Microstructural Precipitation Evolution and In Vitro Degradation Behavior of a Novel Chill-Cast Zn-Based Absorbable Alloy for Medical Applications

: In recent years, increasing interest has been placed in the development of Zn alloys for absorbable biomedical applications. It has been demonstrated that these alloys are potential candidates for endovascular applications. In the present work, a novel Zn-12.5Ag-1Mg alloy was investigated as a potential biomedical absorbable material. As a reference, the exhibited biocompatible properties are compared with those of pure Zn and a Zn-1Mg alloy. All the alloys investigated in this work were cast in a water-cooled Cu-mold (chill casting). Subsequently, the alloys were solution-treated and then extruded. The microstructural evolution at each stage of the alloy processing was resolved by analytical means including optical, scanning, transmission microscopy, and X-ray di ﬀ raction. By these means, the various phases belonging to this alloy system were disclosed. In addition, determinations of both corrosion and mechanical properties were carried out in the proposed Zn-12.5Ag-1Mg alloy. In particular, an excellent combination of strength and ductility was found, which is attributed to grain reﬁnement as well as the precipitation of a uniform distribution of reﬁned phases (i.e., AgZn solid solution, ε -AgZn 3 , and Ag 0.15 MgZn 1.85 intermetallics). All the precipitated intermetallics were embedded in a η -Zn matrix. As for the corrosion degradation in the physiological NaCl solution in the as-extruded condition, the experimental outcome indicates that the Zn-12.5Ag-1Mg alloy exhibits degradation rates far superior to currently reported ones for Zn-based alloys intended for absorbable biomedical applications.


Introduction
Absorbable metals are considered revolutionary as they introduce a new class of materials for applications as biomedical devices. Currently, pure Mg, Fe, and Zn are the dominant metallic materials in the development of novel absorbable alloys [1][2][3]. In particular, a well-known disadvantage of Mg alloys is related to its rapid degradation including hydrogen evolution in physiological environments.
In the present work, a Mg-Zn-Ag ternary alloy was chosen based on crystallographic and microstructural considerations [23]. The experimental alloys were cast from high purity Zn (99.99%), Ag (99.99%), a Prior to melting, three gas evacuations reaching 1 Torr were carried out. An Ar gas was introduced for purging purposes inside the chamber furnace. Subsequently, the two alloy systems (Table 1) were brought to above 500 °C and 850 °C and poured at ~460 °C and ~770 °C, respectively. Melting was conducted at 12 kW input power for 5-7 min (depending on the alloy system). Figure  1a shows the Cu-mold containing a cylindrical perforation to rapidly solidified billets of 25 mm in diameter and ~70 mm in length ( Figure 1b). Annealing was carried out in a Carbolite RHF 1600 furnace (Carbolite Inc., Hope Valley, UK) at 370 °C ± 2 °C for 3 and 5 h, respectively, followed by water quenching. A significant grain refinement was achieved by extruding all Zn-based alloy billets at 280 °C ± 5 °C in the form of 10 mm cylindrical rods (see Figure 1c).

Microstructural Characterization
Sections parallel to the extrusion direction of the cylindrical bars were metallographically prepared and chemically etched in a 5 vol. % HNO3 + ethanol for 10 to 60 s, depending on the alloy composition. High-resolution transmission electron microscopy (HRTEM), JEM ARM200F (Jeol Inc., Prior to melting, three gas evacuations reaching 1 Torr were carried out. An Ar gas was introduced for purging purposes inside the chamber furnace. Subsequently, the two alloy systems (Table 1) were brought to above 500 • C and 850 • C and poured at~460 • C and~770 • C, respectively. Melting was conducted at 12 kW input power for 5-7 min (depending on the alloy system). Figure 1a shows the Cu-mold containing a cylindrical perforation to rapidly solidified billets of 25 mm in diameter and~70 mm in length ( Figure 1b). Annealing was carried out in a Carbolite RHF 1600 furnace (Carbolite Inc., Hope Valley, UK) at 370 • C ± 2 • C for 3 and 5 h, respectively, followed by water quenching. A significant grain refinement was achieved by extruding all Zn-based alloy billets at 280 • C ± 5 • C in the form of 10 mm cylindrical rods (see Figure 1c).

