The production of fully dense nanocomposites with a homogeneous distribution of nanoparticles through powder metallurgy (PM) techniques is challenging. Additionally to mechanical milling, pressing and sintering, a final consolidation process is needed to fully densify the nanocomposite. Hot isostatic pressing (HIP) is a promising alternative method to other hot forming processes to eliminate porosity in these PM parts. In contrast to hot extrusion, for instance, isotropic properties are achieved, and textures, as they are usually observed in Mg after uniaxial deformation, are avoided. Here, we evaluate the effect of HIP on the densification, microstructure and (nano)hardness of Mg–SiC nanocomposites. Even though density increased indeed, we observed no increase in the mechanical properties, due to significant heterogeneity in the microstructure. SiC-free regions with a higher grain size developed. Local nanohardness measurements of the HIPed Mg nanocomposite revealed that these regions had a significantly lower nanohardness than the SiC-containing regions. Under consideration of mechanisms reported to be active in Mg in the pressure and temperature regime we used, we conclude that grain growth is the most likely mechanism leading to the microstructure observed after HIP. This is driven by the thermodynamic pressure to decrease the grain boundary energy and facilitated by a slightly inhomogeneous distribution of SiC nanoparticles in the sintered nanocomposite.
Hinweise
Claudia Fleck and Sepideh Kamrani contributed equally to the paper.
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Introduction
Strength and stiffness of metallic materials can be significantly improved compared to the pure metal by adding nanoscale particles, thus designing metal-matrix nanocomposites (MMNC) [1‐3]. Such nanocomposites are usually processed through a powder metallurgical (PM) route, comprising mechanical powder compaction and sintering steps. However, achieving full density while keeping the ultrafine microstructure during the consolidation process is still a challenge. This is why an additional consolidation process is needed to fully densify the material. HIP is a promising method to eliminate porosity in these PM parts. Thus, components can be designed, which meet the specifications for use in highly stressed applications [4]. In comparison with hot extrusion as additional consolidation step, HIP avoids texture formation and, therefore, anisotropic properties due to the uniformly applied pressure. The pressure can additionally help to overcome restraining effects in composites due to nanoparticles compared to sintering [5]. Further advantages of the HIP process in general are the production of near-net shaped structures and the greater design freedom in comparison with hot extrusion [6].
Powder is often directly HIPed in a vacuum-sealed flexible capsule. However, the capsule has to be removed after HIP by machining, pickling or sandblasting [7]. Another alternative is the sinter-HIP process which combines two steps and consolidates precompacted powder, while preventing oxidation due to a better control of atmosphere and reducing the risk of grain growth due to the eliminated re-heating in the second step [5, 7]. However, in our case, we separated the process in two steps sintering and HIP in order to characterise the mechanisms occurring during the individual process steps.
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While for pure metal powders plastic deformation and creep are possible dominant mechanisms for improving the compaction during HIP [8], creep plays, however, only a minor role in the compaction of metal composite powders due to the nanoparticles [9].
Thus, hipping composites seems to involve different mechanisms than hipping pure metals. Until now, only a few studies on HIP of metal-matrix composites exist. But HIP has a high potential of achieving full theoretical density and of reaching a uniform compaction, while reducing the overall property scatter, as Xu et al. showed for a cast Al–SiC composite [10]. They further showed that yield stress decreased drastically as ductility increased mainly due to the reduction of porosity. Lange et al. investigated the influence of microinclusions on densification during HIP: inclusion volume fractions above 20% lead to inclusion networks which substantially reduced the densification rate [9]. Thus, even though the reinforcing phase constrains the deformation, strength and creep resistance of the products are nevertheless increased compared to the pure metal. For nanocomposites, this means that the amount of reinforcement has to be as small as possible, while still retaining the positive effects of nanoparticles such as Orowan strengthening and hindering of grain growth.
To the best of our knowledge, there are no reports regarding HIP of magnesium nanocomposites. We investigated the effect of HIP on the densification, the microstructure and the mechanical properties of a Mg–SiC nanocomposite with a reinforcement content of 1 vol % SiC nanoparticles compared to non-reinforced Mg. Besides microhardness, we discuss our findings regarding nanohardness and effective elastic modulus of non-reinforced Mg and Mg–SiC nanocomposite locally at the micron to the submicron scale. We then compare our findings on the densification during HIP and the resulting mechanical properties with those achieved by extrusion of Mg–SiC nanocomposites which we reported previously [11].
