemical gels.
In chemical gels, stiffness and toughness have been
found to be negatively correlated, i.e., the stiffer the gel
is, the less tough it becomes by both Tanaka et al. [9, 10]
using polyacrylamide and Kong et al. [11] using alginate.
On the other hand, Kong et al. showed in physical gels
the elastic moduli and toughness both increase with cross-
linking density. A reason for this is suggested by the
work of Baumberger et al. [12] who investigated the frac-
ture mechanisms of physical gels using gelatin. They
proposed that, unlike chemical hydrogels, physical gels
do not fracture by chain scission but by viscous pull-out
of whole chains from the network via plastic yielding of
the cross-links. This accounts for the dependence of
toughness on crack tip velocity.
Though the above studies qualitatively agree, the
measured energy dissipation values are not necessarily
comparable due to the limitations of the testing methods
employed. Complex phenomena inherent in hydrogel frac-
ture such as viscous deformation, stress relaxation and
large plastic deformation prevent the adoption of tough-
ness measures such as the stress intensity factor [13] or
energy release rate which are based upon Linear Elastic
Fracture Mechanics (LEFM) theory. Also the softness of
the gels prevents the use of the common contact based
strain measurement schemes. To cope with gel softness,
Tanaka et al. [9, 10] measured the fracture energy of gels
using a modified version of the tearing energy concept
proposed for elastomers by Rivlin and Thomas [14],
based on the similarity between elastomers and chemical
gels. This scheme is an extension of Griffith’s approach
Correspondence to: H.J. Kwon; e-mail: [email protected]
Contract grant sponsor: Natural Sciences and Engineering Research
Council of Canada (NSERC).
DOI 10.1002/pen.21923
Published online in Wiley Online Library (wileyonlinelibrary.com).
VVC 2011 Society of Plastics Engineers
POLYMER ENGINEERING AND SCIENCE—-2011
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and is equivalent to the energy rate interpretation of the
J-integral [15]. However, under this scheme tearing
energy is coupled with the energy for plastic deformation
occurred at the sharply bent corner adjacent to the crack
tip. Therefore, this scheme is not suitable to measure the
toughness of physical gels where plastic deformation
energy is large compared with the fracture energy. Also
this scheme is not regarded as a standard procedure to
assess the fracture toughness.
Baumberger et al. [12] overcome the challenges posed
by hydrogel softness through the use of optical techni-
ques to measure crack position and velocity. They were
able to assess the quasi-static toughness using a linear
regression technique based on the observation that the
energy release rate G is linearly proportional to crack ve-
locity. A constant crack speed was required for them to
extrapolate the average fracture energy release rate (frac-
ture energy divided by fracture area) to zero crack speed.
For this reason, all measurements of crack growth were
taken well after crack initiation in the center of rather
large specimens. However, in most of the fracture pro-
cess, the crack speed as well as energy release rate varies
with the crack growth; therefore, their approach is limited
to special cases where crack speed can be assumed
constant.
The essential work of fracture (EWF) method [16–18]
employed by Kong et al. [11] for gel study is more gener-
ally applicable. It overcomes the difficulty posed by plas-
tic deformation by separating the essential work (that con-
sumed for crack growth within process zone) from the
nonessential work (that dissipated outside the process
zone) through empirical dimensional analysis. It also has
the advantage that it can use crosshead force and dis-
placement data from a standard tensile tester. Unfortu-
nately this method is rather cumbersome requiring several
tests to be performed at differing initial ligament widths
before enough data are available for the mathematical
manipulation. Its accuracy is also dependent on the
underlying assumptions of the derivation which does
not consider the effects of loading rate in its formulation,
a potential problem in physical gels, most of which
demonstrate high rate-dependency in both stiffness and
toughness.