Mechanical Characterization
The exhibited mechanical properties were obtained from microhardness determinations and tensile testing following the ASTM E8-08-16a standard [24]. The extruded bars were tensile tested at a strain rate of 4.2 × 10 −5 s −1 in an Instron 1125 machine (MTS Systems Corporation, Eden Prairie, MN, USA). Average and standard deviation of tensile properties were estimated based on three tests for each condition. Ten microhardness readings were taken for each sample using a Vickers hardness tester (THBRV -187.5V, Lab. Testing Technology, Zhejiang, China); the load used was 500 gf with a dwelling time of 15 s.

Corrosion Behavior
To determine the specimen's corrosion rates, a transverse section of the extruded rods ( Figure 1) were cut (1 cm of diameter). Surface preparation consisted of mechanical polishing from 80 to 1000 grit SiC paper, and the final mirror surface was achieved by using 50 nm alumina. Finally, all samples were degreased and dried with acetone and air (compressed), respectively. A typical three electrode cell was used to perform corrosion measurements. A saturated calomel electrode (SCE) was the reference electrode (Radiometer Analytical, Lyon, France), graphite rods were used as counter electrodes, and Zn-based specimens were the working electrodes. The exposed area of the working electrode was 1 cm 2 . In each condition, the tests were repeated 3 times to ensure reproducible and reliable results.
The electrochemical measurements were obtained using a BioLogic VSP-300 Potentiostat-Galvanostat (BioLogic Inc., Seyssinet-Pariset, France). The open circuit potential (OCP) was monitored for a duration of 7200 s. Potentiodynamic polarization (PP) measurements were carried out, using ±300 mV over the previously determined open circuit potential at a 0.166 mV·s −1 sweep. All the corrosion tests were conducted in a NaCl solution at physiological concentration to investigate the effect of Cl − ions on the experimental alloys. The electrolyte was stirred and maintained at 37 ± 1 • C (body temperature) by a coil heater during all the duration of the test. The pH of the pseudo-physiological solution was adjusted to 7.4, by adding 1 M HCl or 1 M NaOH as required. The electrolyte was a physiological saline solution, prepared with 8.94 g of NaCl (Sigma Aldrich S5886-1 KG) in 1 L of nano-pure water as reported by Tolouei et al [25].
The Stern equation predicts that for E > E corr , the anodic reaction predominates and, for E < E corr , the cathodic reaction predominates. This is known as the Tafel approximation described in Equations (1) and (2): To validate Tafel extrapolation, a general criterion was considered taken into consideration the following points; (1) at least one of the branches from the polarization curve must exhibit Tafel's behavior, (2) extrapolation could be done at least 100 mV with respect to E corr . For each branch, and (3) at least one of the branches from polarization curves should be under polarization activation zone [26]. Additionally, extrapolation fitting was completed by EC-Lab software 11.3 (BioLogic Inc., Seyssinet-Pariset, France) to calculate the corrosion potential (E corr ), Metals 2020, 10, 586 5 of 20 corrosion current value (I corr ), and Tafel coefficients (β a and β c ). Linear regression was done by using a log(|I|) vs. E representation.
