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International Journal of Corrosion

Volume 2013 (2013), Article ID 983261, 11 pages

http://dx.doi.org/10.1155/2013/983261

## Corrosion Behavior of Commercial Aluminum Alloy Processed by Equal Channel Angular Pressing

^{1}National Center of Researches in Materials Sciences, Technopark of Borj-Cédria, BP 73, 8027 Soliman, Tunisia^{2}Laboratoire d’Energétique et d’Electrochimie des Solides (LEES), Faculté de Technologie, Université Ferhat Abbas, 19000 Sétif, Algeria

Received 23 February 2013; Revised 16 May 2013; Accepted 23 May 2013

Academic Editor: W. Ke

Copyright © 2013 Atef Korchef and Abdelkrim Kahoul. 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

A commercial aluminum alloy was subjected to severe plastic deformation through equal channel angular pressing (ECAP). The alloy contains a low volume fraction of *α*-AlFeSi located essentially at the grain boundaries. The corrosion behavior of the ECAP’ed alloy was investigated in NaCl solution using potentiodynamic polarization and immersion tests. The effects of scan rate and NaCl concentration on the alloy susceptibility to corrosion were also studied. The results obtained were compared with those of the nonpressed alloy. ECAP leads to an intensive grain refinement accompanied by an increased dislocation density. All electrochemical tests confirm that corrosion resistance of the alloy remarkably diminished with increasing the ECAP number of passes. This is presumably due to the breakdown of the *α*-AlFeSi after ECAP leading to higher number of galvanic cells and enhanced dissolution of the aluminum matrix.

#### 1. Introduction

It is now well known that severe plastic deformation (SPD) leads to enhanced grain refinement to the submicrometer (100–1000 nm) or nanometer (<100 nm) levels. The intensive grain refinement is responsible for the enhancement of physical and mechanical properties of the processed materials, such as high strength and ductility. SPD techniques include, among others, torsion under high pressure [1], accumulative roll bonding (ARB) [2], and equal channel angular pressing (ECAP) [3, 4]. The latter procedure, introduced almost 30 years ago to achieve enhanced plastic strains, is especially attractive for several near superplastic applications. Since the cross-section of the sample remains unchanged during ECAP, repetitive pressings on the same sample are possible to achieve the required strains and to invoke different slip systems by rotating differently the sample between consecutive passes [4]. Thus, the microstructure obtained after ECAP depends on the introduced strains and whether and how the sample is rotated between two successive passes. In the early stages of pressing, reported results in the literature showed that the microstructure was reasonably homogeneous and consisted of parallel bands of subgrains. For further pressings, these subgrains evolved into an array of refined grains separated by high angle boundaries [5]. As a result of the grain refinement, a significant improvement of the mechanical properties was observed after ECAP [6].

In addition, ECAP process alters the bulk of the material leading to changes in material flow, residual stress, texture, size and distribution of a second phase if any exists in the material, and so forth. In addition to grain refinement, these changes significantly affect the corrosion behavior of the material [7]. However, the results reported in the literature are often controversial claiming that the same metric could both decrease and increase susceptibility to corrosion. For example, it was suggested that the decrease of the grain size can either decrease [8, 9] or increase [10] the corrosion resistance of aluminum. In fact, depending on whether grains were equiaxed or columnar, corrosion rate would variably increase or decrease with grain refinement [7].

In previous works [11–13], we studied the effect of ECAP process on the microstructure evolution and the mechanical properties of a commercial aluminum containing a low volume fraction of *α*-AlFeSi located essentially at the grain boundaries. X-ray diffraction (XRD) analysis showed an important broadening of the reflections of the alloy attributed mainly to grain refinement and lattice distortions. The grain refinement and the accumulation of dislocations generated by ECA pressing lead to a significant improvement of the mechanical properties in compression and tension tests [13]. The present work aims to investigate the effect of ECAP on corrosion behavior of the same material. The effects of grain refinement and the *α*-AlFeSi on the susceptibility to corrosion of aluminum alloy were especially discussed. This allows gaining a more detailed insight into the effect of SPD through ECAP on corrosion behavior of aluminum alloys. The results obtained for the ultrafine grained (UFG) aluminum alloy were compared with those of the coarse grained counterpart.