The traditional method for studying the fracture tough-
ness of ductile materials is the J-integral method which
can handle the relatively large plastic zone developed
around the crack tip. It does not seem to be widely
adopted for hydrogels, likely due to the difficulty in
applying the conventional measurement scheme to soft
and fragile hydrogels. This can be overcome by using op-
tical techniques to their full potential. The digital image
correlation (DIC) method not only overcomes the issues
involving specimen contact but also allows the complete
deformation field in the vicinity of the crack tip to be
directly observed. With this data, the critical strain energy
release rate (Jc) can be obtained in a very generally appli-
cable manner.
EXPERIMENTS
Agarose Preparation
Agarose sols were prepared by dispersing the agarose
powder (Product codes: A426-05, CAS No: 9012-36-6,
J. T. Baker) in standard 0.5 TBE buffer (Tris/Borate/EDTA,
ph 8.0) at 2% concentration (% w/v, assuming powder to be
100% agarose). The agarose solution was heated to 958Cfor 30 min and poured into a Teflon mold. It was then
cooled quickly to 108C. Preliminary tests indicated no
measurable change in mechanical properties after 30 min
casting time. Based on this, a conservative casting time of
�1 h was adopted for the remainder of the study. After
casting, specimens were immersed in buffer for 30 min to
allow swelling and tested immediately thereafter.
Test Scheme
Identical rectangular gel plates with the dimensions of
75 mm wide (W), 100 mm long (H), and 2 mm thickness
(t0) were prepared for both types of fracture tests, EWF
and J-integral. Specimens were held on the top and the
bottom by custom built grips machined from Delrin
(Dupont) faced with sandpaper to create a coarse gripping
surface.
The following gripping procedure was employed to
prevent damage to specimens prior to testing: (1) Upper
grip was removed from the load frame and attached to
the top part of the specimen in a jig that allowed the
specimen to be supported in a horizontal orientation. (2)
Upper grip holding the specimen was assembled into the
load frame and the bottom part of the specimen was
loosely held by the lower grip. (3) Load zeroed and the
lower grip tightened. (4) Compressive force developed by
gripping was released by moving the crosshead upwards
at 0.2 mm/min until zero load. This restored the specimen
to be vertically straight from the slightly bent shape
obtained during gripping.
Due to the fragility of the material notches were only
made after gripping using a fresh razor blade and a cus-
tom-built jig. Notch length (a in Fig. 1a) was approxi-
mately a half of the specimen width in single-edge-
notched tension (SENT) specimens for J-integral tests.
For EWF tests, the ligament length (L0 in Fig. 1b) of dou-
ble-edge-notched tension (DENT) specimens was varied
from 15t0 (30 mm) to 3t0 (6 mm). The final dimensions
were measured by counting the number of pixels in the
image captured by high resolution CCD camera (1028 31008 pixels, STC-CL202A, SENTECH).
As shown in Fig. 2a, fine chalk powders were
sprinkled on the surface of the specimens before the tests
to produce the patterning required for DIC. Tests were
conducted at ambient environment using a TA.XT Plus
load frame (Stable Micro Systems), with the force and
displacement being recorded. Crosshead speed was varied
from 1 mm/min to 100 mm/min. For each fracture
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experiment, a uniaxial specimen was also prepared from
the same batch and tested following the protocol proposed
in our previous study [6].
METHODS
Digital Image Correlation
DIC [19] is a robust experimental method enabling the
measurement of displacement field by tracking multiple
points on the surface. The surface is usually decorated with
speckle patterns, and the tracking is performed by comparing
the patterns in the digital images before and after deforma-
tion. This method has many advantages over conventional
methods using contacting sensors, such as being capable of
evaluating the strain field in a large domain without contact-
ing material. It can also be applied to various length scales
as long as proper speckle pattern can be generated on the sur-
face, which is a very useful feature when the preparation of
large specimens is untenable or very expensive.
Among the various image tracking algorithms, such as
cross-correlation [19], gradient descent search [20], snake
method [21], and sum of squared differences [22], the fast
normalized cross-correlation algorithm [23] was adopted
for this study because of its computational efficiency and
robustness to lighting conditions [24].
