Mechanical characterization of PM aluminum composites by small punch test

ABSTRACT

In this work Small Punch Test (SPT) was applied to study the mechanical behavior of ultrafine-grained Al-Al₂O₃metal matrix composites (MMCs) fabricated in situ via powder metallurgy route (HITEMAL®). Such MMCs show attractive mechanical properties, enhanced creep performance and increased thermal stability at elevated temperatures, not normally associated with service of conventional Al alloys, even after prolonged high temperature exposure. MMCs fabricated from two powders of different particle size (d50 = 8.9 and 1.2µm) were evaluated in the present work.

SPT was performed at room temperature using disc-shaped specimens of 10 mm in diameter. The effect of the different disc thickness (0.4, 0.5 and 0.6 mm) on the load vs. displacement function was evaluated. The displacements monitored from top and bottom sites of the specimen varied during the course of the test. The discs deformed throughout the test by two plastic stages, typical for ductile materials. The relation between load-displacement and stress–strain tensile curves for both composites was analyzed. A drastic change of mechanical behavior between the green compact of cold pressed material and the hot forged material was detected.

New methods of determination of a characteristic load PY, which represents a transition from elastic to plastic bending regime were presented and discussed. A relationship between PY and corresponding yield stress was studied for each composite material by a calculation of their respective correlation parameters.

Keywords
Small punch test; powder metallurgy; yield strength; aluminum; composite; correlation parameter

1. INTRODUCTION

The HITEMAL® [¹,²] are Al-Al₂O₃ metal matrix composite (MMC) materials fabricated through powder metallurgy (PM) consolidation of fine atomized Al powder with mean particle size of 1-10 µm. The nanoscale Al₂O₃ forms in situ and stems from native amorphous (am)- Al₂O₃ layers on as-atomized feedstock Al powders. One of the PM processes comprises consolidation through the hot quasi-isostatic forging (QIF) of cold compacted powders. The resulting microstructure of QIFed HITEMAL consists of continual special nano-thick am-Al₂O₃ network embedded in ultra-fine grained Al matrix. QIFed HITEMAL shows high strengths at elevated temperatures not normally associated with use of conventional Al alloys and superior structural stability after prolonged exposures up to 400 °C, which predetermines these materials for a potential use especially in application at elevated temperatures where excellent creep resistance is required. The spreading of native oxide skin coming from elementary aluminum particles play a key role in the reinforce mechanism of these composites [²]. Such nature and spreading characteristics of the amorphous and crystalline oxide reinforce nanoparticles are strongly dependent of the raw powders and the PM processes [¹].

SPT has been applied since 80 decade to study the embrittlement of structural components in the nuclear plants due to the aging processes mainly by radiation [³]. For a purpose of sampling from a component under service a small amount of testing material from components surface was non-destructively extracted. The mechanical characteristics are then determined by penetration tests realized on small disks. Disks of 10 or 3mm in diameter were employed with respective thicknesses of 0.500 and 0.200-0.250mm. SPT provides the mechanical behavior via a load (P) vs. displacement (δ) plot. The punch plot is obtained from the controlled indentation of a hemispherical punch (or ball) in the center of the disk specimen. Such response is representative of the mechanical strength and deformation behavior. The potential of this technique lies on the fact that the big reduction of volume of material for specimen, which allows a high selectivity of sampling, contrary to the traditional techniques (tensile, fracture toughness or creep for example) that need large volume of material. This selectivity improves the sampling efficiency in case of limited amount of laboratory materials. The disadvantage of SPT is the lack of a direct way to obtain traditional mechanical properties from this novel technique. That is, due to a complex stress field along the test where the disk is subjected to multiple combination of loading modes, including indentation, elastic and plastic bending, and membrane stretching at different level of deformation [⁴]. The literature has attempted model by numerical methods in order to reproduce the elastoplastic processes in order to identify which parameters controls the deformation in different stages along the test [⁴, ⁵, ⁶].