Nelder and Mead Simplex method was used to find numerical parameters reducing the associated error between I calc,i and I meas,i by the next expression [26], Tafel corrosion current and corrosion rate (CR) in mm·year −1 was determined according to the ASTM G102-89-2015 [27]. Figure 2a,d displays optical micrographs of the as-cast condition for Zn-1Mg and Zn-12.5Ag-1Mg, respectively. Under the solidification conditions employed, a cooling rate of~80 • C/s was achieved for the Zn-1Mg and~3000 • C/s for the Zn-12.5Ag-1Mg alloy as estimated from the expression proposed by Jones [28], λ = Bε −n (where λ = secondary dendrite arm spacing, B = alloy constant, ε = cooling rate K/s, and n = 1/3). These cooling rates gave rise to secondary dendrite arm spacings of~25 µm for Zn-1Mg and~6.5 µm for Zn-12.5Ag-1Mg, respectively. The resultant secondary dendrite arm spacing for the Zn-1Mg alloy indicate an appreciable refinement when compared with the value reported by Mostaed et al. of~110 µm [29] for an alloy of similar composition. This clearly shows that increasing the solidification rates promotes appreciable grain refinement regardless of the amount of Mg additions. A similarly effect was found in the Zn-12.5Ag-1Mg by adding Ag and Mg under relatively high cooling rates.  Figure 3 shows the microstructural evolution of Zn-1Mg after the solution treatment (ST) at 370 °C for 3 h and 5 h (Figure 3a,b). Increasing holding times promoted grain growth to average diameters of ~280 µ m and ~300 µ m, respectively, including a coarse eutectic phase surrounding the grain boundaries. Increasing the grain size after 3 and 5 h of ST in the Zn-1Mg, the reduction is slight for Zn and Zn-1Mg and within experimental error. The reduction trend is clearer in the Zn-Ag-Mg alloy, The presence of a η-Zn matrix (see Figure 2b) corresponding to equiaxed dendrites in the Zn-1Mg alloy [18] was found to be surrounded by a very thin network of a eutectic microconstituent formed by η-Zn/Mg 2 Zn 11 [30,31]. A maximum thickness of~2.6 ηm was found for this eutectic as determined by EDS means (point C from Figure 2b,c). Figure 2d,e shows the presence of precipitates and intermetallic compounds formed during solidification of the Zn-12.5Ag-1Mg alloy (point H in Figure 2e,h). In this case, dendrites of the ε-AgZn 3 phase were observed (point F in Figure 2e,f), in agreement with Liu et al. [18] and Sikora et al [32]. Moreover, a modified eutectic microconstituent containing Zn, Ag, and Mg was resolved see point G (Figure 2e-g). Figure 3 shows the microstructural evolution of Zn-1Mg after the solution treatment (ST) at 370 • C for 3 h and 5 h (Figure 3a,b). Increasing holding times promoted grain growth to average diameters of 280 µm and~300 µm, respectively, including a coarse eutectic phase surrounding the grain boundaries. Increasing the grain size after 3 and 5 h of ST in the Zn-1Mg, the reduction is slight for Zn and Zn-1Mg and within experimental error. The reduction trend is clearer in the Zn-Ag-Mg alloy, however still within experimental error, as shown in Table 3 and Figure 9a.  The microstructural evolution of the Zn-12.5Ag-1Mg alloy after the ST did not exhibit appreciably grain growth after prolonged annealing times. Yet, dendrite dissolution occurred which favored the formation of new equiaxed grains uniformly dispersed throughout the alloy matrix (see Figure 3c,d). In addition, a relatively minor amount of intermetallic compounds were found after ST. Notice that there is an absence of eutectic constituent indicating several plausible phase transformations taking place after dissolution of the as-cast microstructure (see Figures 2d and 3c,d).

Microstructural Characterization
SEM micrographs in the ST alloys after 5 h at 370 °C are shown in Figure 4. From these micrographs, it is possible to identify a high density of planar defects (e.g., twins), as well as, thickening of the interdendritic regions of the Zn-1Mg alloy (Figure 4a,b). The precipitation of three different phases was also identified from EDS microanalyses for the Zn-12.5Ag-1Mg alloy. In these case, the phases were a AgZn solid solution (medium gray, point D from Figure 4c  The microstructural evolution of the Zn-12.5Ag-1Mg alloy after the ST did not exhibit appreciably grain growth after prolonged annealing times. Yet, dendrite dissolution occurred which favored the formation of new equiaxed grains uniformly dispersed throughout the alloy matrix (see Figure 3c,d).
In addition, a relatively minor amount of intermetallic compounds were found after ST. Notice that there is an absence of eutectic constituent indicating several plausible phase transformations taking place after dissolution of the as-cast microstructure (see Figures 2d and 3c,d).
SEM micrographs in the ST alloys after 5 h at 370 • C are shown in Figure 4. From these micrographs, it is possible to identify a high density of planar defects (e.g., twins), as well as, thickening of the interdendritic regions of the Zn-1Mg alloy (Figure 4a,b). The precipitation of three different phases was also identified from EDS microanalyses for the Zn-12.5Ag-1Mg alloy. In these case, the phases were a AgZn solid solution (medium gray, point D from Figure 4c  and Mg-rich precipitates (dark gray, point G in Figure 5d-g). As the grain boundaries were not clearly distinguishable, the average grain size was determined with special care.  Figure 5c shows some microstructural features found in the Zn-12.5Ag-1Mg alloy after extrusion. Notice the aligned deformation bands along the extrusion direction and the presence of uniformly distributed spherically-shaped precipitates. The chemical composition of three different phases was clearly resolved by EDS (see Figure 5d-g). These phases are the ε-AgZn3 phase (medium gray, point E of Figure 5d-e), a Mg-rich AgZn solid solution (light gray, point F in Figure 5d-f), and Mg-rich precipitates (dark gray, point G in Figure 5d-g). As the grain boundaries were not clearly distinguishable, the average grain size was determined with special care.