Experimental procedure
Processing
Nanocomposite powders with a reinforcement content of 1 vol % SiC nanoparticles were prepared by high-energy mechanical milling, precompacted by uniaxial pressing and further compacted by cold-isostatic pressing (CIP) before sintering (see Table 1). Further details are given in our previous works [11, 12]. To achieve fully dense bodies and isotropic properties, HIP was applied as additional consolidation step. The surface of the sintered samples was first ground to remove the oxide layer. Then, HIP was performed under argon atmosphere. The HIP unit was preheated to 200 °C for 1 h followed by pressure build-up to 100 MPa over 2 h. After a pressure of 100 MPa was reached, the unit was heated up to 500 °C with a heating rate of 5 K min−1. After a holding time of 1 h, the unit was cooled down to room temperature with a cooling rate of 3 K min−1 before the pressure was released. As a reference, non-reinforced Mg samples were produced in the same way as the Mg nanocomposite. Henceforth, the samples will be referred to as “non-reinforced Mg”, “Mg” and “Mg nanocomposite”, “Mg–SiC”.
Table 1
Overview of the process parameters
Temperature (°C)
Time (h)
Pressure (MPa)
Atmosphere
Mechanical milling
–
25
–
Argon
Cold-isostatic pressing
–
10 min
700
Oil
Sintering
600
2
–
Argon
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Microstructural analysis
The microstructure and the porosity of the samples following sintering and HIP were investigated on ground and polished sections. After grinding with sandpaper up to 4000-grit with ethanol as lubricant, the sections were stepwise polished, using diamond spray down to ¼ µm particle size (Struers), cleaned with ethanol and blow-dried. The pore shape and distribution and the characteristics of the nanoindents were investigated by scanning electron microscopy (SEM), using a Gemini SEM 500 (Zeiss, Germany) in secondary electron (SE) mode at an accelerating voltage of 8 kV. The grain structure of the Mg matrix and the reinforcement distribution were evaluated qualitatively by transmission electron microscopy (TEM, Tecnai G2 20 S-TWIN, FEI, USA), on a specimen prepared parallel to the uniaxial pressing direction by the focused ion beam (FIB) technique. For quantification of the grain size and to obtain a statistical grain size distribution, the diameters of at least 200 Mg grains were measured in dark field TEM micrographs using the measuring tool of the ImageJ software (National Institute of Health, USA). Further, scanning transmission electron microscopy (STEM) was used to analyse the elemental composition of the Mg grains and the grain boundaries by an energy-dispersive X-ray spectroscopy (EDS) line scan.
The relative density of the materials was determined by 2D pore analysis on SEM images by ImageJ. At least 5 SEM images of different regions of the cross section of each sample were analysed with the help of the tool “Analyze Particles” at a magnification of 500 after digital enhancement of the contrast and segmentation. The percentage amount of pores was determined within a region of interest sized 113 µm × 78 µm in each of the five micrographs.
Mechanical properties
The mechanical properties were investigated by micro- and nanoindentation for the sintered and sintered/HIPed states. Sections were prepared and polished as described above for the microstructural analysis. For the microhardness measurements, a Zwick 3212 (Germany) microhardness tester was used with a maximum force of 1.961 N (HV 0.2) and a dwell time of 10 s. To quantify the local hardness, nanoindentation was performed with a Hysitron TI 950 TriboIndenter (Bruker Corporation, Massachusetts, USA) equipped with a standard Berkovich diamond indenter tip. A maximum load of 1 mN with a dwell time of 10 s and a loading and unloading rate of 200 µN s−1 were used. At least 100 indents were made in several areas of each sample in grid-wise arrangements of 5 × 5 indents with a distance of 15 µm between the single indents to obtain a statistically significant average of nanohardness (Hn) and effective elastic modulus (Eeff). As Si-free and Si-containing regions were identified in the HIP Mg nanocomposites (see below, ch. 3.1, Fig. 2), additionally at least 50 indents were made for local nanohardness measurements in each of the two different regions using grids of 3 × 1 indents with a distance between single indents of 10 µm. Nanohardness and Eeff were determined by the method described by Oliver and Pharr [13, 14]. The statistical significance was determined homoscedastic using a t test and a two-tailed distribution at a significance level of α = 0.05 [15].