#### 2. Experimental Procedure

##### 2.1. Sample Preparation

The experiments were carried out using low purity aluminum (99.1%). The material was received in the form of cast ingots. It was analysed by Inductively Coupled Plasma Optical Emission Spectrometry (ICPOES). The chemical composition is given in Table 1. The material was annealed for 24 hours at 500°C and quenched in iced water. Samples with dimensions ~10 × 10 × 70 mm^{3} were cut for ECA pressing. The die used for ECA pressing has two square channels of 10 × 10 mm^{2} cross sectional area intersecting at an angle . The arc of curvature at the outer point of the intersection of the two channels delineated an angle Ψ = 20°. According to the equation given by Iwahashi et al. [14], the total equivalent strain, , accumulated by passes through the die was equal to ~*N*.

In the present work, repetitive pressings of the same sample were conducted, at room temperature, to achieve an equivalent strain up to ~4 without rotation of the sample between two successive passes (the so-called route A [15]).

##### 2.2. Electrochemical Measurements

The electrochemical tests were conducted at room temperature in aerated stagnant NaCl solutions used as the corrosive medium at pH = 6.4. NaCl (Aldrich) was added to bidistilled water in required amounts to prepare solutions with concentrations varying between 0.15 and 0.9 M (0.875 and 5.25 wt. %, resp.).

The working electrodes used were cut from the central part of the ECA pressed ( and 4) samples. The nonpressed () aluminum alloy was also studied for comparison. Before each experiment, the working electrodes of cross-section 1 cm^{2} were mechanically polished with grinding paper up to 1000 grit to a mirror finish. The electrodes were then degreased with acetone, finally washed with bidistilled water, and dried in air. In order to avoid a prolonged exposure to atmosphere leading to oxide formation on the Al surface, the samples were tested immediately after drying. A Pt sheet was used as a counter electrode. The potential was measured against a saturated calomel electrode (SCE) as a reference. Potentiodynamic polarization curves, using a computerized potentiostat (Radiometer model VoltaLab 40) and Voltamaster 4 software, were performed by starting scanning electrode potential from an initial potential equal or below the open circuit potential (OCP) to an anodic potential of 0.3 V in 3.5 wt.% NaCl solution at pH = 6.4. Electrochemical impedance spectroscopy (EIS) measurements were carried out at open circuit potential (OCP) using the same Voltamaster 4 software. A 10 mV amplitude was applied to the electrodes under study at sweeping frequencies between 100 kHz and 0.1 Hz. Some experiments were repeated two or three times, and reproducibility was found to be satisfactory.

##### 2.3. Weight Loss Tests

The weight loss tests were carried out at room temperature in 100 mL glass beakers containing 3.5 wt.% NaCl solution at pH = 6.4. The polished and cleaned specimens were weighed and immersed for various time intervals. Once the interval time of immersion was finished, the samples were removed from the solution and cleaned with a 70 wt% HNO_{3} solution [16], washed with acetone and weighed again. The above steps were repeated, and the mass loss in every interval was measured to evaluate the corrosion rate (mg·cm^{−2}) of the samples.

##### 2.4. Surface Analysis

For X-ray diffraction (XRD), optical microscopy (OM), and scanning electron microscopy (SEM) investigations, specimens of ~5 × 5 × 10 mm^{3} were cut from the central part of the tested ECA pressed () and unpressed () samples. Their surfaces were electrolytically polished for 30 min at a temperature below 10°C under an operating voltage of 30 V, using a mixture of 66% (CH_{3}CO)_{2}O and 34% HClO_{4}. Added polishing in a 10% H_{2}SO_{4} solution was used for OM under polarized light.