In this practice, the reference template is chosen from unde-
formed image. Its location in the deformed image is found by
performing pixel-by-pixel comparison of intensity values
using the following normalized cross-correlation formula
gðu; vÞ ¼P
x;y½f ðx; yÞ � f u;v�½tðx� u; y� vÞ � t�fPx;y½f ðx; yÞ � f u;v�2
Px;y½tðx� u; y� vÞ � t�2g0:5
(1)
where f is the intensity of deformed image, t the intensity of
reference template, t mean of the reference template, fu,vmean of the image overlapped by the reference template,
(u,v) current location of the reference image, and g(u,v) cor-
FIG. 1. Specimens used in this study: (a) Single-edge-notched tensile (SENT) specimen for J-integral test,and (b) double-edge-notched tensile (DENT) specimen for EWF test.
FIG. 2. (a) Undeformed SENT specimen with the initial grids (þ) gen-
erated around the J-integral path, and (b) integration paths around the
crack tip for the calculation of J-integral.
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relation coefficient at (u,v). The new location in the deformed
image is where the maximum g(u,v) occurs. By tracking
the movement of multiple reference templates, the displace-
ment fields in a large domain can be estimated. This algo-
rithm was coded into internally developed DIC Matlab code.
J-integral Evaluation
For J-integral testing, the DIC method was adopted to
evaluate the displacement and strain field on the images
photographed by CCD camera during the test. As a first
step, the initial notch and the J-integral path around the
notch tip were defined on the image of an undeformed
SENT specimen, as shown in Fig. 2a. Initial grids (þ)
were generated within the rectangular regions of interest
enclosing the path. Then, the sub-images around the grid
points in the deformed image (not shown) were correlated
to sub-images in the reference (undeformed) image using
DIC algorithm to estimate the displacements u and v at
the grid points. By smoothing the in-plane displacement
components (u, v) from DIC [25], the strain components
along the path were determined using infinitesimal strain
tensor in accordance with the assumption of J-integralderivation as:
eij ¼ 1
2
quiqXj
þ qujqXi
� �(2)
where ui is the displacement at each grid and Xi material
coordinate. Since the J-integral path is relatively distant
from the crack-tip, the differences between finite and in-
finitesimal strain tensors along the path are less than 3%.
Conventionally, Hooke’s law based on linear elasticity has
been used to determine the stresses and the energy from strains.
However, our previous study [6] indicates that the stress-strain
behavior of agarose follows the nonlinear relationship as
s ¼ c1 eþ c2 e2 (3)
where c1 and c2 are fitting constants, s and e are the stress
and the strain in the loading direction, respectively. Since
this relationship was estimated from uni-axial tension test,
the stress and strain in Eq. 3 can be regarded as effective
(or equivalent) stress r and effective strain e.It can be assumed that agarose gel is almost incom-
pressible (Poisson ratio m � 1/2) [12] and that a plane-
stress condition, and monotonic loading exist in the J-in-tegral test [26]; thus, the deformation theory of plasticity
was invoked as [27]:
sxx ¼ 4
3
�s�eðexx þ 1
2eyyÞ
syy ¼ 4
3
�s�eðeyy þ 1
2exxÞ
sxy ¼ 2
3
�s�eexy
(4)
where e in Eq. 4 is
�e ¼ffiffiffi2
p
3
�ðexx � eyyÞ2 þ ðeyy � ezzÞ2 þ ðezz � exxÞ2
þ 6 ðe2xy þ e2yz þ e2zxÞ�1=2
ð5Þ
and r is from Eq. 3.Consider the J-integral along the contours around the
crack tip, composed of horizontal and vertical paths as
shown in Fig. 2b. The J integral can be evaluated along
these paths as [28]:
J ¼ JV1 þ JH2 � JV2 � JH1
JV1 ¼ZV1
½w� ðsxxexx þ sxyqvqxÞ�dy
JV2 ¼ZV2
½w� ðsxxexx þ sxyqvqxÞ�dy
JH1 ¼ �ZH1
ðsyy qvqxþ sxyexxÞdx
JH2 ¼ �ZH2
ðsyy qvqxþ sxyexxÞdx
(6)
where w is the strain energy density, and u and v the dis-
placement in x and y direction, respectively. The strain