Results
Microstructural characterisation
Figure 1 shows SEM micrographs of typical metallographic sections of a non-reinforced Mg and a Mg nanocomposite specimen both after sintering (Fig. 1 a, b) and after HIP (Fig. 1 c, d). The Mg matrix appears light grey, while the former powder particle boundaries are dark grey and the pores black. The sintered samples have an almost uniform distribution of the pores. Mg exhibits more equiaxed pores (arrows), while the Mg–SiC contains elongated as well as equiaxed pores. The elongated pores appear along the contact points of former powder particles. They are thus arranged along lines, resembling a string of pearls surrounding the grains. These pores seem to be separated by thin struts of material. After HIP, the samples still show pores; in some areas, these are homogeneously distributed, in others, however, they are clustered in string-like lines, just as in the sintered nanocomposite. While the Mg does not show a significantly different pore shape compared to the sintered state, the Mg–SiC exhibits more ellipsoidal and equiaxed pores with micron and submicron sizes. Although both sintered samples exhibit different pore morphologies, the relative densities of the non-reinforced Mg and the Mg nanocomposite are similar (Table 2). In contrary, after HIP, the Mg–SiC nanocomposite exhibits the highest density, compared to the sintered state as well as compared to the pure Mg sample.
Figure 1
SEM micrographs of a, b sintered and c, d HIPed non-reinforced Mg and Mg nanocomposite: the magnesium matrix appears in light grey and the boundaries between former powder particles in dark grey. The arrows denote elongated pores which appear in black
Table 2
Relative density of sintered and HIPed samples determined by 2D pore analysis
Relative density (%)
Sintered
HIP
Non-reinforced Mg
97.9
98.1
Mg nanocomposite
97.5
99.1
×
A more detailed characterisation of the microstructure of the HIPed Mg–SiC is possible by SEM investigations. At a low magnification (Fig. 2a), we observe two different areas: one appearing in dark grey and the other one in light grey. The latter is much more abundant, comprising approximately 70 to 80% of the area, thus representing the major part of the sample. The maximum extension of the dark grey regions seems to be on the range of 40 µm. Figure 2b shows the microstructure in more detail. The areas appearing in dark grey at the lower magnification show less contrast at this magnification and have been marked with dashed lines for clarity. Figure 2c shows elemental maps of Si and Mg in the light and dark grey areas which prove that the dark and light grey areas are regions free of Si and regions containing Si, respectively. Accordingly, the dark grey areas will be referred to as “SiC-free regions” in the following.
Figure 2
SEM micrographs of a cross section of a HIPed Mg nanocomposite specimen: a enhanced material contrast imaging reveals differences in, the microstructure where some areas appear in darker grey and others in light grey; b detailed view at higher magnification (areas that appear in dark grey at lower magnification are surrounded by dashed lines): these areas appear smoother and more homogeneous, while the areas that appear brighter at lower magnification look more heterogenous; c micrograph and corresponding elemental maps of magnesium and silicon showing that Si only appears in the light grey areas
×
To further analyse the microstructure of the two different regions of the HIPed Mg–SiC in terms of grain size and SiC distribution, TEM analyses were performed. The two regions can be clearly distinguished in the dark-field TEM micrograph in Fig. 3a. At the top and the bottom of this figure, the SiC-free regions are visible, while the SiC-containing region is located in between. Figure 3b shows the SiC-free region in higher magnification illustrating large Mg grains, which are surrounded by white particles. These are MgOx, located at the grain boundaries of the Mg matrix in the SiC-free regions, as shown by EDX (Fig. 3c). The EDX analysis also affirms that no SiC nanoparticles exist within the Mg grains. The bright-field TEM micrograph in Fig. 3d shows that the SiC-containing region has small equiaxed Mg grains, with a homogeneous distribution of SiC nanoparticles throughout the grains. The grain size distribution was evaluated separately in the different areas and is displayed together in Fig. 3e. The grain size distribution is bimodal. The large amount of small grains belongs to the SiC-containing region, and the smaller number of larger grains with sizes greater than 1 µm belongs to the SiC-free region. Averaging over both regions, we determined a grain size of 270 nm.