##### 2.5. X-Ray Diffraction Analysis

XRD was carried out with a Philips X’PERT PRO diffractometer in step scanning mode using Co-K_{α} radiation. The XRD patterns were recorded at room temperature in scan rate of 2 × 10^{−3} deg/s in the scanning range . The exact position and the full-width at half maximum (FWHM) of each reflection was determined using X’PERT HighScore Plus software. A correction for the contribution from the instrumental effects to the experimental FWHM, , for each peak were obtained using the following expression [12]:
where is the instrumental FWHM which was determined using NaCl or the undeformed aluminum as a standard reference material.

The mean coherent crystalline domain size and strain for each pass were calculated using the Halder-Wagner (HW) method [17]. In the HW method, which assumes a Voigt peak shape, the crystallite size, , and the strain, , are related to by the following expression: From (2), the intercept of the plot of versus gives the value of the equivalent strain, and the slope gives the mean cell size.

The lattice parameter of the aluminum before and after ECA pressings was obtained from a linear regression analysis of the measured lattice parameter, , obtained from each reflection, plotted against the Nilson-Reley function [18]: and extrapolated to N-R = 0; that is, .

Assuming that the dislocation density before ECAP deformation is significantly lower than the remaining dislocation density after ECAP , could be calculated using the following equation [19, 20]: where is the coherency length (cell size) provided by XRD, (=1.07 N) is the plastic strain introduced, is the number of ECAP passes, (=0.2867 nm) is the Burgers vector of dislocation, and (=2 nm) is the annihilation distance of dislocation [20].

#### 3. Experimental Results

##### 3.1. Microstructure Investigation

###### 3.1.1. XRD Analysis

The XRD patterns of the unpressed sample () and sample processed by ECAP () between 2*θ* = 20 and 155° are given in Figure 1(a). Besides the fundamental reflections of the aluminum matrix, very fine reflections with low intensity, are observed (inset of Figure 1(a)). These reflections correspond to the presence of a second phase. In several AlFeSi commercial alloys, the phase present is usually denoted by *α*-AlFeSi (*α*-phase). Possible chemistry of the phase is Al_{8}Fe_{2}Si, Al_{12}Fe_{3}Si, or Al_{15}Fe_{3}Si_{2}. It should be noted, however, that the iron-rich phases form in commercial purity aluminum alloys in two very different forms. First is the coarse 1-2 *μ*m “constituents” formed by eutectic solidification, at a spacing of the dendrite cell size set by the solidification rate. Depending on the particular Fe/Si ratio and the casting rate, different phases may result, that is, the metastable Al_{6}Fe or the *α*-phase. Besides, there is a residual Fe content typically about 0.04 wt% left in solution after casting. This can be partially precipitated as the *α*-phase during homogenization anneals especially at the temperature used in the present work, only 500°C, or during low temperature anneals following deformation. These solid state precipitates (usually called dispersoids) are very fine (0.1 to 0.2 *μ*m) particles. In this work, the X-ray emission spectrometry by SEM showed the presence of Al, Fe, and Si in the precipitates. Therefore, the *α*-phase is present in the aluminum alloy before deformation and persists during ECAP since reflections, with lower intensities, corresponding to this phase are still observed after ECAP (inset of Figure 1(a)).

After ECAP, a pronounced reflection broadening was observed (Figure 1(b)). This is due to grain refinement and enhanced lattice distortions of the processed samples. In addition, the reflection, which was well resolved for the nondeformed sample (), became scarcely visible after ECAP because of the reflection broadening. The cell size and the dislocation density evolutions during ECAP are given in Figure 2. An intensive grain refinement was observed after the ECAP process. In fact, the grain size reached ~200 nm after the two first passes and slightly continued to decrease to attain ~192 nm after four passes. The decrease of the cell size during ECAP was accompanied by a significant increase of the dislocation density. It should be noted that during severe plastic deformation such as ECAP, subgrain boundaries evolve in the grain structures [21] developing areas with coherent crystalline domain (cell structure) [22, 23]. The dislocations distribution may affect the size of these areas.