Further characterization using HRTEM revealed high-resolution microstructural details (Figures 6,7). In particular, nanometric grains of ~10 nm diameter were found in two different phases (Figure 6a) with the light gray region corresponding to zone 1 consisting of a AgZn solid solution. From Figure 6b, it was plausible to identify the 3 ̅ crystal structure, which corresponds to a cubic Further characterization using HRTEM revealed high-resolution microstructural details (Figures 6 and 7). In particular, nanometric grains of~10 nm diameter were found in two different phases (Figure 6a) with the light gray region corresponding to zone 1 consisting of a AgZn solid solution. From Figure 6b, it was plausible to identify the Pm3m crystal structure, which corresponds to a cubic phase ( Table 2). The zone axis found for this cubical phase was [001]. The crystal structure of the second zone (dark gray, Figure 6c) consisted of two crystalline microstructures, a hexagonal one (P63/mmc) embedded in a AgZn solid solution (see Table 2). The zone axes for the two phases were [1213] and [001], respectively. Figure 7a shows round-shaped Ag0.15MgZn1.85 precipitates with an average diameter size of ~15 nm. These precipitates were dominant in the alloy extruded at 280 °C. Bright-field high-resolution investigations indicated that these precipitates contained some lattice distortions (white arrows), concentrated at the particle edges and the surroundings. Accordingly, semi-coherency between the hexagonal Ag0.15MgZn1.85 and the cubic AgZn solid solution was confirmed for these precipitates (see Figure 7b and Table 2). Finally, by indexing the fast Fourier transform (FFT), it was found that the zone axes for Ag0.15MgZn1.85 and AgZn solid solution were [011] and [01 1 ̅ 1], respectively. This included a misorientation angle associated with both, geometrically necessary boundaries and incidental dislocation boundaries [33] assisted by simultaneous severe plastic deformation. Moreover, a uniform distribution of precipitates is observed which combined with low and high angle boundaries [34] are expected to promote appreciable alloy strengthening effects in this ternary alloy.    Figure 7a shows round-shaped Ag0.15MgZn1.85 precipitates with an average diameter size of ~15 nm. These precipitates were dominant in the alloy extruded at 280 °C. Bright-field high-resolution investigations indicated that these precipitates contained some lattice distortions (white arrows), concentrated at the particle edges and the surroundings. Accordingly, semi-coherency between the hexagonal Ag0.15MgZn1.85 and the cubic AgZn solid solution was confirmed for these precipitates (see Figure 7b and Table 2). Finally, by indexing the fast Fourier transform (FFT), it was found that the zone axes for Ag0.15MgZn1.85 and AgZn solid solution were [011] and [01 1 ̅ 1], respectively. This included a misorientation angle associated with both, geometrically necessary boundaries and incidental dislocation boundaries [33] assisted by simultaneous severe plastic deformation. Moreover, a uniform distribution of precipitates is observed which combined with low and high angle boundaries [34] are expected to promote appreciable alloy strengthening effects in this ternary alloy.   Bright-field high-resolution investigations indicated that these precipitates contained some lattice distortions (white arrows), concentrated at the particle edges and the surroundings. Accordingly, semi-coherency between the hexagonal Ag 0.15 MgZn 1.85 and the cubic AgZn solid solution was confirmed for these precipitates (see Figure 7b and Table 2). Finally, by indexing the fast Fourier transform (FFT), it was found that the zone axes for Ag 0.15 MgZn 1.85 and AgZn solid solution were [011] and [0111], respectively. This included a misorientation angle associated with both, geometrically necessary boundaries and incidental dislocation boundaries [33] assisted by simultaneous severe plastic deformation.