energy density can be approximated as
w ¼Z �e
0
�s d�e (7)
Essential Work of Fracture
The EWF concept is the scheme to estimate the
fracture toughness of ductile materials that involve large
plastic deformation prior to fracture [16–18]. In this
concept, the total work provided to fracture, Wf, is clas-
sified into two parts. The first part is the work for
deforming the region around the ligament, Wp, which is
proportional to the volume of deformation zone. Since
the width of the deformation zone is proportional to the
initial ligament length [16], Wp is proportional to L20 3t0 where L0 is initial ligament length in Fig. 1b and t0initial thickness. The second part is the essential work
required for the formation of fracture surface, We,
which is proportional to the cross sectional area of the
ligament (L0 3 t0).From energy equilibrium, Wf is the sum of the two
parts of energy consumption as:
Wf ¼ We þWp ¼ weL0t0 þ b wpL20t0 (8)
where we is the specific EWF, wp the average deformation
work, and b the shape factor for the deformation zone.
By measuring the total work of fracture for specimens
of different ligament lengths, and dividing Wf by the
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ligament cross sectional area (L0 � t0), the specific work
of fracture, wf, can be expressed as:
wf ¼ we þ b wp L0 (9)
The specific EWF, we, which represents the fracture
toughness can then be determined by extrapolating wf to
zero ligament length.
RESULTS AND DISCUSSION
J Integral Evaluation
The constants c1 and c2 in Eq. 3 as estimated from uni-
axial tension tests were 150 and 2200 kPa, respectively. In
our previous study [6], it was observed that this constitutive
relation is relatively insensitive to the crosshead speed
range used in this study (1 mm/min �100 mm/min).
J-integral values computed along the path in Fig. 2a
are plotted in Fig. 3. This test was conducted at a cross-
head speed of 10 mm/min. Close investigation of the
images revealed that the crack was initiated at the
moment indicated by the arrow (image no. 54 in Fig. 3).
The small discontinuity between this and the subsequent
point (image no. 55 in Fig. 3) is attributed to sudden
crack development. The J-integral value on this image is
14.95 J/m2, which is taken as the critical J-integral, Jc,for crack initiation at this crosshead speed.
According to the definition of J-integral [28], the
J-integral should be path-independent, i.e., constant
along any path around the notch. To investigate the path
dependence of the Jc estimated by DIC method, multiple
J paths were generated on the image at which the crack
initiated (image no. 54), as shown in Fig. 4a, and J-inte-grals were calculated along each path. As can be seen in
Fig. 4b, the J-integral values for all paths are reasonably
consistent with the average value of 14.62 6 0.68 J/m2.
Therefore, J-integral value evaluated by the DIC method
is path-independent.
Quasi-Static Jc
J-integral was originally formulated based on the
assumption of quasi-static fracture [28] where thermody-
namic energy equilibrium holds. The general form of
energy equilibrium in cracked body is given by:
DW ¼ DEþ DK þ DG (10)
where DW is the increment of external work supplied to
the body, DE and DK are the changes of the internal
energy and kinetic energy, and DG is the change of irre-
versibly dissipated energy. The internal energy E com-
prises elastic strain energy Ue and plastic deformation
energy Up.
Assuming energy dissipation occurs only through
quasi-static fracture process (DK � 0 in Eq. 10), energyrelease rate G or J can be defined as:
J ¼ dW
dA� dUe
dA¼ dG
dAþ dUp
dA(11)
where dA is crack area increment. Note that G is for
linear elastic materials (Up � 0), while J for nonlinearFIG. 3. Variation of J-integral with crack growth.
FIG. 4. (a) Deformed SENT specimen with multiple J-integral paths
generated, and (b) the critical J values (Jc) for different paths in (a).