SPT has been applied in many engineering materials including metallic alloys and composites [⁵, ⁶, ⁷] to correlate the SPT results with the traditional mechanical properties like tensile, fracture or creep. For that purpose some semiempirical correlations between SPT parameters extracted from load-displacement curve and tensile properties like yield strength, tensile strength and elongation are often reported [⁴, ⁷, ³]. Under this approach, the characteristic load P_Y that represents the end of first regime (elastic bending) of SPT has been selected to be related with yield strength. This framework started by Mao and Takahashi [⁸] has been continued in recent studies [⁵,⁷] until these times. There are several definitions of P_Y and its representativeness for the beginning of plasticity is still under debate. By the introduction of a correlation factor α a linear relation as σ_YS proportional to α P_Y/t² has been proposed; where t is the initial thickness of SPT specimen.

The present work is focused on clarifying the relationship between the yield strength and the characteristic load P_Y in two HITEMAL compositions fabricated of two powders of 1.2 and 8.9 µm mean diameter. The methodologies to evaluate the characteristic load P_Y are discussed. Also, the differences among experimental methods to define the central displacement measurement are pointed out.

2. MATERIALS AND METHODS

Two different types of commercially available gas-atomized Al powders (Al >99.8wt%) with d₅₀ = 1.2 and 8.9 µm were used for this study. Loose powders were cold pressed by cold isostatic pressing (CIP) at 200 MPa. The forging blanks with diameter of Ø86 mm and height of 75 mm were machined from CIP green compacts. The forging blanks were subjected to vacuum degassing at 420 °C for 12 h at 5∙10^-2 Pa prior to forging. Degassed forging blanks were heated in air to the forging temperature of 420 °C and held at that temperature for 60 min. QIF compaction with a limited amount of induced deformation was performed using a Lasco SPR 1000 screw press with an impact energy of 57 kJ and a maximal initial strain rate of 7.3 s^-1. The forging die was preheated to 110 °C. The die walls were lubricated with a graphite water solution [²]. As “hot forged” condition samples of 1.2 (F12) and 8.9 µm(F89) were cut and machined by turning cylinders of 10 mm in diameter to obtain SPT specimens. Disks of 1mm were cut by metallographic saw and mechanical polishing was made with emery paper up to 2000 grit. Specimens of 0.400, 0.500 and 0.600 mm in thickness were polished with thickness tolerance lower than +-1%. Small punch device is basically two halves of dies that locate the specimen by clamping or simple bend in a receiving hole. Reference [³] details the dies, their dimensions and systems to record displacements and load. The puncher is a ceramic ball of 2.5mm in diameter pushed by a hard steel plunger. The Instron 5567 electromechanical testing machine was used to apply displacement at constant crosshead speed of 0.1 mm/min. SPT were performed up to maximum load for all cases. Special case of study was made for unclamped specimens of F12 material and the cold press material (CP12) before being subject to hot forging. Both materials were tested in order to study the changes in mechanical behavior. Two displacements were recorded during all tests: i) plunger displacement (δ_EXT) measured with an extensometer MTS 25 mm gage length and ii) bottom face displacement (δ_BOT) measured with by a displacement transducer (HBM W1T3 +- 1mm). The transducer was coupled to a push rode in direct contact with the bottom face of the specimen. Load was monitored by an Instron load cell of 1 kN.

3. RESULTS AND DISCUSSION

3.1 SPT behavior until P_MAX

The plots of figure 1a represent the mechanical behaviors obtained by SPT for F12 and F89 materials until maximum load P_MAX (defined by an arrow). The displacements showed in these plots correspond to measurements from bottom face δ_BOT. This displacement allows capturing directly the pure movement of the center of the disk. Two tests per material were carried out in order to evaluate the reproducibility.

Figure 1
(a) SPT plots measured from δ_BOT. Regimes of elastoplastic deformations are separated by fine dotted lines. (b) Typical plots of uniaxial tensile test.