Moreover, a uniform distribution of precipitates is observed which combined with low and high angle boundaries [34] are expected to promote appreciable alloy strengthening effects in this ternary alloy.   Figure 8 shows XRD patterns for the Zn-1Mg and Zn-12.5Ag-1Mg alloys subject to the different processing routes. In the extruded pure Zn (Figure 8a), intensity peaks corresponding to the η-Zn solid solution were found in agreement with Liu et al [18]. For the Zn-1Mg, new peaks appeared (Figure 8b) corresponding to Zn 2 Mg 11 precipitation (Figure 2b,c), while the η-Zn phase peaks remained present. After the ST at 370 • C for 5 h, there were no new peaks related to other precipitates (Figure 8c), only morphological changes, as shown in Figures 3b and 4a. After extrusion at 280 • , new phase precipitation occurred as shown in Figure 8d. Notice the new reflections at 36.14 • , 43.02 • , and 54.07 • corresponding to the Mg 4 Zn 7 phase. In particular, extrusion processing induced precipitation due to plastic deformation and fracture of the eutectic microconstituent (Mg 2 Zn 11 , Figure 5b). Figure 8e shows reflections from several phases related to the as-cast Zn-12.5Ag-1Mg alloy, including the η-Zn phase, a second solid solution composed by Ag and Zn with a cubic crystal structure (Pm3m), and two hexagonal phases (P63/mmc), that is, ε-AgZn 3 and Ag 0.15 MgZn 1.85 (Figure 2e-h). After ST for 5 h, all the phases already found in the as-cast condition were preserved (Figure 8f), despite the morphological changes caused by the thermal treatment (Figures 3d and 4c). The Ag 0.15 MgZn 1.85 phase found after extrusion were identified as shown in Figure 8g. Notice that they have a spherical morphology (5d-g). Apparently, the implemented solution treatment and subsequent processing by alloy extrusion was not able to dissolve these hexagonal intermetallics. Therefore, in this case, the challenge in alloy design is to be able to maintain a highly uniform distribution of precipitates in the ternary alloys.

XRD Characterization and Phase Identification
Under these conditions, the resultant alloys are expected to make a significant contribution to alloy toughness. Table 2 gives a summary of the phases identified each step of the way during the processing of the Zn-based alloys, including their corresponding crystallography and EDS.   Tables 3 and 4 show the exhibited mechanical properties of the experimental alloys. Moreover, Vickers hardness measurements and a bar diagram of the tensile properties for the Zn alloys are given in Figure 10a,b, including their fracture morphologies (see Figure 10c,d), where it is possible to observed a ductile behavior exhibited by the ternary alloy (Figure 10d), in comparison to the Zn-1Mg system (Figure 10c). After ST for 3 h at 370 • C, the Zn-12.5Ag-1Mg alloy hardness was 177.6 ± 9.8 HV and then 164.5 ± 8.1 HV after 5 h of holding time (see Table 3 and Figure 10a). As expected, increasing ST holding times increases the alloy ductility for the investigated compositions. The reduction in hardness values from 61.6 ± 4.0 HV to 33.4 ± 1.9 HV after extrusion for the Zn-1Mg alloy and from 164.5 ± 8.1 HV to 151.5 ± 4.8 HV for the Zn-12.5Ag-1Mg can be related to further precipitate coarsening events with time at temperature (Table 3, Figure 10a).  Table 4. Mechanical properties and strain hardening exponent, n, of the investigated alloys.