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elastic materials. Since nonlinear elastic and plastic
stress-strain curves are not discernible in monotonically
increasing load, J can be also applied to elasto-plastic
materials where a part of the energy is dissipated by plas-
tic deformation (Up . 0). Under mode I loading, the J-in-tegral fracture criterion for crack initiation takes the form
J ¼ Jc where Jc is the quasi-static fracture toughness. The
implicit restrictions of this criterion are:
i. Energy dissipation rate with respect to time ( _C) is higherthan or equal to energy supply rate ( _W) so that the meas-
ured J value represents the instantaneous energy release
rate of a cracked body at the moment, and
ii. Jc is rate-independent. Otherwise, a separate scheme to
decouple K from J in Eq. 11 needs to be arranged.
If the fracture process or estimated J value does not
conform to these restrictions, the aforementioned J-inte-gral method may not be a suitable testing scheme and the
estimated Jc is not true fracture toughness.
The fracture process in agarose was examined by
observing the crack growth behavior in a separate SENT
test. In this test, SENT specimens with an initial notch
(Fig. 5a) were loaded in tension by moving the crosshead
upward. As soon as crack initiation was observed at the
notch tip, the crosshead was arrested (Fig. 5b). If it is a
quasi-static fracture conforming to the restriction (i), thecrack should stop growing immediately or shortly aftercrosshead arrestment, since the external energy supply,dW, in Eq. 11 is zero so that J falls below Jc, as strainenergy is dissipated by crack growth. However, crackgrowth continued at a slow but almost constant speed(Fig. 5c), to the end of the specimen (Fig. 5d). Repeatedtests revealed that once crack was initiated, the crackalways propagated through the remaining body of thespecimen regardless of initial notch length or notch shape.This suggests that _C is much less than _W in the crack
nucleation and development process; thus, much larger
strain energy is always accumulated before crack initia-
tion than that for crack development across the entire
specimen width. Therefore, the fracture process in agarose
is not quasi-static and the Jc estimated by the above J-in-tegral scheme should not be the quasi-static fracture
toughness.
The rate effect on Jc was investigated by performing
the fracture tests at various crosshead speeds ranging from
1 to 100 mm/min, and the results are presented in Fig. 6.
The variation of Jc against loading rate clearly demon-
strates that fracture toughness is not constant, but a func-
tion of loading rate. A similar trend was also found in the
literature [29] in a study on metals. Our previous study
on agarose [6] elucidated that ultimate stress and strain of
FIG. 5. The crack growth behavior: initial notch (a) was opened and crack started growing as the crosshead
moved upward. Crosshead was arrested at (b), but the crack kept growing (c) to the end of the specimen (d).
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agarose specimen under uniaxial tension have power law
relationships with crosshead speed, i.e. linear relationship
on log-log scale. Since Jc is the critical strain energy
release rate corresponding to the material resistance to
crack initiation, where strain energy is given as stress
times strain, Jc is expected to follow a similar power law
relationship. As this is the case in the high speed fracture
(HSF) region of Fig. 6, the second restriction regarding
rate independence of fracture toughness is also not met,
and a scheme for stripping rate dependency needs to be
arranged.
From the above observations, it can be hypothesized
that if the loading rate becomes extremely small, _Cbecomes comparable with _W and quasi-static energy
equilibrium can be achieved to meet the first restriction.
Then, the Jc value at this equilibrium condition may rep-
resent material resistance at quasi-static fracture, i.e.,
true fracture toughness. Figure 6 illustrates that the trend
of Jc versus crosshead speed changes as the crosshead
speed decreases. In HSF region, Jc decreases almost lin-
early in the log-log plot with the decrease of crosshead
speed, as indicated by the inclined solid trend line in
Fig. 6. If the crosshead speed is less than 10 mm/min,
Jc decreases very rapidly until it reaches 2 mm/min, as
presented in the transition region in Fig. 6. A linear
trend is still maintained in this region. Below 2 mm/
min, Jc is almost constant, as illustrated by the horizon-
tal solid trend line in the low speed fracture (LSF)
region. Extrapolating to the zero abscissa using linear
regression the y-intercept is 6.5 J/m2. Since the fracture
process and estimated Jc satisfy both restrictions, this
value can be regarded as true Jc, a quasi-static fracture
toughness of 2% agarose.