The four deformation stages were developed in the case of F89: I- elastic bending, II- plastic bending, III- membrane stretching and IV-plastic instability before reaching maximum load P_MAX, as demonstrated by dotted lines in figure 1a. The results for F89 showed good reproducibility. The material F12 showed only the development of two stages followed by a sudden instability before reaching P_MAX at shorter displacement. Moreover, F12 showed significant variations in terms of both P_MAX value and the corresponding displacement for P_MAX (δ_MAX). From several tests made on both materials the damage beginning could be clearly detected at P_MAX. If the ball is forced to penetrate after reaching P_MAX the load started decreasing. That was a case of fine line plot of F12 showed in figure 1a, where a growing crack after reaching P_MAX was confirmed in light microscope after unloading.

Figure 1b shows the representative tensile behaviors obtained from uniaxial tests for F12 and F89. Data were taken from reference [¹]. They showed that F89 has more than twice of maximum elongation εUTS (eng. strain at ultimate tensile strength) respect to F12. A qualitative analyze suggests that the ratio between ε_UTS(F89)/ε_UTS(F89) elongations obtained from uniaxial tensile tests was in agreement with the ratio of δ_MAX(F89)/δ_{MAX (F89)}obtained from respective SPT tests.

3.2 Evaluation of bonding process by SPT

Before to perform the hot forging, the green body (CP12) was obtained from cold compaction at 200MPa. In order to compare the mechanical states of CP12 and F12 unclamped tests were performed in specimens in 0.500mm in thickness for both materials. Drastic difference in PMAX was obtained: 13 N for CP12 with a brittle behavior while 266 N was obtained for F12 with a ductile behavior followed by a development of damage. Two specimens of CP12 were tested under the same condition and three or four parts in a brittle manner were obtained. Figure 2 show a macroscopic view of both materials after tests. The difference in mechanical behavior reveals the strong bonding obtained during the hot forging. While a high density is obtained by cold compaction (isostatic pressing) in CP12, enough bonding between powder particles is not provided. In reference [⁹] it was discussed this phenomena for axial compaction of aluminum powder. Aluminum particles are subject to extremely high contact pressure leading to severe plastic deformation but the oxide film hinders the proper bonding between metallic particles. As powder is finer the barrier mechanism is increased due to higher surface density. In spite of pronounced brittleness of CP12, which was even too brittle to machine the specimens, SPT was a feasible technique to evaluate its mechanical properties.

Figure 2
Optical micrograph of tested specimens of F12 (left) and CP12 (right).

3.3 Displacement measurement methods

Most of the publications represent SPT curves in terms of load (P) vs. punch displacement (δ). However, punch displacement is not good enough representative of a pure displacement derived from the contact point between ball and the specimen. Sometimes crosshead is computed as puncher displacement, while in other cases the transducer (extensometer or LVDT for instance) is attached directly to the puncher providing more isolated measurements. This way to measure could lead to compute extra displacements due to compliance of puncher (plus the ball if it used as indenter). Thus, if the puncher has low stiffness the recorded displacement is higher than the travel of the contact point of the indenter with specimen. In order to extract the pure displacement of the contact point a discount of elastic compliance should be done [⁴, ⁷, ¹⁰]. For the present work the two direct measurement are studied i) δ_BOT obtained directly from the extensometer attached and ii) δ_EXT which represent the recording by the extensometer. Figure 3a and 3b shows the first and the transition to second regime of deformation for F89 and F12 respectively. It is noted for δ_EXT coarse that is not linear from zero to low loads (indicated with the circle in the figures 3a and 3b). This behavior reflects plastic indentation of ball into disk due to a high effective contact pressure that leads to local yielding in a confined zone. In spite of compliance correction of δ_EXT performed initial non linear coarse of the plot remains [⁴, ¹⁰].

Figure 3
SPT plots for first and the transition to second regimens of deformation measured by from δ_BOT and δ_BOT for(a) F12. (b) F89. Both tests made in 0.500 mm thickness specimens.