Specimen n YS (MPa) UTS (MPa) Elongation (%)
Zn 0.23 42 ± 4 75 ± 4 71 ± 6 Zn-1Mg 0.33 80 ± 4 152 ± 6 11 ± 3 Zn-12.5Ag-1Mg 0.37 (1) , 0.76 (2) 64 ± 4 305 ± 17  From the experimental outcome, true stress-strain curves were plotted and then used for the determination of work hardening power-law exponents, n, for the Zn-12.5Ag-1Mg alloy [35] (Figure  10a,b). The resultant strength and ductility values, as well as those reported in the literature for alloys of similar composition, are given in Figure 11. In the present work, tensile properties for the Zn-1Mg alloy were found that are comparable with the ones reported by Mostaed et al. and Gong et al., [28,36]. Even though, in this work the ST was carried out at a relatively high temperature (370 °C) in order to minimize holding times (5 h max.). This together, with a slightly high extrusion temperature (280 °C) brought about a notable reduction in yield strength (YS) (80 MPa) and UTS (152 MPa) values (see Figure 11). Surprisingly, the elongation to fracture remained relatively high, near 11% (Figure 9b).   From the experimental outcome, true stress-strain curves were plotted and then used for the determination of work hardening power-law exponents, n, for the Zn-12.5Ag-1Mg alloy [35] (Figure  10a,b). The resultant strength and ductility values, as well as those reported in the literature for alloys of similar composition, are given in Figure 11. In the present work, tensile properties for the Zn-1Mg alloy were found that are comparable with the ones reported by Mostaed et al. and Gong et al., [28,36]. Even though, in this work the ST was carried out at a relatively high temperature (370 °C) in order to minimize holding times (5 h max.). This together, with a slightly high extrusion temperature (280 °C) brought about a notable reduction in yield strength (YS) (80 MPa) and UTS (152 MPa) values (see Figure 11). Surprisingly, the elongation to fracture remained relatively high, near 11% (Figure 9b).  From the experimental outcome, true stress-strain curves were plotted and then used for the determination of work hardening power-law exponents, n, for the Zn-12.5Ag-1Mg alloy [35] (Figure 9a,b). The resultant strength and ductility values, as well as those reported in the literature for alloys of similar composition, are given in Figure 11. In the present work, tensile properties for the Zn-1Mg alloy were found that are comparable with the ones reported by Mostaed et al. and Gong et al., [28,36]. Even though, in this work the ST was carried out at a relatively high temperature (370 • C) in order to minimize holding times (5 h max.). This together, with a slightly high extrusion temperature (280 • C) brought about a notable reduction in yield strength (YS) (80 MPa) and UTS (152 MPa) values (see Figure 11). Surprisingly, the elongation to fracture remained relatively high, near 11% (Figure 10b).
Regarding the Zn-12.5Ag-1Mg alloy, for comparison purposes there are only a few ternary or quaternary systems proposed as absorbable materials [15,16]. The main reason for this is the increasing system complexity when additional elements are introduced to improve the mechanical performance. In this sense, Mg additions to Zn alloys are desirable in order to provide superior mechanical properties together with a high level of cytocompatibility [36]. In a previous work, two Zn-based ternary alloys, Zn-1Mg-1Ca and Zn-1Mg-1Sr [37], were investigated. Both alloys had a relatively small difference in YS and UTS values (205 MPa and 201 MPa, and 257 MPa and 253 MPa, respectively). Nevertheless, these alloys were relatively brittle with elongation values of 7.4% and 5.3% respectively. Additionally, a Zn-3Cu-1Mg alloy system was explored with relatively high YS and UTS values of 427 MPa and 441 MPa, respectively [38]. Surprisingly, the alloy elongation was extremely low (0.9%). This lack of enough ductility was attributed to the development of Mg 2 Zn 11 brittle intermetallics [38]. Therefore, Mg additions are expected to improve tensile strength at expenses of alloy ductility. In this work, the mechanical properties of the investigated alloys greatly exceed the ones reported by Liu et al., [37]. In addition, the alloy possesses an outstanding elongation to failure of 21% (see Table 4 and Figure 11).
As for the role of Ag additions combined with extrusion processing, the experimental outcome indicates that this is an effective method to achieve appreciable grain refinement. As a result, alloy ductility and strength are significantly improved (see Table 4). respectively). Nevertheless, these alloys were relatively brittle with elongation values of 7.4% and 5.3% respectively. Additionally, a Zn-3Cu-1Mg alloy system was explored with relatively high YS and UTS values of 427 MPa and 441 MPa, respectively [38]. Surprisingly, the alloy elongation was extremely low (0.9%). This lack of enough ductility was attributed to the development of Mg2Zn11 brittle intermetallics [38]. Therefore, Mg additions are expected to improve tensile strength at expenses of alloy ductility. In this work, the mechanical properties of the investigated alloys greatly exceed the ones reported by Liu et al., [37]. In addition, the alloy possesses an outstanding elongation to failure of 21% (see Table 4 and Figure 11). As for the role of Ag additions combined with extrusion processing, the experimental outcome indicates that this is an effective method to achieve appreciable grain refinement. As a result, alloy ductility and strength are significantly improved (see Table 4). The development of Mg2Zn11 or MgZn2 intermetallics was not detected in the extruded condition. This in contrast with published reports for alloy systems with Mg additions [36,39,40]. Another factor which has a strong influence on the precipitation sequence is the ST temperature. This temperature should be high enough in order to achieve total precipitate and dendrite dissolution. In turn, this has a determinant effect on the exhibited mechanical properties. Table 3 shows the effect of The development of Mg 2 Zn 11 or MgZn 2 intermetallics was not detected in the extruded condition. This in contrast with published reports for alloy systems with Mg additions [36,39,40]. Another factor which has a strong influence on the precipitation sequence is the ST temperature. This temperature should be high enough in order to achieve total precipitate and dendrite dissolution. In turn, this has a determinant effect on the exhibited mechanical properties. Table 3 shows the effect of various annealing times for the investigated alloys showing in general a decreasing trend in alloy strength with increasing times.
