Fracture behavior of lithia disilicate- and leucite-based ceramics
Fracture behavior of lithia disilicate- and leucite-based ceramics
Fracture behavior of lithia disilicate- and leucite-based ceramics
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Dental Materials (2004) xx, xxx–xxx<br />
<strong>Fracture</strong> <strong>behavior</strong> <strong>of</strong> <strong>lithia</strong> <strong>disilicate</strong>- <strong>and</strong><br />
<strong>leucite</strong>-<strong>based</strong> <strong>ceramics</strong><br />
Alvaro Della Bona a, *, John J. Mecholsky Jr. b , Kenneth J. Anusavice c<br />
a School <strong>of</strong> Dentistry, The University <strong>of</strong> Passo Fundo, P.O. Box 611/613, Passo Fundo, RS 99001 970, Brazil<br />
b Department <strong>of</strong> Material Sciences <strong>and</strong> Engineering, University <strong>of</strong> Florida, Gainesville, FL, USA<br />
c Department <strong>of</strong> Dental Biomaterials, University <strong>of</strong> Florida, Gainesville, FL, USA<br />
Received 8 July 2003; received in revised form 3 February 2004; accepted 19 February 2004<br />
KEYWORDS<br />
Structural reliability;<br />
<strong>Fracture</strong>; Fractography;<br />
<strong>Fracture</strong> toughness;<br />
Weibull modulus<br />
Introduction<br />
The appeal <strong>of</strong> <strong>ceramics</strong> as structural dental<br />
materials is <strong>based</strong> on their esthetics, low density,<br />
high hardness, chemical inertness, <strong>and</strong> wear resistance.<br />
A major goal <strong>of</strong> ceramic research <strong>and</strong> development<br />
is to produce stronger, tougher <strong>ceramics</strong><br />
that are structurally reliable in dental applications.<br />
Limited information is available on the fracture<br />
<strong>behavior</strong> <strong>and</strong> toughness <strong>of</strong> hot-pressed dental<br />
*Corresponding author. Tel.: þ55-54-3115142; fax: þ55-54-<br />
3168403.<br />
E-mail address: dbona@upf.br<br />
ARTICLE IN PRESS<br />
www.intl.elsevierhealth.com/journals/dema<br />
Summary Objective: This study was designed to characterize the fracture <strong>behavior</strong> <strong>of</strong><br />
<strong>ceramics</strong> <strong>and</strong> test the hypothesis that variation in strength is associated with a<br />
variation in fracture toughness.<br />
Methods: The following four groups <strong>of</strong> 20 bar specimens (25 £ 4 £ 1.2 mm) were<br />
fabricated (ISO st<strong>and</strong>ard 6872): E1, a hot-pressed <strong>leucite</strong>-<strong>based</strong> core ceramic<br />
(IPS Empress); E2, a hot-pressed <strong>lithia</strong>-<strong>based</strong> core ceramic (IPS Empress 2); ES, a<br />
hot-pressed <strong>lithia</strong>-<strong>based</strong> core ceramic (Experimental); <strong>and</strong> GV, a glass veneer (IPS<br />
Empress2 body). Specimens were subjected to four-point flexure loading in 37 8C<br />
distilled water. Fractographic analysis was performed to determine the fracture origin<br />
ðcÞ for calculation <strong>of</strong> fracture toughness ðK ICÞ: Weibull analysis <strong>of</strong> flexure strength ðsÞ<br />
data was also performed.<br />
Results: Differences in mean s <strong>and</strong> K IC were statistically significant for E1 <strong>and</strong> GV<br />
ðp , 0:05Þ: These differences are associated with processing effects <strong>and</strong> composition.<br />
Significance: The higher mean s <strong>and</strong> K IC values <strong>of</strong> E2 <strong>and</strong> ES core <strong>ceramics</strong> suggest<br />
potentially improved structural performance compared with E1 although the Weibull<br />
moduli <strong>of</strong> E1 <strong>and</strong> E2 are the same.<br />
Q 2004 Academy <strong>of</strong> Dental Materials. Published by Elsevier Ltd. All rights reserved.<br />
