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ISRN Ceramics

Volume 2012 (2012), Article ID 741042, 9 pages

http://dx.doi.org/10.5402/2012/741042

## Contact Deformation of Alumina

Central Glass and Ceramic Research Institute, CSIR, 196 Raja S.C. Mullick Road, Kolkata 700032, India

Received 28 September 2012; Accepted 15 October 2012

Academic Editors: K. L. Bing, H. I. Hsiang, C.-F. Yang, and K. Zupan

Copyright © 2012 Manjima Bhattacharya and Anoop Kumar Mukhopadhyay. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

#### Abstract

The study of contact-induced deformations during hardness evaluation and the subsequent damage mechanisms of alumina under low loads deserves significant importance for its applications as wear-resistant inserts, biomedical implants, thin films, and armour plates, because the contact-induced brittle failure is an issue of major scientific concern that prevents their widespread commercial applications. However, the studies on hardness of dense, coarse grain alumina at ultralow load, for example, 1 N, are still lacking. Therefore, the present study was conducted on a dense (*~*95% of theoretical) coarse-grain (*~*20 *μ*m) alumina at a low peak load of 1 N with varying loading rates (10^{−3}–10^{0} N·s^{−1}) applied in depth sensitive indentation experiments. The results showed profuse presence of multiple micro-pop-in and pop-out events possibly linked to dislocation nucleations underneath the indenter. The critical resolved shear stress () was found to enhance with the increase in applied loading rates. The occurrences of the localized shear deformation band formation and microcracking in and around the indentation cavity were explained in terms of the correlation between the nanoscale plasticity events, the small magnitude of (), the maximum shear stress () developed just underneath the indenter, and the dislocation loop radius ().

#### 1. Introduction

Alumina is well established as one of the most important structural and engineering ceramics. It has good oxidation resistance, chemical stability, good electric insulation, relatively high hardness, high wear resistance, and low friction in many contact situations. Therefore it is used as wear-resistant inserts [1], biomedical implants [2], wear resist coatings [3], thin films [4], and armour plates [5]. All such high end engineering applications of alumina and/or its composites are basically controlled by contact-induced deformation mechanisms and damage initiation, as well as growth mechanisms at macro-, micro- and/or nanostructural length scale of the microstructure. This contact-induced brittle failure is an issue of major scientific and technical concerns which retards the rate of more widespread commercial applications of alumina ceramics. The most important surface mechanical property that defines the contact resistance of alumina is its hardness. Therefore, it is not surprising that hardness evaluation at various length scales consumes a significant amount of current research efforts in alumina [6–14]. Most of the commercially available alumina ceramics used for a variety of technical applications are coarse grained. They exhibit low to moderate hardness and, in addition, characteristically exhibit an R-curve behaviour which means that their crack growth resistance improves as the crack grows. In spite of the wealth of literature that exists on hardness of alumina measured at macro-, microscale [10–12], or nanoscale [13, 14] mostly for fine grain and/or submicrometer grain-sized alumina ceramics; however, the reports on hardness behaviour of dense coarse grained alumina ceramics are really rare [10]. It is important to recognize that depth sensitive indentation technique has emerged as a very effective technique to determine the surface mechanical properties of wide variety of materials [15–19].

Interestingly, alumina generally exhibits localized plastic deformation even under micronewton order of load [20]. The effect of these deformations are revealed by the occurrence of *“multiple micro-pop-in”* and *“multiple micro-pop-out”* events in the load-depth plots, followed by the formation of shear deformation bands and localized microcracking in and around the indentation cavity [21–37] and the formation of dislocation loops in the alumina sample. The detailed mechanisms of pop-in events which occur during indentation in ceramics are far from being well understood and may be strongly sensitive to the plane bearing the nanoindentation, nanoindenter tip radius, temperature and so forth, while the microscale hardness may [38–41] or may not be [42] sensitive to strain and loading rate variation.