In contrast when plots of figures 3a and 3b are in function of δ_BOT, they show linear behaviors from the beginning, covering more extended range of load. In addition δ_BOT reveals a higher slope of linear regime than that for δ_EXT. Therefore, a pure elastic behavior is detected during first regime when dBOT is used for SPT plots. In order to evaluate the elastic response of δ_BOT partial unloadings were effected for both materials (two cycles for F12 and single for F89) during linear region. Coincident slope and linear behavior were obtained in the unloading cycle. In contrast, the slope of same unloadings of δ_EXT resulted in higher than that for load curve (unloading cycle path is departure from initial curve in Figures 3a and 3b). It must be highlighted that only few works from open literature discuss this differences. Summarizing, it is highly recommended to evaluate the beginning of yielding by using the δ_BOT on SPT plots.

3.4 Relation of yield strength with SPT results

The assessing of yield strength proposed by MAO and TAKAHASHI [⁸] uses the characteristic load P_Y obtained from SPT. P_Y represents the end of the elastic bending regime of a thin circular plate clamped and indented by a concentric load. The relation proposed for this mechanism is through a correlation parameter α as:

$${\sigma }_{YS}=\alpha P_Y/t^2$$ (1)

Different methodologies have been proposed to define P_Y. MAO and TAKAHASHI [⁸] defined P_Y^MAO as the intersection of the representative lines of regimen I and II (labeled in figure 4a and 4b), elastic and plastic bending respectively. However this intersection P_Y^MAO falls out from P vs. δ curve. Following a similar procedure suggested by the European Code [¹²] a vertical projection from P_Y^MAO was made to define a P_Y^MAO* [⁴].GARCIA et al [⁶] proposed an offset method defined by a parallel line to regime I shifted in displacement t/100. The intersection is called P_Y^t/100 is equivalent to engineering definition of 0.2 % strain to calculate the yield stress. The cited definitions of P_Y^MAO, P_Y^MAO* and P_Y^t/100are shown in figures 4a and 4b for F12 and F89 respectively. It should be noted that another offset t/10 method is also found in the open literature [⁴,⁷].For the present work only two definitions P_Y^MAO*and P_Y^t/100 will be analyzed due to these respective load represent the beginning of plasticity [⁴]. Other authors assume that massive yielding is the right criterion to define the fully plastic behavior [⁷,¹²], that is the case of t/10 method.

Figure 4
SPT plots for first and the transition to second regimen of deformation measured by from δ_BOT for (a)F12. (b)F89. Both tests were performed with0.400, 0.500 and 0.600mm thickness specimens.

Figure 5
Linear fittings of equation (1) for (a)F12. (b)F89.

It is also noted that the effect of thickness variation has to be taken into account very carefully because small variations have strong incidence in load change in SPT curve. Thus, the accurate thickness variation has been accomplished during specimens preparation. The effect of thickness can be seen in the both material in figures 4a and 4b slopes of first regime are in accordance roughly as t³.

Assuming that this equation (1) is valid for different material thickness, the increase of P_Y should compensate for t²increment. From figures 5a and 5b the collection of P_Y for Mao* and t/100 methods were plotted for both composites. The linear fittings passing by zero for each material in terms of σ t² vs. P_Y was done. Good linearity was obtained for all fittings and the slopes of these fittings are the respective correlation parameters of equation (1). Similar correlation parameters close to 0.83 was obtained for both materials for t/100 method. On the one hand, there is no big difference in respect to choose method for the case of F12. On the other hand, the physical meaning of P_Y is still under debate [⁴,⁷,¹⁰,¹²] . A selection of P_Y methodological criteria should be complemented with more detailed analyze of plasticity development across the whole specimen thickness. According to this work the t/100 method provides a better relation of uniaxial yield strength with SPT parameters.

4. CONCLUSIONS

Small punch test was used to evaluate mechanical behavior of two hot forged Al-Al₂O₃composites fabricated of 1.2 and 8.9 µm Al 99.8% powders. The disks specimens with the diameter of 10 mm and the thickness of 0.400, 0.500 and 0.600 mm were employed. The following conclusions are drown:

A sudden change from brittle to high mechanical strength ductile behavior was confirmed when cold compacted green body was compared to hot forged material. Such difference was due to the lack of bonding during cold compaction, while a relative high strength was found after hot forging. Therefore SPT is suitable to capture the both brittle and ductile behaviors in correspondence with such extreme values of mechanical strength.