<strong>ceramics</strong>. Brittle fracture is a complex process. 1,2<br />
Quantitative fractographic analysis facilitates the<br />
identification <strong>of</strong> fracture mechanisms through the<br />
use <strong>of</strong> fracture mechanics. 3<br />
<strong>Fracture</strong> toughness is <strong>of</strong>ten used to characterize<br />
the fracture resistance <strong>of</strong> brittle materials 4–6 <strong>and</strong> it<br />
is usually controlled by the fracture in Mode I<br />
(opening mode, tensile load). Irwin 16 defined<br />
failure at the point when the Mode I stress intensity<br />
(KI) reaches or exceeds a critical value ðK I $ K ICÞ:<br />
The critical stress intensity factor ðK ICÞ is in many<br />
cases a material constant <strong>and</strong> is one measure <strong>of</strong> the<br />
toughness <strong>of</strong> the material, i.e. the resistance<br />
to crack propagation. Therefore, the fracture<br />
0109-5641/$ - see front matter Q 2004 Academy <strong>of</strong> Dental Materials. Published by Elsevier Ltd. All rights reserved.<br />
doi:10.1016/j.dental.2004.02.004
2<br />
Figure 1 Diagram <strong>of</strong> the typical fracture surface features occurring in brittle materials. The regions are not drawn to<br />
scale. Adapted from Mecholsky (1993). 27<br />
toughness or critical stress intensity factor ðK ICÞ can<br />
<strong>of</strong>ten be determined using the Griffith–Irwin<br />
equation:<br />
K IC ¼ Ys fc 1=2<br />
ð1Þ<br />
where Y is a geometrical factor that accounts for<br />
the location <strong>and</strong> geometry <strong>of</strong> the critical flaw <strong>and</strong><br />
type <strong>of</strong> loading, 7 s f is the stress at fracture, <strong>and</strong> c is<br />
the radius <strong>of</strong> an equivalent semicircular flaw for a<br />
semi-elliptical crack <strong>of</strong> semiminor axis ‘a’ <strong>and</strong><br />
semimajor axis ‘b’ (Fig. 1). 8,9<br />
Little information is available on the structural<br />
reliability <strong>of</strong> hot-pressed <strong>lithia</strong> <strong>disilicate</strong>-<strong>based</strong> <strong>and</strong><br />
<strong>leucite</strong>-<strong>based</strong> <strong>ceramics</strong>, <strong>and</strong> the sensitivity <strong>of</strong> processing<br />
variables is unknown. This study was designed to<br />
characterize the fracture <strong>behavior</strong> <strong>and</strong> fracture<br />
toughness <strong>of</strong> a glass veneer (GV), a <strong>leucite</strong>-<strong>based</strong><br />
ceramic, <strong>and</strong> two <strong>lithia</strong> <strong>disilicate</strong>-<strong>based</strong> <strong>ceramics</strong><br />
using fractographic principles. The objective <strong>of</strong> this<br />
study was to test the hypothesis that variation in<br />
strength is associated with the variation in fracture<br />
toughness for the same surface preparation.<br />
Materials <strong>and</strong> methods<br />
The ceramic materials (E1, E2, ES, <strong>and</strong> GV) <strong>and</strong><br />
firing procedures used for bar specimens<br />
Table 1 Firing temperatures ðTÞ <strong>and</strong> times ðtÞ for the four <strong>ceramics</strong>.<br />
Dental <strong>ceramics</strong> Starting T<br />
(8C)<br />
(25 £ 4 £ 1.2 mm) are summarized in Table 1. The<br />
GV specimens were fabricated using a metal mold<br />
<strong>and</strong> fired according to the manufacturer’s instructions<br />
(Table 1). The hot-pressed <strong>leucite</strong>-<strong>based</strong> core<br />
ceramic (E1) <strong>and</strong> the two hot-pressed <strong>lithia</strong> <strong>disilicate</strong>-<strong>based</strong><br />
core ceramic specimens (E2 <strong>and</strong> ES)<br />
were prepared using the lost-wax technique. 10<br />
After removal <strong>of</strong> the hot-pressed ceramic from<br />
the investment, the interaction layer was removed<br />