Recently, significant effect of loading rate on hardness of glass [21–24] and alumina [25, 26, 43, 44] was reported. The occurrence of the pop-in behaviour was also reported for glass [21–24], polycrystalline alumina [25, 26, 43, 44], bulk metallic glass [27–29], sapphire [30], GaN [31], and ZnO [32]. The occurrence of pop-in has often been associated with shear localization [21–37]. There are though many contradictory viewpoints about their genesis in a wide variety of materials [37, 45–49], an unequivocal picture is yet to emerge. Therefore, the objective of the present work was to study in detail the effects of sharp contact, for example, a Berkovich indentation, induced deformation of a high density (~95% of theoretical) coarse grain (~20 *μ*m) alumina with varying loading rates of (10^{−3}–10^{0} N·s^{−1}) in the present indentation experiment at a very low peak load of 1 N. The idea behind choosing the low peak load of 1 N was to be able to control the extent of damage that such a sharp contact event would create. The effects were explained in terms of shear localization, as well as the formation of dislocation loops under the indenter.

#### 2. Materials and Methods

Since experimental details have been reported elsewhere [21–26, 43, 44], a brief description is mentioned here. Alumina discs of ~10 mm in diameter and ~3 mm in thickness were prepared by pressureless sintering in air at 1600°C. Density of the sintered alumina discs was measured by Archimedes’s principle. The polished alumina discs having surface roughness () of 0.01 *μ*m were thermally etched for 1 h in air at a temperature of 1700°C. Photomicrographs of the thermally etched alumina discs were taken by using a field emission scanning electron microscope (FE-SEM, Supra VP35, Carl Zeiss, Germany). These photomicrographs were used to measure the average grain size of the pressureless sintered alumina by using an image analyzer (Q500MC, Leica, UK).

A load controlled indentation technique was used with a commercial nanoindentation machine (Fischerscope H100-XYp; Fischer, Switzerland) to evaluate hardness and Young’s modulus of the alumina samples. A 5 × 5 array matrix was utilized for this purpose. Four random locations were chosen for experiments. The machine had depth sensing resolution of 1 nm. The load sensing resolution of the machine was 0.2 *μ*N. The indentation experiments were conducted with a Berkovich indenter attached to the machine. The indenter had a tip radius of ~150 nm and a semiapex angle of 65.3°. The area function of the indenter tip was evaluated prior to each experiment. The dedicated software available in the control system of the machine corrected the experimentally obtained load () versus depth of penetration () data for tip blunting effect. Following the DIN 50359-1 standard, the machine was finally calibrated with nanoindentation-based independent evaluation of hardness, (4.14 GPa) and Young’s modulus, (84.6 GPa) values of a reference BK7 glass block (Schott, Germany). The standard reference glass block was provided by the supplier of the machine. The calibration was repeated before each experiment to make sure that the data generated remains reproducible. Next, the Oliver-Pharr model [37] was used to measure the hardness and Young’s modulus data of the alumina samples from the experimentally measured load-depth (-) data plots. No particular bias was associated with the location selection for the positions of the nanoindentation arrays. Thus, at least 100 individual measurements of hardness values were used for each reported average data. In the present experiments, peak load of 1 N was used. Further, both the loading and the unloading times were varied from 10^{0} to 10^{3} seconds to obtain the variation of loading rates in the range of 10^{−3} to 10^{0} N·s^{−1}. Thus, the loading rate was calculated by dividing the peak load by the time to reach the peak load. For instance, a loading time of 1 second to reach a peak load of 1 N gives the loading rate of 10^{0} N·s^{−1}. The error bars represent ±1 standard deviation of the data for all experimental data reported in this work. Field emission scanning electron microscope (FE-SEM, Supra VP35, Carl Zeiss, Germany) as mentioned earlier was also used to observe the microstructure and the indents in the present alumina samples.

#### 3. Results and Discussions

FE-SEM photomicrograph (Figure 1) reveals the surface microstructure of the alumina having a relative density of 95% and grain size of 20 *μ*m. The indentation experiments were conducted on this alumina sample at thirteen different loading rates in the range of 10^{−3}–10^{0} N·s^{−1} at a peak load of 1 N. The loading part of the load-depth (-) plots at thirteen different loading rates corresponding to is shown in Figure 2(a). Exploded views of 4 selected typical load versus depth plots from Figure 2(a) are shown in gradual exaggerations in the subsequent Figures 2(b)–2(d). The - data plots revealed the presence of large number of serrations in the load-depth plots, Figure 2(b). These serrations were found to vary with the loading rates, Figures 2(b)–2(d). At lower loading rates, a large number of serrations occurred, while at higher loading rates, a much lesser number of serrations occurred, Figures 2(c) and 2(d). Similar phenomenon was observed during the unloading part of the load-depth plots, Figures 3(a), 3(b), 3(c), and 3(d).