Figure 3
TEM micrographs of a HIPed Mg nanocomposite specimen: a dark-field (DF) micrograph showing the overall microstructure parallel to the uniaxial pressing direction: SiC-free regions (top and bottom, appear light grey in SEM) and SiC-containing region in between (appears dark grey in SEM), vertical lines are artefacts from sample preparation; b DF image showing the SiC-free region, line scan in d is denoted by the white line; c bright-field micrograph showing SiC nanoparticles in the SiC-containing region which are marked with arrows; d line scan along the direction; e statistical grain size distribution shows large amount of small grains belonging to the SiC-containing regions and a low amount of large grains belonging to the SiC-free region
×
Mechanical properties
The average Vickers microhardness of all four material compositions and states is shown in Fig. 4. Considering the determined grain sizes, the Vickers indent, exhibiting a size of 40–50 µm, includes a high number of grains, thus leading to an average hardness value. On the microscale, for both materials a slight increase in hardness is observed after HIP compared to the sintered state. The HIPed Mg–SiC has the highest Vickers hardness with an increase to 49.3 HV 0.2. All states except the sintered Mg–SiC and the HIPed Mg differ statistically significantly.
Figure 4
Average Vickers microhardness values (HV 0.2): the differences between all states are significantly different with the exemption of the difference between the sintered Mg nanocomposite and the HIPed non-reinforced Mg. The black vertical lines denote the standard deviation
×
The mechanical properties on the nanoscale, and, specifically, the local property variations due to the two different, SiC-free and SiC-containing regions, in the HIPed nanocomposite were assessed by nanoindentation. Typical load–displacement curves are shown in Fig. 5. The shape of the curves is typical for an elastic–plastic behaviour. For the sintered states, the load–displacement curves are smooth, while both HIPed samples show small pop-in effects. The curves of the Mg nanocomposite are shifted slightly towards lower displacements (“to the left”) compared to the non-reinforced Mg, reflecting a higher resistance to deformation. The nanoindents of the sintered and HIPed samples (Fig. 5) have a size of approximately 1 to 2 µm and show no signs of crack initiation. Brighter areas, visible at the edges of the imprints, suggest minor pile-up.
Figure 5
a Load–displacement curves obtained by nanoindentation with a maximum load of 1 mN. Only the HIPed samples show a pop-in effect for low loads (inset). b–e SEM images of typical indents on b,c sintered and d,e HIPed cross sections of non-reinforced Mg (left: b, d) and Mg nanocomposite (right: c, e): minor pile-up is observed at the indent edges, visible as rims in lighter grey at the edges of the triangular indents, marked with arrows
×
Figure 6 summarises the nanoindentation results. Compared to the sintered samples, only the nanohardness of Mg increased significantly through HIP. The HIPed Mg and the HIPed Mg–SiC show the highest average nanohardness values, with 0.83 and 0.86 GPa, respectively, but these values are not statistically significantly different from each other.
Figure 6
a Average nanohardness and effective elastic modulus (Eeff) values of non-reinforced Mg and Mg nanocomposite in the sintered and HIPed states; b Influence of the local microstructure on the nanohardnesses and the Eeff of Mg nanocomposite: SiC-free regions possess significantly lower nanohardness than the SiC-containing regions, while Eeff is comparable. The vertical black lines denote the standard deviation
×
The average Eeff of the HIPed materials, both in the non-reinforced Mg and in the reinforced state, statistically significantly decreased by 7.5 and 9.7%, respectively, compared to the sintered samples. However, in all cases, the addition of the hard SiC nanoparticles increased the effective elastic modulus of the Mg nanocomposite as compared to the non-reinforced state.
The local nanohardness and effective elastic modulus values of the SiC-free and the SiC-containing regions in the HIPed Mg–SiC are shown in Fig. 6b. While Eeff shows no difference, the nanohardness of the SiC-free regions (0.74 GPa) is lower than nanohardness of the SiC-containing regions (0.91 GPa).