by grit blasting with 80 mm glass beads at a pressure<br />
<strong>of</strong> 2 bar (30 psi). The bar specimens were cleaned in<br />
1% hydr<strong>of</strong>luoric acid (HF) for 30 min, grit blasted<br />
with 100 mm Al2O3 at a pressure <strong>of</strong> 2 bar, <strong>and</strong><br />
polished through 1200 grit SiC metallographic paper<br />
to a thickness <strong>of</strong> 1.2 mm. All specimens were<br />
finished with 1 mm polishing alumina (Mark V<br />
Laboratory, East Granby, CT, USA) to the final<br />
dimensions (25 £ 4 £ 1.2 mm). They were ultrasonically<br />
cleaned in distilled water <strong>and</strong> steam cleaned<br />
using distilled water. Specimens were examined for<br />
flaws using light microscopy at 30 £ (microscope<br />
model SCW30L, Fisher Scientific, Thail<strong>and</strong>). Specimens<br />
with any obvious large flaws would be<br />
eliminated, if detected. However, no major flaws<br />
were detected. The specimens were stored for 48 h<br />
in distilled water at 37 8C <strong>and</strong> then subjected to<br />
four-point flexure loading (applied along rollers<br />
at 1/3 <strong>and</strong> 2/3 <strong>of</strong> the length <strong>of</strong> the bars) at<br />
Heating rate<br />
(8C/min)<br />
Firing T<br />
(8C)<br />
Holding t<br />
(min)<br />
Vacuum T on–<strong>of</strong>f<br />
(8C)<br />
E1—IPS Empress core a (<strong>leucite</strong>-<strong>based</strong> ceramic) 700 60 1180 20 500–1180<br />
E2—IPS Empress2 core a (<strong>lithia</strong> <strong>disilicate</strong>-<strong>based</strong> ceramic) 700 60 920 20 500–920<br />
ES—Experimental core a (<strong>lithia</strong> <strong>disilicate</strong>-<strong>based</strong> ceramic) 700 60 910 15 500–910<br />
GV—IPS Empress2 body a (amorphous glass) 403 60 800 2 450–799<br />
a Ivoclar AG, Schaan, Liechtenstein.<br />
ARTICLE IN PRESS<br />
A. Della Bona et al.
a cross-head speed <strong>of</strong> 0.5 mm/min in a universal<br />
testing machine (Model 1125, Instron Corp., Canton,<br />
MA, USA) while immersed in distilled water.<br />
Note that any local residual stresses induced during<br />
preparation, i.e., around any flaws, were relieved<br />
by the storage under water because <strong>of</strong> slow crack<br />
growth in a conducive environment. An Isotemp<br />
Immersion Circulator (Model 730, Fisher Scientific,<br />
Pittsburgh, PA, USA), which was connected to the<br />
testing chamber, was used to maintain the water at<br />
37 8C. 11 Failure loads were recorded <strong>and</strong> the<br />
flexural strength values were calculated using the<br />
following equation:<br />
s ¼ PL=wt 2<br />
ð2Þ<br />
where P is the applied load at failure, L is the<br />
length <strong>of</strong> the outer (total) span, w is the width <strong>of</strong><br />
the specimen, <strong>and</strong> t is the thickness <strong>of</strong> the<br />
specimen. 11,12<br />
<strong>Fracture</strong> surfaces were examined using optical<br />
microscopy (OM) <strong>and</strong> scanning electron microscopy<br />
(SEM) to determine the mode <strong>of</strong> failure <strong>based</strong> on the<br />
fracture origin <strong>and</strong> fractographic principles.<br />
3,13 – 15<br />
In preparation for SEM (JSM 6400, Jeol Ltd, Tokyo,<br />
Japan) examination, the fracture surfaces were<br />
sputter-coated with gold–palladium for 3 min in a<br />
Hummer II Sputter Coater (21020, Technics Inc.,<br />
Alex<strong>and</strong>ria, VA, USA) at a current <strong>of</strong> 10 mA <strong>and</strong> a<br />
vacuum <strong>of</strong> 130 mTorr.<br />
The critical flaws were located <strong>and</strong> their size<br />
ðcÞ was determined using fractographic principles.<br />
The flaw size calculation ½c ¼ðabÞ 1=2 Š is the same as<br />
that used for an equivalent semicircular surface<br />
crack <strong>and</strong> corner crack. In the case <strong>of</strong> a corner<br />
crack, ‘c’ corresponds to the distance from the<br />
crack corner to the limit <strong>of</strong> the critical flaw-mirror<br />
region (Fig. 1).<br />
The mean crack size <strong>and</strong> strength values were<br />
used to calculate the fracture toughness ðK ICÞ via<br />
Eq. (1). The geometrical factor ðYÞ was calculated<br />
<strong>based</strong> on R<strong>and</strong>all’s 7 interpretation <strong>of</strong> Irwin’s 16<br />
work:<br />
Y ¼½0:515Q 1=2 Š 21<br />
ð3Þ<br />
Q ranged in value from 1.00 for long, shallow<br />
cracks ðY ¼ 1:94Þ to 2.46 for semicircular cracks<br />
ðY ¼ 1:24Þ: For a corner crack, the factor Y can be<br />
approximated by<br />
Y ¼ 1:12 2 2=p 1=2<br />
ð4Þ<br />
where 1.12 2 represents the surface flaw corrections<br />
<strong>and</strong> 2=p 1=2 represents the correction for a pennyshaped<br />
embedded crack, i.e. Y ¼ 1:4. 17<br />
Extra samples <strong>of</strong> each ceramic were fabricated<br />
<strong>and</strong> ground to a powder, mixed with an adhesive<br />
ARTICLE IN PRESS<br />
<strong>Fracture</strong> Behavior <strong>of</strong> Ceramics 3<br />
(collodian–amyl acetate in a ratio <strong>of</strong> 1:7), <strong>and</strong><br />
placed on a glass slide sample area. To identify the<br />
ceramic crystal phases, X-ray diffraction (XRD) was<br />
performed using a 3720 Phillips room temperature<br />
diffractometer (serial #1470, Phillips, Netherl<strong>and</strong>s)<br />
<strong>and</strong> PW1877 automated powder diffraction s<strong>of</strong>tware.<br />
A copper tube anode in a continuous scan<br />
from 3.01 to 89.978 (,3–908) with step size <strong>of</strong> 0.028<br />
every 0.4 s was used at a voltage <strong>of</strong> 40 kV, <strong>and</strong><br />
current <strong>of</strong> 20 nA. A slow scan from 10 to 408 was also<br />
used. The IPS Empress2 GV was analyzed for any<br />
crystal phase using a DRIFT (Diffuse Reflectance<br />
Infrared Fourier Transform, Spectra Tech Inc.,<br />
Shelton, CT, USA) analyzer with a Gemini Stage<br />
(Nicolet Magna 760, Nicolet Inc., Madison, WI, USA)<br />
<strong>and</strong> OMNIC 4.1b s<strong>of</strong>tware (Nicolet Inc., Madison,<br />
WI, USA). The following four powder samples were<br />
analyzed: (1) 0.5 g <strong>of</strong> KBr powder (Spectra Tech<br />
Inc., Shelton, CT, USA) for the background control;<br />
(2) 0.5 g <strong>of</strong> KBr powder mixed with 0.025 g <strong>of</strong><br />
unfired incisal GV powder; (3) 0.5 g <strong>of</strong> KBr powder<br />
mixed with 0.025 g <strong>of</strong> unfired dentin GV powder;<br />
<strong>and</strong> (4) 0.5 g <strong>of</strong> KBr powder mixed with 0.025 g <strong>of</strong><br />
fired dentin GV powder. Analysis was performed in<br />
64 scans for four wave number resolutions. The data<br />
were corrected for H2O <strong>and</strong> CO2 interferences <strong>and</strong><br />
results were recorded.<br />
Ceramic disks specimens <strong>of</strong> each material used in<br />
this part <strong>of</strong> the study (Table 1) were fabricated<br />
<strong>and</strong> polished through 1 mm alumina abrasive. The<br />
specimen thickness was measured using a caliper<br />
(Digimatic caliper, Mitutoyo Co., Kawasaki, Japan)<br />
<strong>and</strong> the weight was obtained using an analytical<br />
balance (Mettler H31, Mettler Instrument Corp.,<br />
Hightstown, NJ, USA). The density ðrÞ was obtained<br />
using the Helium Pycnometer (Accupyc 1330,<br />
Micromeritics Instrument Co., Norcross, GA, USA)<br />
after calculating the volume.<br />
The elastic modulus ðEÞ <strong>and</strong> Poisson’s ratio ðnÞ<br />
were determined by means <strong>of</strong> ultrasonic waves <strong>and</strong><br />
a computer program (ECALC <strong>and</strong> Sigview-F s<strong>of</strong>tware,<br />