The serrations implied the occurrences of nanoscale localized plastic deformation signatures expressed in terms of micro-pop-in and micro-pop-out events in the loading and unloading parts. Similar observations were also reported for glass [21–24], polycrystalline alumina [25, 26, 43, 44], bulk metallic glasses [27–29], sapphire [30], GaN [31], and ZnO [32].

The load at which the nanoscale plasticity event had initiated is referred to as the critical load . The high resolution FE-SEM photomicrograph (Figures 4(a) and 4(b)) showed shear-induced localized microcracking in the vicinity of the indent and microshear band formation inside the indentation cavity. The genesis of such nanoscale plasticity events has been correlated [35, 36] to shear burst and shear localization which initiate at a critical load as mentioned above.

However, microcrack formation requires a low value of the critical resolved shear stress . Based on the measured Young’s modulus for the present alumina ( GPa for 1 N) [44], the values of shear modulus were estimated from assuming as 0.21 [37]. The shear modulus () data were not sensitive to the variations in loading rate as expected, Figure 5. Now, following the method suggested in [46] and using the present experimental data, the corresponding critical resolved shear stress values were evaluated assuming the magnitude of the Burger’s vector as ~0.5 nm [46].

It is interesting to note that the critical resolved shear stress showed a power law dependence on the loading rates as shown in Figure 6. The values of the estimated were found to be very low (0.6–1.85 GPa for 1 N). Thus, from the aforesaid values, the average critical resolved shear stress value was estimated as ~1.23 GPa for the applied load of 1 N. This value (~1.23 GPa for 1 N) for the present coarse grain alumina was lower than those, for example, ~2-3 GPa and ~2.18 GPa, reported, respectively, for single crystal sapphire [46] and nanograined *α*-alumina [35]. Furthermore, was which compared favourably with reported for sapphire [46]. Such a small magnitude of suggests a high possibility of localized microcracking around the indents, because of the high stresses generated at the small contact region, particularly at the vertices of the indents due to the steep change in slopes of the supporting contact area. The high resolution FE-SEM photomicrographs (Figures 4(a) and 4(b)) indeed provide necessary evidence in support of such a picture.

Now we would like to discuss the possibility of dislocation nucleation that might have had led to the initiation of nanoscale plasticity events in the coarse grained alumina. Thus, following the method suggested by Gouldstone et al. [47], the possible range of dislocation loop radius data was estimated as a function of the loading rates, considering the typical magnitude of Burger’s vector ~0.5 nm [46] as mentioned before.

Assuming that the typical maximum effective thickness within which the dislocation loops generated underneath the indenter will be typically ~one-tenth of the grain size, the range of dislocation loop radius data was estimated as ~85–2.2 nm corresponding to the range (e.g., 10^{−3}–10^{0} N·s^{−1}) of loading rates. The prediction of the data required the use of critical load and critical depth data determined from the experimentally measured load depth plots, Figures 2(a)–2(d) obtained during the loading cycles.

It may be noted that was much greater than [35, 36]. Furthermore, the value of nm compared favourably with the value of nm reported for nanograined *α*-alumina [35]. The variation of exhibited a power law dependence on the loading rate with a negative exponent, Figure 6.

At lower loading rates the indenter spent longer time in contact with the alumina microstructure. Hence it was expected to face more microstructural obstruction during penetration process. However, at higher loading rates, it spent comparatively much lower amount of time, for example, 1 sec, in contact with the alumina microstructure. Therefore, it was highly likely that the amount of microstructural obstruction faced by the penetrating indenter would be much lesser in this case. Thus, the data presented in Figure 6 would suggest that, at higher loading rates, the indenter penetrated for relatively lesser amounts of time and hence it possibly faced lesser obstructions.

As the amount of obstruction faced was less, the radius of the dislocation loop was very small, for example, ~2.2 nm at higher loading rate. Then it would be logical to argue that the total number of dislocations nucleated per unit volume of the coarse grain alumina at higher loading rates would be much more than those nucleated at lower loading rates, where the dislocation loop radii were predicted to be relatively larger, for example, ~85 nm.

The more the number of such nanoscale plasticity events would occur, the more would be the amount of strain in the microstructure. Therefore, it was not surprising that the hardness of the present alumina increased by about 6.64% (Figure 7) as the loading rate was increased from 10^{−3} to 10^{0} N·s^{−1}.