###### 3.1.2. Microscopic Analysis

After annealing of the as-cast aluminum, at 500°C, OM reveals that the microstructure was heterogeneous and consists of equiaxed coarse grains with an average size of ~80 *μ*m and significantly coarser ones with an average grain size of about 500 *μ*m, due to prolonged annealing (Figure 3).

The SEM analysis gives information about the resulting microstructure of the material before and after ECAP. Before ECAP, SEM observations show that the aluminum matrix contains precipitates located essentially at grain boundaries, even though some precipitates were also observed in the grain interior (Figures 4(a) and 4(b)). As demonstrated by XRD and X-ray emission spectrometry by SEM, these precipitates correspond to the *α*-phase. After ECAP, a heterogeneous microstructure was obtained consisting of ultrafine equiaxed grains and elongated grains (Figures 4(c) and 4(d)). We showed in a previous work [13] that the presence of the *α*-AlFeSi essentially at grain boundaries allowed to reveal the initial shape of the grains and to follow their evolution during ECA pressing by OM; that is, the grains appeared to be elongated in the side face of the sample after ECAP. Therefore, ECAP leads to grain refinement of the aluminum alloy to some extent. Similar trend has been reported in microstructure investigation by transmission electron microscopy (TEM) on high purity aluminum processed by ECAP [24, 25].

In addition to grain refinement and enhanced dislocation density, high strain imposed by ECAP leads to the breakdown (Figure 4(e)) and/or partial dissolution of the *α*-phase particles (Figure 4(f)).

##### 3.2. Corrosion Behavior

When Al contacts with water solution, a rapid hydrated oxide film (AlOOH, also regarded as Al_{2}O_{3}·H_{2}O) will form on the surface. The hydrated passive film formation process is as follows [26]:

Then, the total electrode reaction is
In contact with Cl^{−} containing solution, the film will be attacked, and the anodic dissolution products (AlOHCl, AlOHCl_{2}) having a good water solubility will promote the anodic dissolution of the passive film [27]. Figure 5 shows typical potentiodynamic polarization curves plotted from −1.2 V to 0 V at 10 mV/s for the ECAP’ed ( and 4) and unpressed () Al samples. All samples were immersed in a 3.5 wt% solution for about 3 min at pH = 6.4 before polarization tests to achieve their stable OCP values. A similar shape is observed for the three samples. The more ECAP passes correlate with the nobler corrosion potentials and the higher corrosion current densities . In fact, corrosion current densities of the unpressed () and ECAP’ed samples ( and 4) are equal to about 8 × 10^{−6}, 2 × 10^{−5}, and 4 × 10^{−5} A/cm^{2}, respectively. The values were determined, from the polarization curves, by extrapolation of the linear Tafel plots of the cathodic branches. The results show that the ECAP’ed Al sample () has nobler corrosion potential value but higher and less corrosion resistance when compared with nondeformed () and ECAP’ed (). Therefore, ECAP increased the susceptibility to corrosion of the aluminum alloy. While the value of represents a thermodynamic characteristic of a given metal-electrolyte system [28], the value represents the kinetics of the metal corrosion and reflects more accurately the general corrosion rate than the value of . It is important to note that values of the ECAP’ed samples increased with increasing the ECAP number of passes, and the after 4 passes is of several orders of magnitude higher than that obtained for the nondeformed () sample.