Nuson Inc., Boalsburg, PA, USA) <strong>based</strong> on a<br />
set <strong>of</strong> equations that uses the time <strong>of</strong> flight,<br />
density, <strong>and</strong> thickness. Piezoelectric transducers<br />
(Ultran Laboratories Inc., Boalsburg, PA, USA) <strong>and</strong><br />
an ultrasonic pulse apparatus (Ultima 5100, Nuson<br />
Inc., Boalsburg, PA, USA) were used to determine<br />
the time <strong>of</strong> flight through the ceramic specimens.<br />
Longitudinal <strong>and</strong> shear (transverse) time <strong>of</strong> flight<br />
values were obtained <strong>and</strong> used to calculate n <strong>and</strong> E<br />
<strong>of</strong> the materials. 11 A hardness tester (Model MO<br />
Tukon Microhardness Tester, Wilson Instruments<br />
Inc., Binghampton, NY, USA) with a Vickers diamond<br />
was used to measure the hardness <strong>of</strong> these<br />
ceramic specimens. Each specimen was indented at<br />
four different locations under a load ðPÞ <strong>of</strong>
4<br />
9.8 N. The dimensions <strong>of</strong> the indentation diagonals<br />
were measured using an optical microscope with a<br />
filar eyepiece. The hardness ðHÞ values were<br />
calculated by<br />
H ¼½2P sinðu=2ÞŠ=a 2<br />
ð5Þ<br />
where P is the indentation load, u is the angle<br />
between opposite diamond faces (1368), <strong>and</strong> a is the<br />
mean diagonal length <strong>of</strong> the indentation.<br />
Flexural strength <strong>and</strong> K IC data were analyzed<br />
statistically using one-way ANOVA <strong>and</strong> Tukey’s HSD<br />
test. Weibull regression analysis was performed on<br />
the strength data as previously described 12 <strong>and</strong> as<br />
presented in a previous report. 11<br />
Results<br />
The mean values <strong>of</strong> density ðrÞ; elastic modulus ðEÞ;<br />
Poisson’s ratio ðnÞ; <strong>and</strong> Vickers hardness ðHÞ <strong>of</strong> the<br />
<strong>ceramics</strong> used in this study are summarized in<br />
Table 2.<br />
XRD analyses showed that high-exp<strong>and</strong>ing mineral,<br />
<strong>leucite</strong> (K2O·Al2O3·4SiO2), is the crystal phase<br />
in the IPS Empress core ceramic (E1), <strong>and</strong> the<br />
lithium <strong>disilicate</strong> (Li2O·2SiO2) is the crystal phase in<br />
the IPS Empress 2 (E2) <strong>and</strong> Experimental (ES) core<br />
<strong>ceramics</strong>. These crystal phases are shown in Fig. 2.<br />
The length <strong>of</strong> the elongated Li2Si2O5 crystals ranged<br />
from 0.5 to 4 mm for E2 <strong>and</strong> from 0.5 to 2 mm for ES.<br />
XRD analysis <strong>of</strong> the IPS Empress2 GV produced a<br />
typical amorphous glass plot. The absence <strong>of</strong> any<br />
crystal phase was confirmed by FTIR analysis.<br />
Representative photomicrographs <strong>of</strong> the <strong>ceramics</strong><br />
microstructure are presented in Fig. 2. As<br />
expected, there is a positive correlation between<br />
the elastic modulus ðEÞ; hardness ðHÞ; flexure<br />
strength ðsÞ; <strong>and</strong> fracture toughness ðK ICÞ for the<br />
four <strong>ceramics</strong> studied (E1, E2, ES, <strong>and</strong> GV).<br />
One-way ANOVA <strong>and</strong> Tukey’s test subsets<br />
revealed significant statistical differences for the<br />
mean s <strong>and</strong> K IC values between E1 <strong>and</strong> GV <strong>ceramics</strong><br />
ðp , 0:05Þ: The two <strong>lithia</strong> <strong>disilicate</strong>-<strong>based</strong> <strong>ceramics</strong><br />
(E2 <strong>and</strong> ES) showed greater mean s <strong>and</strong> K IC values<br />
Table 2 Mean values <strong>of</strong> density ðrÞ; elastic modulus ðEÞ;<br />
Poisson’s ratio ðnÞ; <strong>and</strong> Vickers hardness ðHÞ <strong>of</strong> Empress<br />
<strong>ceramics</strong>.<br />
Material properties E1 E2 ES GV<br />
Density (r, g/cm 3 ) 2.47 2.51 2.56 2.53<br />
Elastic modulus (E, GPa) 86 96 96 65<br />
Poisson’s ratio ðnÞ 0.27 0.26 0.24 0.23<br />
Vickers hardness (H, GPa) 5.9 6.3 6.3 5.4<br />
ARTICLE IN PRESS<br />
compared with the <strong>leucite</strong>-<strong>based</strong> ceramic (E1) <strong>and</strong><br />
the GV (Table 3) <strong>and</strong> the differences in mean values<br />
were statistically significant ðp # 0:05Þ:<br />
All fractures initiated along the tensile surfaces<br />
between the inner load points. Corner flaws (CF),<br />
either cracks or voids, were identified as the<br />
fracture origin in 20–30% <strong>of</strong> the specimens (Fig. 3,<br />
Table 3).<br />
Discussion<br />
A. Della Bona et al.<br />
Structural failure associated with an applied load<br />
occurs when the induced stress is greater than the<br />
strength <strong>of</strong> the material. The failure location is<br />
dependent on the size <strong>of</strong> the initiating crack <strong>and</strong> the<br />
fracture toughness. 9 Usually, fracture <strong>of</strong> the ceramic<br />
originates from the most severe flaw. The<br />
large number <strong>of</strong> pre-existing ceramic cracks <strong>of</strong><br />
differing sizes, coupled with a low fracture toughness,<br />
limits the strength <strong>of</strong> <strong>ceramics</strong> <strong>and</strong> causes a<br />
large variability in strength <strong>and</strong> the time dependence<br />
<strong>of</strong> strength. The size <strong>and</strong> spatial distribution<br />
<strong>of</strong> flaws justify the necessity <strong>of</strong> a statistical<br />
approach to failure analysis 18 to determine the<br />
reliability <strong>of</strong> <strong>ceramics</strong>. 11,19<br />
Investigations <strong>of</strong> clinically failed all-ceramic<br />
restorations have shown that the fracture origin is<br />
typically located at the inner tensile surface.<br />
20 – 22<br />
However, for strength tests to yield relevant<br />
service information, the test <strong>and</strong> service environments<br />
must be similar <strong>and</strong> the strength-controlling<br />
flaw population must approximate that responsible<br />
for failure in clinical service. 19 The distribution <strong>of</strong><br />
flexural strengths under wet environmental conditions<br />
is a potential indication <strong>of</strong> ceramic performance.<br />
The greater mean s <strong>and</strong> K IC values <strong>of</strong> E2<br />
<strong>and</strong> ES core <strong>ceramics</strong> are indicative <strong>of</strong> potentially<br />
improved structural performance. However, resistance<br />
to stress corrosion processes <strong>and</strong> a small range<br />
<strong>of</strong> strength values are also factors in structural<br />
reliability. Thus, a combination <strong>of</strong> good fracture<br />
toughness, excellent resistance to stress corrosion,<br />
<strong>and</strong> resistance to loading are required for structural<br />
reliability. If one <strong>of</strong> these elements is missing, then<br />
there may be a false sense <strong>of</strong> security in designing<br />
ceramic prostheses made from these materials. For<br />
example, in the case <strong>of</strong> the Group GV, the Weibull<br />
modulus, m; is twice as large as that for each <strong>of</strong> the<br />
other groups <strong>and</strong> the flaw size is smaller than the<br />
flaw sizes <strong>of</strong> the other groups. This appears to be a<br />
positive result. However, because <strong>of</strong> the low value<br />
<strong>of</strong> fracture toughness, the strength is much less<br />
than that <strong>of</strong> the other groups <strong>and</strong> this, most likely,<br />
would not be a reliable material.
Under certain service <strong>and</strong>/or environmental<br />
conditions, stable crack extension or slow crack<br />
growth can occur at stress intensities that are less<br />
than the critical value, K C: In this study all fracture<br />
surfaces were produced from specimens immersed<br />
in 37 8C distilled water. The loading rate used<br />
limited, but did not eliminate, slow crack growth,<br />
when tested in water. 11 Thus, the strengths<br />
reported are less, but more conservative than<br />
those expected for tests conducted in air. Yet<br />
the calculated fracture toughness does not depend<br />
on the crack growth since the flaw size was<br />
measured. The strength values are correlated to<br />
the flaw size to calculate the value <strong>of</strong> toughness.<br />
ARTICLE IN PRESS<br />
<strong>Fracture</strong> Behavior <strong>of</strong> Ceramics 5<br />
Figure 2 SEM micrographs <strong>of</strong> lightly etched <strong>ceramics</strong>. (A) IPS Empress 2 GV revealing light <strong>and</strong> dark glass phases<br />
containing very similar compositions. (B) XRD analysis showed the presence <strong>of</strong> <strong>leucite</strong> crystals ( p ) in a glassy phase <strong>of</strong><br />
IPS Empress core ceramic (E1). XRD analysis showed the presence <strong>of</strong> lithium <strong>disilicate</strong> crystals ( p ) in a glassy phase <strong>of</strong><br />
(C) IPS Empress 2 core ceramic (E2) <strong>and</strong> (D) Experimental <strong>lithia</strong> <strong>disilicate</strong>-<strong>based</strong> core ceramic (ES).<br />
Previous reports on the fracture toughness using the<br />
single edge notched beam (SENB) method performed<br />
at room conditions showed KIC values<br />
comparable to those presented in this study.<br />
23 – 25<br />
<strong>Fracture</strong> surface analysis is well established as a<br />
means <strong>of</strong> failure analysis in the field <strong>of</strong> glasses <strong>and</strong><br />
<strong>ceramics</strong>. 3 It has been recognized as a powerful<br />
analytical tool in dentistry. 20,22 <strong>Fracture</strong> in glass<br />
<strong>and</strong> <strong>ceramics</strong> occurs when pre-existing cracks<br />
propagate under excessive tensile stresses.<br />
These cracks can be produced by mechanical<br />
means, e.g. grinding or polishing, by processing,<br />
or by intrinsic defects, e.g. imperfections in the<br />
structure. Fractographic analysis identified the type<br />
Table 3 Mean values <strong>and</strong> st<strong>and</strong>ard deviation (SD) <strong>of</strong> flexural strength ðs fÞ; critical crack size ðcÞ; fracture toughness ðK ICÞ;<br />
characteristic strength ðs 0Þ; Weibull modulus ðmÞ; <strong>and</strong> fracture origins for the four ceramic groups.<br />
Groups s f (SD) (MPa) s 0 (MPa) m c (SD) (mm) K IC (SD) (MPa m 1/2 ) <strong>Fracture</strong> origin a (%)<br />
E1 85 (15) B b<br />
91.3 5 110 (62) 1.3 (0.3) B b<br />
SF (70); CF (30)<br />
E2 215 (40) A 231 5 140 (56) 3.4 (0.6) A SF (70); CF (30)<br />
ES 239 (36) A 252 7 110 (25) 3.1 (0.4) A SF (80); CF (20)<br />
GV 63.8 (5.8) C 65.7 14 95 (35) 0.8 (0.1) C SF (80); CF (20)<br />
a SF, surface flaw (void or crack); CF, corner flaw (void or crack).<br />
b The values in each column with same letters do not differ significantly ðp , 0:05Þ:
6<br />
Figure 3 SEM micrographs <strong>of</strong> ceramic fracture surfaces showing representative critical flaws outlined by white arrows.<br />
(A) <strong>Fracture</strong> surface <strong>of</strong> E1; line from flaw corner, c ¼ 84 mm (500 £ ). (B) <strong>Fracture</strong> surface <strong>of</strong> E2; measured line<br />
represents the semiminor axis, a ¼ 44 mm (500 £ ). (C) <strong>Fracture</strong> surface <strong>of</strong> ES; measured line represents the semiminor<br />
axis, a ¼ 35 mm (600 £ ). (D) <strong>Fracture</strong> surface <strong>of</strong> GV; note the tailed fracture markings (top right) pointing toward the<br />
crack origin; measured line represents the semiminor axis, a ¼ 55 mm (500 £ ).<br />
<strong>of</strong> origins <strong>and</strong> confirmed the presence <strong>of</strong> characteristic<br />
markings <strong>of</strong> the fracture process (Fig. 3).<br />