As for the work hardening properties of the Zn-base ternary alloy (Figure 9), in the investigated Zn-12.5Ag-1Mg alloy after extrusion, the initial n value is 0.37. Nevertheless, from the log(σ) − log(ε) relationship (Figure 9a), an inflection point on this curve is found at log (ε) = − 1.3. Therefore, two values of work hardening exponent are obtained that is 0.37 and 0.76. The exhibited work hardening properties can be explained by considering the alloy microstructural features. From Figure 6a, the presence of two different phases was already disclosed by TEM means. A ductile AgZn solid solution was identified (Figure 6b), and the presence of ε-AgZn 3 hexagonal phase nanometric crystallites embedded in a cubic AgZn solid solution (Figure 6c). Therefore, during deformation, at relatively low strains, dislocation motion encounters relatively significant opposition provided by the solid solution phase, and soft-precipitates, grain boundaries, including coherent nano-phases (regions holding AgZn cubic solid solution grains). Yet at increasing strain, other hard phases become dominant, dislocation obstacles leading to an increase in the alloy work hardening.

Corrosion Behavior
Potentiodynamic tests carried out in Zn-12.5Ag-1Mg, Zn-1Mg, and Zn in NaCl indicated a decreases cathodic reaction by modifications mixed potential towards more negative values compared to "pure zinc" (SCEs = −1.044 V, −1.056 V, and −1.092) with alloying additions. In turn, this indicated that the metal-electrolyte interface was increasingly active when Ag was added as alloying element. Regarding to hydrogen evolution, all the specimens exhibited a current limit in the cathodic zone of the curve. In particular, it is found that this current limit tends to increase as the amount of alloying elements (Ag and Mg) is increased and as a result there is increasing metallic dissolution.
Tafel extrapolation was implemented to the polarization curves in order to investigate the corrosion phenomena undergone in the Zn-based alloys.
From Figure 12, anodic branches were used to perform Tafel analysis due it was observed a current limit typical of hydrogen formation in the cathodic zone. This current increases with the presence of alloy elements (such as An or Mg) and modify the cathodic response. To prevent calculation errors related to the aforementioned observations, the corrosion potential and corrosion current density were calculated using the anodic zone with a properly adjustment. As mentioned in the past section, Mg2Zn11 intermetallics were not found in the extruded Zn-1Mg specimens. In contrast, both Mg4Zn7 and Mg0.971Zn0.029 precipitates were detected as evidenced in Figure 8d. These precipitates are known to be highly corrosion resistant when compared with the matrix, so they act as cathodic spots which accelerate the corrosion rates of the surrounding matrix. Overall, the corrosion rate of the Zn-1Mg alloy increases, attaining a value of 0.683 mm·year −1 in comparison with 0.525 mm·year −1 for pure Zn. An even faster corrosion rate is achieved by adding Ag, reaching values of up to 1.251 mm·year −1 (see Table 5), in agreement with the work of Sikora-Jasinska et al., [31]. The surface corrosion morphologies found in Zn-1Mg and Zn-12.5Ag-1Mg are shown in Figure  13. Notice the degradation product layer found on the surface of the Zn-1Mg alloy. The layer was quite uniform and generally adherent to the surface; some craters were found on the degraded surface, showing the underneath base material. XRD phase identification of the corroded specimens From the anodic slopes, electrochemical parameters were estimated, and the measured current densities are summarized in Table 5. Notice that the anodic slopes corresponding to pure Zn, Zn-1Mg and Zn-12.5Ag-1Mg are 0.167 V/SCE, 0.129 V/SCE, and 0.107 V/SCE, respectively ( Figure 12). A comparison of the I corr values (Table 5) shows that pure Zn has the lowest oxidation rates. In contrast, the Zn-12.5Ag-1Mg alloy exhibits an increment in the corrosion rate with a drop in the magnitude of the anodic slope. As mentioned in the past section, Mg 2 Zn 11 intermetallics were not found in the extruded Zn-1Mg specimens. In contrast, both Mg 4 Zn 7 and Mg 0.971 Zn 0.029 precipitates were detected as evidenced in Figure 8d. These precipitates are known to be highly corrosion resistant when compared with the matrix, so they act as cathodic spots which accelerate the corrosion rates of the surrounding matrix. Overall, the corrosion rate of the Zn-1Mg alloy increases, attaining a value of 0.683 mm·year −1 in comparison with 0.525 mm·year −1 for pure Zn. An even faster corrosion rate is achieved by adding Ag, reaching values of up to 1.251 mm·year −1 (see Table 5), in agreement with the work of Sikora-Jasinska et al., [31].