Comparing the cathodic branches controlling the uniform corrosion process for all samples, it can be seen that, while the nondeformed sample shows low cathodic current density , the ECAP’ed sample () exhibits the highest , which is equivalent to corrosion rate. During the positive potential scan, curves do not exhibit active dissolution region near . The lack of active dissolution could be assigned to the hydrated passive films formed on the Al samples. When the potential moves towards more anodic values, narrow anodic plateaus are observed for all samples, indicating formation of a passive layer on the electrode surface, and then the current rises rapidly, denoting destruction of this layer at a pitting potential [29]. It is important to point out that, besides the higher value, the current density of the passive layer increases, and its potential range decreases with ECAP, as a result of the decrease in pitting corrosion resistance for the ECAP’ed samples ( and 4).

Figure 6(a) shows the impedance spectra on Nyquist plots obtained at open circuit potential (OCP) values from the ECAP’ed ( and 4) and nondeformed () Al samples. For all samples, the results of EIS measurements showed that the diameter of the arc, giving the polarization resistance (), exceeds 5 kΩ·cm^{2}. High values indicate that the aluminum forms a relatively stable oxide layer and has an excellent corrosion resistance in the naturally aerated 3.5 wt% NaCl solution. Compared with that of the unpressed sample, the value decreased with increasing ECAP passes; that is, the corrosion resistance decreased with increasing ECAP passes. The adopted Randles equivalent circuit, which is very common for these plots, is illustrated in Figure 6(b). It shows the electrochemical system of metal/oxide layer/electrolyte, where , , and represent the electrolyte resistance, the charge-transfer resistance of corrosion reaction and the interfacial capacitance, respectively. This capacitance contains the contribution of the passive film and the double layer , which are in series. The results of EIS measurements are consistent with those of the Tafel plots since is inversely proportional to and can be obtained from via the Stern-Geary equation [30] given as
where is the corrosion current density, and are the anodic and cathodic Tafel coefficients, respectively, and is the polarization resistance. The Tafel coefficients are generated from the anodic and cathodic branches of the Tafel plots.

The influence of scan rate, (in the range 5–100 mV·s^{−1}), on the potentiodynamic polarization behavior of the unpressed and ECAP’ed samples has been studied in 3.5 wt.% NaCl solution and pH 6.4 (data obtained are not shown herein). It has been shown that the increase in shifts , in all cases, towards more noble values. The variation of with , for the unpressed and ECAP’ed samples, is depicted in Figure 7. A linear relationship is obtained fitting the relation
where and are constants depending on whether the sample was pressed or not. Similar results were obtained for Zn [31], pure Al, and Al-Cu alloys [32]. The linear trend has been explained in terms of incubation time (the time needed for Cl^{−} ions to penetrate the passive film and to reach the metal surface) [33, 34]. At high scan rate, initiation of passivity breakdown occurs only at more positive potentials corresponding to a sufficient short pit incubation time. For all samples, the increase of the scan rate up to 100 mV·s^{−1} leads to the increase of the pitting potential. It is easy to note that increases for all samples in the following order: 4 passes sample < 2 passes sample < nondeformed sample; that is, the pitting corrosion resistance decreases with increasing the ECAP passes.

Typical polarization curves of the ECAP’ed sample () in different NaCl concentrations at pH = 6.4 and scan rate of 10 mV·s^{−1} in the anodic potential domain are shown in Figure 8(a). The curves show that an increase in the chloride concentration produces changes in both the anodic current density and the pitting potential of the sample. Figure 8(b) shows, for the unpressed and ECAP’ed samples, the relation between and logarithm of Cl^{−} concentration (log [Cl^{−}]); straight lines are observed, fitting the following equation:
where and are constants depending on whether the sample was pressed or not. The linear dependence is well established for pure Al [35] and is entirely due to the variation of the solution ohmic drop IR at the pit mouth. These results show that the pitting corrosion depends on NaCl concentration. The increase of NaCl concentration leads to a decrease of the to more negative values accounting for a decreased resistance to pitting corrosion. This resistance increases in the same order as for the effect of scan rate: 4 passes sample < 2 passes sample < nondeformed sample.