• Indirect measurement of displacement from the top face of a specimen is distinguish ably different when compared to direct measurement from the bottom face.

• In order to identify a change in elastic response to the beginning of plastic behavior bottom displacement measurement is preferable, as neither calibration nor corrections are required in this case. The semi empiric relationship between the yield strength and the characteristic load P_Y were pursued by using the correlation parameter α. Two methods to calculate the characteristic load P_Y: i, the offset t/100 and, ii., the modified Mao were employed. For both composites a value of α = 0.83 was obtained using the t/100 method. This criterion is suggested as most representative one as it allows detection of a beginning of plastic yielding during SPT.

5. ACKNOWLEDGMENTS

Technical support from Metales Group (Centro Atómico Bariloche, CNEA Argentina) is recognized.

Financial support from international project CONICET/SAS 2013-2014 is acknowledged. Financial support from the SRDA APVV-0556-12 project and the VEGA 2/0065/16 project is acknowledged.

6. BIBLIOGRAPHY

• ¹
  BALOG, M., POLETTI, C., SIMANCIK, F., et al, “RajnerThe effect of native Al₂O₃ skin disruption on properties of fine Al powder compacts”, J.of Alloys and Comp, v.509, pp. S235–S238, 2011.
• ²
  BALOG, M., KRIZIK, P., NOSKO, M. “Forged HITEMAL: Al-based MMCs strengthened with nanometric thick Al₂O₃ skeleton”, Materials Science &Engineering, v. A613,pp. 82–90, 2014.
• ³
  MANAHAN, M.P., ARGON, A.S., HARLING, K.O. “The Development of Miniaturized Disk Bend Test for the Determination of Post Irradiation Mechanical Properties”, J. Nucl. Mater, v. 104, pp.1545-1550, 1981.
• ⁴
  MORENO, M., BERTOLINO, G., YAWNY, A. “The significance of specimen displacement definition on the mechanical properties derived from Small Punch Test”, Mat. Des, v. 95, pp. 623 – 631, 2016.
• ⁵
  PEÑUELAS, I., CUESTA, I., BETEGÓN , C. “Inverse determination of the elastoplastic and damage parameters on small punch tests”, Fatigue FractEng M, v. 32, pp. 872–885, 2009.
• ⁶
  ABENDROTH, M., KUNA, M. “Determination of Ductile Material Properties by Means of the Small Punch Test and Neural Networks”, Advanced Engineering Materials, v. 6, vn.7, pp. 536-540, 2004.
• ⁷
  GARCÍA, T.E.., RODRÍGUEZ, C., BELZUNCE, F.J. “Estimation of the mechanical properties of metallic materials by means of the small punch test”, J Alloys Compd, v. 582, pp.708–717, 2014.
• ⁸
  MAO, X., TAKAHASHI, H. “Development of a further-miniaturized specimen of 3 mm diameter for tem disk small punch tests”, J Nucl.Mater.,v. 150, pp. 42-52, 1987.
• ⁹
  MORENO, M. F., González Oliver, C. J. R. “Densification of Al powder and Al-Cu matrix composite (reinforced with 15 % Saffil short fibres) during axial cold compaction”, Powder Technology, v.206, pp.297–305, 2011.
• ¹⁰
  MORENO, M. F. “Application of small punch testing on the mechanical and microstructural characterizations of P91 steel at room temperature”, Int. J. Press.Vess.Pip, v. 1-9,pp. 142-143, 2016.
• ¹¹
  CEN Workshop Agreement, “Small punch test method for metallic materials”. CWA 15627:2006 E. Brussels: CEN; 2007.
• ¹²
  HURST, R.C., MATOCHA, K., “Renaissance in the use of the small punch testing technique”, Proceedings of the ASME 2015Pressure Vessels and Piping Conference PVP2015, Boston, Massachusetts, USA, July 19-23, 2015.

Publication Dates

• Publication in this collection
  2018

History

• Received
  01 Aug 2017
• Accepted
  25 Oct 2017