Discussion
Hot isostatic pressing has been routinely used for the production of standard sintered materials to achieve isotropic densification of metal and ceramic powders before sintering. Here, we investigated an alternative use of HIP as an additional processing step to densify Mg–SiC nanocomposites following pressing and sintering of nanostructured composite powders. We compared the outcome with hot extrusion, another uniaxial hot forming process. Due to the combined application of high pressure and high temperature, HIP is expected to profoundly modify the microstructure of the nanocomposites. Indeed, we observed significant changes in the size and shape of the pores, the grain size and the distribution of the nanoparticles. Furthermore, and importantly, the density increased. All in all, however, the mechanical properties stayed below the expected values: the high temperature allowed significant grain growth, leading to a coarsening of the microstructure and to the formation of SiC-free regions. These negative effects were not sufficiently counteracted by the positive effect of the higher density. We therefore conclude that either the isostatically applied pressure was not high enough to induce sufficient plastic deformation, or the temperature was too high, so that the coarsening of the microstructure happened too fast. Dynamic recrystallisation therefore either was totally hindered by the effect of Zener pinning by the nanoparticles, or it did not take place to an extent sufficient to counterbalance the coarsening.
In principle, at the pressure and temperature applied, a variety of deformation mechanisms are possible during HIP. Due to the ultrafine microstructure of our Mg nanocomposite, grain boundary sliding (GBS) and Coble creep may be expected to take place. Based on the densification map of Frost and Ashby for pure Mg [16], we may safely assume that dislocation creep and volume diffusion are the most likely mechanisms, besides Coble creep. In contrast, Dieringa expects that, at temperatures between 200 and 300 °C, dislocation creep and grain boundary sliding are the mechanisms preferred to Coble creep and volume diffusion [17]. Dynamic recrystallisation and Nabarro–Herring creep, on the other hand, are less likely because these mechanisms are known to occur only at higher temperatures than those we used. Furthermore, SiC nanoparticles and other fine oxide particles are well known to extensively increase the creep resistance by pinning dislocations and hindering grain boundary diffusion [18, 19].
Based on our findings, we propose the model shown in Fig. 7 that schematically describes which deformation mechanisms we assume to be active, and the sequence of events during the microstructure evolution of our materials. Ideally, the SiC nanoparticles should be homogeneously distributed in the Mg–SiC nanocomposites. The real microstructure, however, is inhomogeneous with some Mg grains lacking SiC nanoparticles along their grain boundaries. Thus, some grain boundaries are not pinned. Consequently, due to the relatively long exposure time to elevated temperatures during the HIP process, and due to the high thermodynamic pressure because of the very fine grains, grain growth is likely to occur in these areas. Concomitantly, in areas with less nanoparticles, these move together with the grain boundaries [20] and a region devoid of SiC nanoparticles and with a coarser grain size develops. Eventually, the migrating grain boundaries meet more and more nanoparticles until they are stopped. In areas where SiC nanoparticles are homogeneously distributed, grain growth is hindered through Zener pinning, and so are grain boundary sliding, dynamic recrystallisation, Coble creep and the overall diffusion. Additionally, we assume that MgO can act as a barrier and suppress volume diffusion to the grain interior. This corroborates the findings of Dadbakhsh and Hao in Al–Fe2O3 composites [21]. The existence of large Mg grains in a former ultrafine microstructure was also reported by Yao et al. for an Al6063-SiC nanocomposite after extrusion [20]. The authors explained this finding with the higher internal driving force for grain growth compared to the dragging force of few individual nanoparticles, that is, Zener pinning. In pure Mg, the fine MgO particles prevent the grain growth; however, the dragging force is not as great as that of the larger nanoparticles, which is why the grains can grow larger.
Figure 7
Schematic illustrations of ideal and real microstructures including a model of the possible mechanisms involved for a pure Mg and b Mg–SiC nanocomposite. Mg grains keep their shape due to the applied isostatic pressure. The internal driving force for grain growth is higher than the dragging force of the few individual SiC nanoparticles or MgO particles. When a certain amount of particles has accumulated, the grain boundary movement is stopped by Zener pinning, which also hinders recrystallisation
×
Interestingly, the Mg nanocomposite showed a higher densification during HIP than the non-reinforced Mg. This may be explained by the finer grain size and, thus, the higher number of grain boundaries present in the Mg nanocomposite which allows more grain boundary diffusion and sliding, despite the nanoparticles. TEM investigations could help clarify the mechanisms. However, visualising dislocations in the hcp crystal structure is very complex and challenging, especially if the grain orientations of the nano-sized Mg grains in the TEM foil are not known. In principle, EBSD analysis is a possibility to characterise the grain orientations in a TEM foil; however, this is not feasible in the Mg nanocomposites due to their extremely small grain size.