Essential Work of Fracture
EWF method has much less stringent restrictions than
LEFM based methods or J-integral. Plastic energy dissi-
pation is allowed in a much larger scale, since it is to
be decoupled from the specific EWF, we, representing
fracture toughness, by linear regression method.
Therefore, this approach can be applied to the fracture of
various materials with diverse ductility. However, EWF
method also does not consider the rate-dependence in its
formulation.
The rate dependent fracture behavior of agarose gel
was investigated first by comparing load-displacement
curves of DENT specimens with 30 mm ligament length
tested at various crosshead speeds: 1 mm/min, 10 mm/
min, and 100 mm/min. The initial parts of load-displace-
ment curves from different loading rates are almost over-
lapped one another up to 2 mm displacement, as pre-
sented in Fig. 7. This may be attributed to the relatively
insensitive stress-strain relationship to the loading rate, as
observed in our previous study [6]. However, crack initia-
tion, crack growth and fracture behaviors were signifi-
cantly varied by the loading rate. At 100 mm/min cross-
head speed, crack initiated at around 3 mm displacement.
Interestingly, the load kept increasing almost linearly even
after crack initiation until the last moment of fracture at
which highly brittle failure occurred with a loud noise. In
this fracture process, a large amount of strain energy was
accumulated during crack growth, and was released in the
form of rapid failure, retraction, vibration, and sound at
the final fracture. As described above, this was caused by
the unbalance of energy flow in crack growth with energy
dissipation rate ( _C) being much lower than energy supply
rate ( _W). Since these energies are not scalable as other
energies in Eq. 8, the EWF method is not valid for this
type of fracture behavior.
On the other hand, the fracture test at 1 mm/min cross-
head speed demonstrated significantly different fracture
behavior. At this loading rate, crack initiation happened
much earlier at around 2 mm crosshead displacement.
This is consistent with the decreasing trend of Jc with the
decrease of loading rate in Fig. 6. As soon as a crack was
initiated, the load started decreasing, suggesting that the
FIG. 6. The variation of Jc value with respect to crosshead speed.
FIG. 7. Load-displacement curves from the fracture tests using DENT
specimens with 30 mm ligament length at the crosshead speeds of
1 mm/min (^), 10 mm/min (&) and 100 mm/min (~).
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energy dissipation rate ( _C) and energy supply rate ( _W)
were relatively balanced and energy equilibrium was
maintained. Note that the shape of the load-displacement
is typical of quasi-static fracture of ductile materials [30]
to which EWF method has been successfully applied.
Based on this fracture behavior, EWF tests were
performed employing 1 mm/min crosshead speed to yield
the specific EWF value (we) as the quasi-static fracture
toughness.
The specific work of fracture wf was calculated using
the area under the load-displacement curve, and plotted in
Fig. 8 with respect to ligament length L0. Figure 8 clearly
shows a linear relationship between wf and L0 for the liga-
ment length used for this study (6 mm � L0 � 30 mm).
The y-intercept at zero ligament length corresponds to we
that is 5.3 J/m2 with the correlation coefficients (R) for
the curve fitting being 0.9991. This EWF value is reason-
ably close to the quasi-static Jc value, 6.5 J/m2, evaluated
above.
Dynamic Fracture Behavior of a Physical Gel
In most materials, crack tip velocity is very low at the
crack initiation stage, but accelerates with crack growth,
reaching the maximum at the final stage of the fracture.
In strong contrast to this, we observed that in the fracture
of physical gels, crack speed is almost constant or
increases at a much slower rate than that predicted by
LEFM [12]. This may be closely related to the positive
rate-dependence of fracture toughness in these materials.