Figure 9 displays the corrosion rate variation with the immersion time during testing of the nondeformed and ECAP’ed samples. The corrosion rates of all samples increase with increasing immersion time or with increase of ECAP passes; that is, the 4 passes ECAP’ed sample has much higher corrosion rate than the nondeformed and 2 passes ECAP’ed samples. Also, it should be noted that the corrosion rate of the 4 passes sample is about 4 times higher than the nondeformed sample after immersion for 30 days. This confirms the above results indicating that ECAP leads to the decrease of the corrosion resistance of the aluminum alloy.

#### 4. Discussion

The corrosion behavior of a commercial aluminum alloy processed by ECAP was investigated in NaCl solution using potentiodynamic polarization and immersion tests. Polarization curves showed that the increase of ECAP passes leads, in addition to the increase of weight loss, to higher corrosion current densities and a decrease of pitting corrosion resistance. Also, electrochemical impedance spectra (EIS) tests showed that the polarization resistance decreased with increasing ECAP passes. Therefore, corrosion resistance of the alloy remarkably diminished with increasing the ECAP number of passes. It is not easy to draw a clear conclusion about the reasons for this behavior since many contributions (grain refinement, internal stresses, second phase, etc.) should operate simultaneously. Previous works reported in the literature [36, 37] that grain refinement leads to a high density of grain boundaries which have higher energy than the bulk of the material. This enhances electron diffusion and leads to a more stable passive film and, therefore, to an enhanced corrosion resistance. Controversially, grain refinement may provide more sites to initiate corrosion which enhanced corrosion rate and consequently decreased corrosion resistance. Whether grain refinement is detrimental or not to corrosion resistance could be related to the material nature and environment [7]. It is clear from our results that the grain refinement of the ECAP’ed Al alloy to some extent was accompanied by increased susceptibility to corrosion.

It is well established that internal stresses, especially related to high dislocation accumulation generated by ECAP, may or may not result in the improvement of the corrosion resistance depending on the material [7].

ECAP leads to an intensive grain refinement accompanied by an increased dislocation density. For example, the remaining dislocation densities were equal to 0.25 × 10^{16} and 0.26 × 10^{16} m^{−2} for and 4, respectively. The increase of the dislocation density with the number of ECAP passes could be one of the reasons for decreasing the corrosion resistance of the deformed Al alloy. This is in agreement with the results of Schultze et al. [38].

It is known that severe plastic deformation can lead to the quick decomposition of the Al-based supersaturated solid solution [39, 40]. The start of the decomposition of supersaturated solid solution and formation of nanoprecipitates could be one of the reasons for decreasing the corrosion resistance. However, in the present work, the ECAP process leads to partial dissolution of the *α*-phase. In fact, since there is a large volume of insoluble eutectic constituent present, the formation or dissolution of the *α*-phase cannot be followed by observation of the *α*-phase X-ray reflections. However, a very careful measurement of the aluminum lattice parameter can potentially detect changes in iron solute contents. Thus, a reflection shift to higher 2*θ* angles was observed after ECAP (Figure 1(b)) indicating the decrease of the aluminum lattice parameter during ECAP. For example, the lattice parameter values of the nondeformed () and ECAP’ed () samples are 4.05420 and 4.04957 Å, respectively, corresponding to a relative variation of about −0.11%. The decrease of the lattice parameter is due to partial dissolution of the *α*-phase precipitates since the dissolution of Fe and Si in aluminum matrix decreases the lattice parameter. Indeed, the relative variations of the lattice parameter, , with the concentration, , of both Fe and Si, , are −13.6 [41] and −2.6% [42], respectively. The partial dissolution of the *α*-phase was experimentally supported by SEM investigation (Figure 4(f)). It should be noted that, besides *α*-phase dissolution, oriented strain introduced by the ECAP process could affect the lattice parameter value.