Densification of the Mg nanocomposites during HIP was lower than what we observed during hot extrusion [11]. Possible reasons are the very low strain rates and the uniform pressure during HIP. The latter leads to a uniform stress distribution within the specimen, and shear stresses are negligible. As a consequence, the overall amount of plastic deformation is lower and, thus, pore removal is less effective because the driving force for dynamic recrystallisation is lower. Additionally, due to the longer process time of HIP (> 1 h compared to a few minutes for hot extrusion), there is more time for diffusion. We may safely assume that the longer time supports some diffusion driven processes, which assist in increasing the density, and lead to a rounding of the formerly elongated pores of the Mg nanocomposite during HIP. However, the increase in density is small and other mechanisms seem more likely to contribute to densification than diffusion driven processes, as discussed above.
The microstructural features, such as grain size and SiC distribution, strongly influence the mechanical properties, according to the Hall–Petch relationship and the Orowan mechanism, respectively. The development of few SiC-free regions with their relatively large Mg grains appears to be sufficient to reduce the microhardness, so that no significant improvement can be observed compared to the sintered state despite the increase in density. Nanoindentation showed that the SiC-free regions indeed exhibit a lower local nanohardness; this may be due to deformation twinning, which is an additional deformation mechanism besides sliding of dislocations and which has been observed to take place in coarse-grained Mg to a greater extent [22]. The pop-in observed in the loading curve of the nanoindentation loading cycle corroborates twinning, as also described by Hu et al. [23]. Thus, in addition to the lower effective elastic modulus, the SiC-free regions are expected to allow a higher amount of plastic deformation. Note that the increase in Eeff in the Mg nanocomposite compared to Mg is mainly due to the higher elastic modulus of the SiC nanoparticles. The indents have edge lengths in the range of 1 to 2 µm and depths in the range of 200 nm. They are therefore much larger than the nanoparticles which exhibit sizes of up to 50 nm at maximum. We may therefore safely assume that nearly always both phases, the Mg matrix and the SiC nanoparticles are present in the indented volume, however, with locally varying relative contents. This explains the high scatter of the results, and the higher Eeff of the nanocomposites as compared to the pure Mg. Furthermore, high standard deviations of Eeff and of the nanohardness are expected, because there may be grain boundaries below the surface in the region of the indented volume which will surely influence the plastic deformation and thus the nanoindentation results.
After HIP, the result is a material with pronounced stress and strain inhomogeneity during mechanical loading. On the one hand, this heterogeneity may be disadvantageous; on the other hand, the more ductile SiC-free regions might also be beneficial in slowing cracks down. Further tests on macroscopic specimens are needed to evaluate the full potential of the nanocomposites after different processing steps.
Conclusions
Here, we report on the effect of hot isostatic pressing on the densification, the microstructure evolution and the mechanical properties measured by micro- and nanoindentation of a Mg–SiC nanocomposite. As compared to uniaxial hot forming processes, HIP is a promising alternative because the isostatic pressure may help preventing the development of a texture as it usually develops in the hcp Mg materials during hot extrusion, for instance. Even though we achieved an increase in density no increase in the mechanical properties was achieved, mainly due to grain growth and the development of SiC-free, non-reinforced regions. Since the isostatic pressure causes too little shear and, therefore, deformation energy is low, dynamic recrystallisation is not induced and the increase in density is limited. Technologically, pressures up to 200 MPa are possible. However, based on our observations and the discussion of possible deformation mechanisms, we may safely assume that doubling the pressure will not have a major influence on the densification. This is mainly due to the hindering of deformation mechanisms by nanoparticles. Further studies need to be carried out in order to validate the assumed mechanisms.
Acknowledgement
Open Access funding provided by Projekt DEAL. The authors gratefully acknowledge the financial support by the DFG (Deutsche Forschungsgemeinschaft). We also acknowledge Claudia Fasel from the group Dispersive Solids, Institute of Materials and Earth Sciences at TU Darmstadt, for her support during material production and the Non-Metallic Inorganic Materials group for providing technical cooperation. We further thank Jan Räthel from the Fraunhofer Institute for Ceramic Technologies and Systems (IKTS, Dresden) for performing the sinter and HIP process. The SEM and TEM analyses were performed at the Central Electron Microscopy Unit (ZELMI) of TU Berlin. The authors thank Christoph Fahrenson and Sören Selve for their valuable support during these measurements.
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Conflicts of interest
The authors declare that they have no conflict of interest.
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