Ceramic specimens tested in bending are very<br />
sensitive to edge or surface machining damage. 19<br />
Fractographic analysis has shown that all failures<br />
started from either a surface (Fig. 3B–D) or a corner<br />
flaw (Fig. 3A) located along the tensile surface <strong>of</strong><br />
the specimens. These results are consistent with a<br />
previous report, which suggested that surface<br />
failures started only at the tensile side <strong>of</strong> specimens<br />
tested in four-point bending. 26 However, the<br />
number <strong>of</strong> fractures originating from corner flaws<br />
(20–30%) in this study suggests that careful manual<br />
chamfer or rounding <strong>of</strong> specimen edges may<br />
improve the reproducibility <strong>of</strong> test results produced<br />
through ISO st<strong>and</strong>ard 6872 for dental <strong>ceramics</strong>.<br />
Although machine rounding <strong>of</strong> edges can produce<br />
even more defects, careful manual rounding <strong>of</strong> the<br />
edges is preferred, by some investigators, to<br />
machining 908 corners.<br />
The Weibull modulus ðmÞ is a measure <strong>of</strong> the<br />
distribution <strong>of</strong> critical flaws. As the Weibull moduli<br />
are similar for three <strong>of</strong> the four <strong>ceramics</strong>, <strong>and</strong> the<br />
crack sizes ðcÞ are comparable (Table 3),<br />
ARTICLE IN PRESS<br />
A. Della Bona et al.<br />
the differences in mean strength cannot be<br />
explained by a difference in crack sizes. In fact,<br />
E2 has the largest mean crack sizes, <strong>and</strong> yet, has<br />
one <strong>of</strong> the largest mean strength values. Since the<br />
fracture toughness is a constant (Eq. (1)), a large<br />
crack size would result in a low strength value for<br />
the same toughness. Thus, the differences in mean<br />
strength can only be explained by differences in<br />
fracture toughness that are related to processing<br />
<strong>and</strong> composition variables. The GV contains<br />
relatively few, if any, crystals <strong>and</strong> would be<br />
expected to have a toughness value the same as,<br />
or slightly greater than those <strong>of</strong> silicate glasses as<br />
shown in Table 3. The E1 core ceramic has crystals<br />
dispersed in a glassy matrix. However, the volume<br />
fraction <strong>of</strong> crystals is very small (Fig. 2) compared<br />
with those <strong>of</strong> E2 <strong>and</strong> ES <strong>ceramics</strong> <strong>and</strong> is expected to<br />
have a toughness value that lies between that <strong>of</strong> the<br />
GV <strong>and</strong> those <strong>of</strong> the E2 <strong>and</strong> ES <strong>ceramics</strong>. The fine<br />
dispersion <strong>of</strong> crystals in the E2 <strong>and</strong> ES <strong>ceramics</strong><br />
leads to the increased toughness values observed<br />
relative to either the GV or the E1 ceramic core<br />
material. The differences in the crystal sizes<br />
between E2 <strong>and</strong> ES <strong>ceramics</strong> are not great enough
within the sampling error to determine if these<br />
differences can affect the toughness values.<br />
However, the amount <strong>and</strong> sizes <strong>of</strong> crystals are<br />
enough to increase the magnitude <strong>of</strong> toughness to a<br />
greater level compared with GV <strong>and</strong> E1. Thus, the<br />
strength values are proportional to the toughness<br />
values as stated previously.<br />
Acknowledgements<br />
This paper is <strong>based</strong> on a dissertation submitted to<br />
the graduate faculty, University <strong>of</strong> Florida, in<br />
partial fulfillment <strong>of</strong> the requirements for the PhD<br />
degree.<br />
This study was partially supported by CNPq-Brazil,<br />
grant 300659/03-2, <strong>and</strong> NIH-NIDCR grant DE06672.<br />
The authors thank Dr C. Shen for performing the<br />
statistical analysis <strong>and</strong> Mr Robert B. Lee for his<br />
assistance in processing the <strong>ceramics</strong>. We also<br />
thank Ivoclar AG (Liechtenstein) for providing the<br />
ceramic materials used in this study.<br />
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