In this context, the maximum shear stress developed underneath the indenter was calculated [33, 34] and the data are incorporated in the same plot (Figure 7) as a function of loading rate. It was interesting to note that the maximum shear stress showed an empirical power law dependence with a positive exponent on the loading rate. Furthermore, it might be mentioned that the estimated average of the maximum shear stress ( GPa) active at depth of about 0.35 times the static contact radius was much greater than the theoretical shear strength (e.g., ~3 GPa) of alumina [10] and hence shear-induced deformation and/or fracture was expected (Figures 4(a) and 4(b)). Other researchers also reported ( GPa) for polycrystalline *α*-alumina [35, 36] located at the depths of 0.41 to 0.5 times the static contact radius .

Furthermore, the similar nature of power law dependencies of the maximum shear stress developed underneath the indenter and hardness on the loading rate with positive exponents suggested that there was a relationship between the increase in hardness and . This conjecture is indeed strongly supported by the data presented in Figure 8 which demonstrate that the rate of change in hardness of the alumina with loading rate was linearly dependent on the rate of change of the maximum shear stress with loading rate.

In other words, the higher magnitude of maximum shear stress at higher loading rate could have had easily played a pivotal role in nucleating more number of nanoscale plasticity events (because the dislocation loop radii were low) and thereby more localized strain accumulation in the microstructure of the alumina. The apparent small increase of about 6.64% in hardness may be the result of such a microstructural localized strain accumulation process. The characteristic lower magnitude of the critical resolved shear stress of course had aided some release of stress around the indent cavity through formation of highly localized microcracks.

Such a picture is further supported by the fact that both the brittleness index (BI) calculated [50] and the characteristic contact deformation resistance parameter defined for the first time in the present work as increased with the loading rate, following empirical power law dependencies with positive exponents, Figure 9. In this context it should be mentioned that the fracture toughness for the present alumina sample was measured by the conventional indentation fracture technique [51] to be ~3.28 ± 0.65 MPa·m^{0.5}. This data was used for calculating the brittleness index following [50]. Thus, the data presented in Figure 9 implied that the higher the contact deformation resistance of the present alumina, the more prone it became to contact-induced fracture as expected for characteristically brittle solids.

Although large number of nanoscale plasticity events could have occurred at higher loading rates as discussed above, it should be kept in mind that here the contact time between the indenter and the alumina sample was really very small. As a result, at higher loading rates, only the overall average elastoplastic and plastic deformation processes might have had come into play. In such a scenario, the simultaneous operation of multiple nanoscale plasticity events, for example, large number of dislocation nucleations due to high shear stress active at the vicinity of the tip of the indenter, could have had forced a homogenization of the plastic deformation response of the present alumina ceramics. This picture is supported by the fact that, on a comparative scale, a much lower number of serrations could be observed in the experimentally obtained load versus depth of penetration plots at higher loading rates (Figure 2).

On the other hand, at lower loading rates, there was comparatively longer interaction time, for example, up to 1000 sec, available during the indentation process. As a result, the action of the first, the immediate next one, and all such consequent nanoscale plasticity events might have had come into play nearly sequentially one after another. It is proposed that due to this sequential discrete fashion action of the multiple nanoscale plasticity events the multiple serrations appeared one after another in the - plots (Figure 2) recorded for the present alumina ceramic.

#### 4. Conclusions

We presented an experimental observation of a high density (95% of theoretical) coarse grain (~20 *μ*m) alumina, undergoing indentation at an ultralow peak load of 1 N. The hardness of the material against the initiation of nanoscale plasticity events can enhance with the loading rates following a power law dependence with a positive exponent. This enhancement is explained by the increase in maximum shear stress developed under the indenter with the loading rates. The apparent increase in hardness of the alumina was well supported by the decrease in the dislocation loop radius with the loading rates, creating, thereby, more number of dislocation nucleations at higher loading rates. Also, we found that the brittleness index of the coarse grain alumina can register an apparent increase with the loading rates and, hence, we can define a new parameter called contact deformation resistance () that also increases with the loading rates.

#### Acknowledgments

The authors are grateful to the Director of CSIR-Central Glass and Ceramic Research Institute (CGCRI), Kolkata, for his kind permission to publish this paper. In addition, the authors appreciate the infrastructural supports received from all colleagues and particularly those received from the colleagues of the Mechanical Property Evaluation Section, NOCCD. Finally, the authors gratefully acknowledge the financial supports received from CSIR (Project no. NWP 0027, NWP 0029).

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