Conventional fracture mechanics suggests that cracks
begin to move when the potential energy released by a
unit extension of a crack (middle term in Eq. 11) becomes
equal to critical fracture toughness Jc. Even if this condi-
tion of energy balance predicts the onset of motion, once
a crack starts to move the kinetic energy due to material
motion around the moving crack has to be taken into
account. Accounting for this energy led to the equation of
motion for a crack [31–33] as
V ¼ffiffiffiffiffiffi2pk
rc0 1� a0
a
� �� 0:38c0 1� a0
a
� �(12)
where c0 ¼ffiffiffiffiffiffiffiffiffiE=q
p, is the speed of sound for one-dimen-
sional wave propagation, k is a function of m [34], and a0the initial current crack length given by
a0 ¼ 2EJcps2f
(13)
Equation 12 predicts that a crack should continuously
accelerate as a function of its instantaneous length to a
limiting, but finite, asymptotic velocity. In 2% agarose
gel, c0 is around 14 m/s so that the asymptotic velocity is
around 5.3 m/s. This asymptotic limit can be reached by
either increasing the amount of energy driving the crack
or by reducing the fracture toughness to zero. Note that
Eq. 12 was derived based on rate-independent fracture
toughness Jc in the framework of LEFM.
Baumberger et al. [12] proposed that the physical gels
are fractured by viscous pull-out of whole polymer chains
from the network via plastic yielding of the cross-links. The
viscous nature of this fracture mechanism leads to the
increase of fracture energy with increased crack tip velocity
in their experiments. According to Eq. 12, a crack is initi-
ated at an infinitesimally low velocity, as a � a0. If Jc is
constant, V will increase as a0/a decreases with the crack
growth. However, in the physical gels that are fractured by
chain pull-out mechanism, Jc increases with V, and hence
a0 does. This in turn lowers the crack speed and energy dis-
sipation rate ( _C) in the fracture of physical gels compared
with the materials having rate-independent fracture tough-
ness. As a result, the energy supply rate ( _W) usually
exceeds the energy dissipation rate ( _C) and much larger
strain energy is accumulated within the gel than that
required for fracture, unless _W is fairly low as in the test
at 2 mm/min crosshead speed for 2% agarose gel as
described above. Previous studies [9, 12, 16] employed ap-
proximate scheme to compute fracture toughness using
Jc ¼ W/(A0) where A0 is the cracked area; however, it may
yield erroneous result overestimating the fracture tough-
ness, since W is much larger than fracture energy.
It needs to be mentioned that the fracture at 100 mm/min
in Fig. 7 showed quite brittle and unstable behavior with
extremely high fracture energy, which is significantly differ-
ent from those at lower loading rates. At this high loading
rate, _W is much larger than _C, thus most of the supplied
energy is piled up as an elastic strain energy. We speculate
that this allows the stored strain energy to reach the critical
energy level for the failure by chain scission, resulting in
rapid crack growth and highly brittle behavior, as opposed
to the slow and stable failure by chain pull-out mechanism
at low strain rate.
FIG. 8. Specific work of fracture (wf) from the fracture tests on DENT
specimens as a function of ligament length.
DOI 10.1002/pen POLYMER ENGINEERING AND SCIENCE—-2011 1085
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CONCLUSIONS
The evaluation of fracture toughness of hydrogels is
often very challenging due to the difficulty of testing as
well as lack of standard testing methods. We evaluated
fracture toughness of a physical hydrogel using 2% aga-
rose, and adopting the J-integral test based on DIC
method. The quasi-static fracture toughness was deter-
mined by linear regression on critical Jc values with
respect to loading rate. When this was compared with
EWF results obtained using a quasi-static equilibrium
condition, the quasi-static we was found to be reasonably
close to the quasi-static Jc value. Rate dependent fracture
behavior of physical gels was considered. At low speeds,
results were consistent with the chain pull-out mechanism,
while at high speeds, elastic energy accumulated faster
than could be dissipated by crack growth resulting in brit-
tle fracture likely due to chain scission.
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