SEM examinations were carried out before and after immersing the nondeformed () and ECAP’ed () Al samples in 3.5 wt.% NaCl solution at pH 6.4 for 30 days. The SEM micrographs (Figures 10(a) and 10(b)) show obvious localized corrosion damage, particularly on 4 passes ECAP’ed sample. Figure 10(a) exhibits relatively small and hemispherical pits with different sizes, grown throughout the surface of the nondeformed sample. Severity of pitting attack is enhanced by ECAP process, which produces, in particular after 4 passes, much larger (~0.5 *μ*m) and deeper rectangular pits. SEM micrograph of Figure 10(c) shows that the *α*-phase particles are the pit initiation sites. So, this attack takes place at the contact between the particles and the Al matrix. In the present work, susceptibility to corrosion results from local galvanic cells formed between the *α*-phase particles and the aluminum matrix. These particles act as cathodes which allowed the reduction of oxygen and drive anodic dissolution of the surrounding matrix. The particles were broken down with the ECAP passes (Figure 4(e)). Consequently, the number of the galvanic cells increases and so is the contact surface between the broken particles and the aluminum matrix. This leads to enhanced dissolution of the matrix which explains the decrease of the corrosion resistance of the aluminum alloy with ECAP passes. This is in agreement with the reported results of Wei et al. [43], which showed that the fragmentation of second phase particles improved localized corrosion behavior in Al-Mn alloys processed by accumulative roll bonding (ARB). Naeini et al. [44] studied the pitting corrosion susceptibility of ultrafine grained 5052 Al alloy (AA 5052) sheets deformed by ARB. They showed that as the ARB number of passes increased, intermetallic Mg and Fe-rich particles were refined so their total surface area increased. Thus, the preferential sites for initiation of pitting corrosion increased. In contrast, Song et al. [45] found that the refinement of Si containing impurities in pure aluminum processed by ECAP reduced the susceptibility of pitting corrosion which is consistent with the ‘small cathode, large anode’ mechanism. Comparable results for AA 1050 aluminum alloy deformed by ECAP have been previously reported [46]. It should be noted that a critical size of particles exists in aluminum alloys below which the particles cannot act as distinct electrochemical entities [47]. For Al-Cu-Mg alloys, this critical size varied between 3 and 8 nm. For the 1100 Al alloy, the particles size was largely higher. Accordingly, it is not possible that a stable protective passive oxide film forms.

#### 5. Conclusion

The effect of ECAP process on the corrosion behavior of a commercial aluminum alloy was investigated in NaCl solution using potentiodynamic polarization and immersion tests. The alloy contains a low volume fraction of *α*-AlFeSi. ECAP leads to an intensive grain refinement of the aluminum alloy to the submicrometer level accompanied by an increased dislocation density. All electrochemical tests confirm that ECAP leads to a significant decrease of the corrosion resistance of the alloy: (i) potentiodynamic curves showed that the more ECAP passes correlate with the higher corrosion current densities and the decrease of pitting corrosion resistance; (ii) electrochemical impedance spectra (EIS) tests showed that the polarization resistance decreased with increasing ECAP passes; (iii) increase of scan rate and NaCl concentration leads to an increase and a decrease of to more positive and negative potentials, respectively. The increase of susceptibility to corrosion results from local galvanic cells formed between the *α*-AlFeSi and the aluminum matrix. The *α*-phase particles act as cathodes which allowed the reduction of oxygen and drive anodic dissolution of the surrounding matrix. The particles were broken down with the ECAP passes which increase the number of the galvanic cells. This leads to enhanced dissolution of the matrix which explains the decrease of the corrosion resistance of the aluminum alloy with ECAP passes.

#### Conflict of Interests

The authors recognized that there is no conflict of interests concerning the results obtained.

#### Acknowledgments

The authors would like to acknowledge Professor N. Njah from the Laboratory of Applied Metallurgy, FSS (Tunisia), and Mr. N. Bouras from the University of Sétif (Algeria) for useful helps.

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