The surface corrosion morphologies found in Zn-1Mg and Zn-12.5Ag-1Mg are shown in Figure 13. Notice the degradation product layer found on the surface of the Zn-1Mg alloy. The layer was quite uniform and generally adherent to the surface; some craters were found on the degraded surface, showing the underneath base material. XRD phase identification of the corroded specimens for all Zn-based alloys and its corrosion products are shown in Figure 14.  From Figure 13a, preferential attack corrosion was found in the Zn-1Mg alloy, where degradation zones are distinctly visible. Notice that Mg-rich precipitates ( Table 2) were found in discrete sites. Moreover, Mg 4 Zn 7 phase is extremely resistant to corrosion due to their electrochemical stability, which favors sites where corrosion morphology is not uniform (Figure 13b).
For the ternary alloy Zn-12.5Ag-Mg (Figure 13c), it can be observed a different corrosion mechanism with respect to Zn-1Mg alloy, exhibiting a surface covered by cracks. This degradation is slightly favored along the grain boundaries where a combination of the ε-AgZn 3 and Ag 0.15 MgZn 1.85 is observed. Therefore, when Ag is added as an alloying element, a galvanic cell corrosion is preferential (Figure 13d). Consequently, all grain boundaries act as an anode with respect to the matrix, facilitating, in thermodynamic terms, localized potential differences, which create a micro-galvanic cell mechanism.
Diffraction analyses carried out on the surface of the corroded specimens confirmed the presence of Zn, ZnO, and Zn(OH) 2 in pure Zn (Figure 14a), in agreement with Bowen et al. [22] and Zheng et al. [4]. In the Zn-1Mg alloy similar degradation products were found (Figure 13a), including Mg 0.97 , Zn 0.029 , and Mg 4 Zn 7 intermetallics (see Figure 14b). These intermetallic compounds possess a relatively high corrosion resistance, thus causing rapid and local erosion. From Figure 13a, preferential attack corrosion was found in the Zn-1Mg alloy, where degradation zones are distinctly visible. Notice that Mg-rich precipitates ( Table 2) were found in discrete sites. Moreover, Mg4Zn7 phase is extremely resistant to corrosion due to their electrochemical stability, which favors sites where corrosion morphology is not uniform (Figure 13b).
For the ternary alloy Zn-12.5Ag-Mg (Figure 13c), it can be observed a different corrosion mechanism with respect to Zn-1Mg alloy, exhibiting a surface covered by cracks. This degradation is slightly favored along the grain boundaries where a combination of the ε-AgZn3 and Ag0.15MgZn1.85 is observed. Therefore, when Ag is added as an alloying element, a galvanic cell corrosion is preferential (Figure 13d). Consequently, all grain boundaries act as an anode with respect to the Figure 14c corresponds to XRD pattern of the corroded Zn-12.5Ag-1Mg surface alloy. In this alloy, corrosion products such Zn 0.15 MgZn 1.85 ; ε-AgZn 3 ; and ZnO, ZnO, and Zn(OH) 2 were detected. Consequently, plausible dissolution-passivation mechanisms in the investigated alloys can be identified according to the following reactions.
Zn oxidation reaction sequence: