Effect of Grain Refinement on the Dynamic, Mechanical Properties, and Corrosion Behaviour of Al-Mg Alloy

In this investigation, aluminium Al-2.5% Mg cast alloy was modified by adding 0.5 Ti and 0.1 B wt % modifiers to investigate their impact on the dynamic behaviour, as well as the mechanical and microstructure properties. The dynamic properties were analysed experimentally using a free vibration impact test and predicted using finite element methods. This study used a high-resolution polarised optical microscope to analyse the microstructure of the studied alloys and X-ray Powder Diffraction (XRD) analysis to determine the developed phases. Microstructure and mechanical properties were mostly enhanced as a result of grain refining during solidification and through the metal segregation process. The microstructure analysis of the modified alloy showed a significant improvement in the grain refinement; hence, the grains were 10 times finer than the cast alloy. The modified Al-2.5% Mg/Ti-B alloy demonstrated reduced inter-granular corrosion (IGC) than the Al-2.5% Mg standard cast alloy. By incorporating Ti-B modifiers into the composition of the cast Al-Mg alloy, the ultimate tensile strength (UTS), strain (ε), and hardness values (HV) were increased by 30.5%, 100%, and 18.18%, respectively. The dynamic properties of the modified alloy showed an enhancement in the resonant (fn) and damping ratio (ζ) by 7% and 68%, respectively. The predicted resonance frequencies of the investigated alloys showed results close to the experimental dynamic tests.


Introduction
Due to their low weight and high deformability, aluminium alloys are the foundation of the automotive and aerospace industries. These alloys are frequently utilised in the food industry, as well as in automotive and chemical equipment. Moreover, they have high specific strengths and good mechanical properties; thus, they are preferred for ordinary sheet metal and marine applications. The improvement of aluminium alloys may be accomplished by improving their mechanical characteristics; as a result, the use of reinforcing particles and additives becomes increasingly necessary to enhance the performance of aluminium alloys and their composites [1][2][3][4]. Modifying Ti, B, and B 4 C has significantly affected the microstructure of grain refinement [5]. These modifiers play an essential role in reducing grain size and displaying the dendritic structure during manufacturing. Furthermore, they enhance the mechanical properties of the material. However, these dynamic properties have not been investigated in the literature.
As a result, various particles and alloying elements, including Al 2 O 3 , SiC, and TiB 2 , are employed to refine and fine-tune aluminium alloy grains and surface morphology to improve the mechanical characteristics [6,7]. Grain refining can be accomplished using rapid solidification and repeated deformations, dissolving the modifiers using molten metal, lasers, and friction stir processing [8,9]. The first technique depends on the molten metal's melting point and elemental structure and the amount of molten metal present [10,11]. The phase of the matrix may also influence the structure of the refined grain [12]. Furthermore, modifying elements such as titanium and boron have been used as grain refiners in various aluminium alloy series [13,14]. Many researchers have focused on the impact of these components on grain refinement and particle size on mechanical characteristics [15][16][17]. The modifiers enhanced the cast alloy in two ways through grain refinement and decreased porosity during the casting process [18]. Aluminium is an excellent material for manufacturing energy-absorbing structures. The value of the parameters describing the mass-specific energy absorption capacity for aluminium is double that of mild steel and equivalent to steel alloys [19]. The mechanical characteristics of 6082-T6 and 7075-T6 aluminium alloys have been utilised for finite element method (FEM) modelling applications, particularly when dynamic experiments are performed, such as car crashes, explosions, or ballistic strikes [20]. The relationships between erosion and corrosion are complicated, where both processes can either increase material loss or reduce overall wear [21,22]. Even though aluminium has excellent corrosion resistance, the external medium or certain alkalis can dissolve the oxide coating on the metal surfaces, resulting in corrosive metal when this film is damaged. Thus, a significant study was conducted to investigate the impact of corrosion on aluminium alloys [23].
The methods used to identify the dynamic properties of the metals and the role of reinforcement elements to enhance the structural properties were investigated in many works of literature [24,25]. The most simple and accurate method is the free vibration test, which depends on the excitation of the structure to obtain the dynamic properties. As a result of refining the grains, there are many pores and defects in the casting that can be reduced. The internal friction of the materials has long been studied to find suitable damping materials that address or account for environmental and safety concerns. The recent societal focus has been paid to various materials' damping characteristics given new factors for consideration, such as more delicate equipment, eco-friendly machines, and electronic industry needs [26]. The measurement of internal friction behaviour in terms of heat treatment and alloy composition has been used in investigating the relationship between general damping behaviour and internal microstructure, providing a better understanding of the damping mechanism process [27].
Moreover, the grain refiner's presence results in a redistribution of porosity [28,29]. The refined grains significantly affect the dynamic properties of alloys and their composites regarding the impedance of the refined grains of the transmitted excitation source. Fewer investigations have discussed the impact of alloying elements on the dynamic properties [30][31][32]; hence, the effect of refined grains in addition to Al 2 O 3 nanoparticles using friction stir processing showed a significant improvement in the dynamic behaviour [33].
From the previous literature, the researchers' interest in looking for the best quantities of titanium and boron elements developed to refine aluminium grains. It was also clear that only mechanical and apparent properties would explain this improvement without experiencing the effect of such modification on dynamic properties. Therefore, the current work focuses on the effect of grain refinement on the dynamic and mechanical properties by dissolving the Ti-B modifiers into an Al-2.5% Mg cast aluminium alloy. Hence, the primary goal is to find a new relationship between the grain refinement of the modified alloy and its dynamic properties. Furthermore, we investigate the refine action on the corrosion resistance. The FEM, implemented using the ANSYS software, was used to simulate and predict the behaviour of the resonant frequencies that represent the theoretical eigenvalues.

Microstructure and Mechanical Properties Test
The investigated alloys, with chemical compositions listed in Table 1, were melted in a graphite-fireclay crucible (Aug. Gundlach KG, Grossalmerode, Germany) at a temperature of 825 • C using a 5.5 kW Nabertherm resistance furnace(Nabertherm GmbH, Nuremberg, Germany). The melted composition was stirred to homogenise the alloying elements with the base melt alloy, and then, the melted cast was poured into a graphite die. After the casting process, the ingot was annealed at a temperature of 200 • C for three hours to remove the residual stresses that occurred during the casting process. The samples were sectioned and ground via SiC papers with numbers ranging from P320 to P4000; then, it was polished in a 20% water solution of colloidal silica-based suspension. The polished surface was electrically etched at 18 V using a 10% electrolyte solution (saturated solution of H 3 BO 3 in HF) in distilled water. Optical microscopy was used to conduct the microstructural investigation (Olympus PMG Tokyo, Japan). The grain size was measured using the standard linear intercept technique. The average grain size was measured by JMICRO Vision software (JMicroVision 1.3.4, Switzerland) using the average grain intercept (AGI) method. There are three samples chosen from different sections along with the cast alloy to ensure the grains' distribution and refinement. X-ray diffraction (XRD) was conducted with Cu-Kα radiation (Bruker Corp., Billerica, MA, USA) to study the microstructure by the heating/cooling rate of 5 • K/min. In addition to the EDX, elemental analysis was used to identify the participating elements, phases, and construction of the investigated alloy. After the samples were polished and prepared, they were subjected to the hardness test. A Labsys Setaram differential scanning calorimeter (DSC; Setaram Instrumentation, Caluire, France) was used to determine the liquidus and solidus temperatures with a heating rate of 5 K/min. The Vickers hardness test (Zwick/Roell, Kennesaw, GA, USA) was employed to measure the micro-hardness of the samples with a force of 30 N and a dwell duration of 10 s, which was in accordance with the ASTM E-384-17 specifications. Using the ISO 11,846 Method B, the samples were submerged in an aqueous solution comprised of 30 g/L NaCl and ten millilitres per litre concentrated HCl for 24 h to determine intergranular corrosion. The samples were immersed in the solution for 24 h to investigate the influence of the addition of the modifiers TiB on the corrosion behaviour of Al-2.5% Mg aluminium alloys, respectively. Then, the samples were treated with a solution comprised of 15% HNO 3 and 85% distilled water; afterwards, the samples were dried. Next, they were washed in fresh water and dried on a drying rack. Optical microscopy was used to examine the specimens. A Zwick/Roell Z250 Allround series testing machine (ZwickRoell GmbH & Co. KG, Ulm, Germany) was used to perform the tensile tests. Three tensile samples of each alloy were tested, and the average of these three data points was used to get the reported value. The samples had a gauge length and width of 20 mm and 6 mm, respectively, which were performed according to the Russian GOST 1497-84. The dimensions of the samples used in this study are shown in Figure 1. The tensile tests were performed at a constant strain rate of 4 s −1 for all samples.

Microstructure and Mechanical Properties Test
The investigated alloys, with chemical compositions listed in Table 1, were melted in a graphite-fireclay crucible (Aug. Gundlach KG, Grossalmerode, Germany) at a temperature of 825 °C using a 5.5 kW Nabertherm resistance furnace(Nabertherm GmbH, Nuremberg, Germany). The melted composition was stirred to homogenise the alloying elements with the base melt alloy, and then, the melted cast was poured into a graphite die. After the casting process, the ingot was annealed at a temperature of 200 °C for three hours to remove the residual stresses that occurred during the casting process. The samples were sectioned and ground via SiC papers with numbers ranging from P320 to P4000; then, it was polished in a 20% water solution of colloidal silica-based suspension. The polished surface was electrically etched at 18 V using a 10% electrolyte solution (saturated solution of H3BO3 in HF) in distilled water. Optical microscopy was used to conduct the microstructural investigation (Olympus PMG Tokyo, Japan). The grain size was measured using the standard linear intercept technique. The average grain size was measured by JMI-CRO Vision software (JMicroVision 1.3.4, Switzerland) using the average grain intercept (AGI) method. There are three samples chosen from different sections along with the cast alloy to ensure the grains' distribution and refinement.
X-ray diffraction (XRD) was conducted with Cu-Kα radiation (Bruker Corp., Billerica, MA, USA) to study the microstructure by the heating/cooling rate of 5 °K/min. In addition to the EDX, elemental analysis was used to identify the participating elements, phases, and construction of the investigated alloy. After the samples were polished and prepared, they were subjected to the hardness test. A Labsys Setaram differential scanning calorimeter (DSC; Setaram Instrumentation, Caluire, France) was used to determine the liquidus and solidus temperatures with a heating rate of 5 K/min. The Vickers hardness test (Zwick/Roell, Kennesaw, GA, USA) was employed to measure the micro-hardness of the samples with a force of 30 N and a dwell duration of 10 s, which was in accordance with the ASTM E-384-17 specifications. Using the ISO 11,846 Method B, the samples were submerged in an aqueous solution comprised of 30 g/L NaCl and ten millilitres per litre concentrated HCl for 24 h to determine intergranular corrosion. The samples were immersed in the solution for 24 h to investigate the influence of the addition of the modifiers TiB on the corrosion behaviour of Al-2.5% Mg aluminium alloys, respectively. Then, the samples were treated with a solution comprised of 15% HNO3 and 85% distilled water; afterwards, the samples were dried. Next, they were washed in fresh water and dried on a drying rack. Optical microscopy was used to examine the specimens. A Zwick/Roell Z250 Allround series testing machine (ZwickRoell GmbH & Co. KG, Ulm, Germany) was used to perform the tensile tests. Three tensile samples of each alloy were tested, and the average of these three data points was used to get the reported value. The samples had a gauge length and width of 20 mm and 6 mm, respectively, which were performed according to the Russian GOST 1497-84. The dimensions of the samples used in this study are shown in Figure 1. The tensile tests were performed at a constant strain rate of 4 s −1 for all samples.

Determination of the Natural Frequency and Damping Ratio by Experiment
The schematic diagram for the free vibration test is shown in Figure 2. A specific fixture was conducted to support the specimens acting as cantilever beams, and the piezoelectric accelerometer was used to detect the vibration response (Type 4507-B, Bruel & Kjaer, Naeuram, Denmark). An impact hammer exciter equipped with a force transducer (Type 8206, Bruel & Kjaer) was utilised in the excitation process. The vibration signals were gathered using the LAN-XI pulse analyser (type 3050 A-60, Bruel & Kjaer). Pulse Lab Shop software (Bruel & Kjaer) was used to handle the post-processing signal. The fast Fourier transform (FFT) was calculated using a 3200-line resolution and a frequency spread of 10k Hz. Ten data blocks were averaged in a linear mode. The data were averaged over ten tests in order to arrive at proper data. Once the data had been processed, it was examined using MEscope software (Vibrant Technology Inc., Scotts Valley, CA, USA). In the absence of non-destructive test scans, such as radiography or ultrasonic tests, all samples were analysed using an average of five samples for each alloy. A logarithmic decrement, Equations (1) and (2), were used to compute the damping ratio (ζ). The quality factor (Q) is obtained from Equation (3) [24,34]. Figure 3 shows the principal idea in which the logarithmic decrement is calculated from the time-domain graph. Consequently, the damping ratio (ζ) measures how the materials resist the vibratory motion. The variable x o refers to the initial amplitude on the time-domain graph, while x n represents the amplitude of the oscillating wave after n cycles.
where δ = Logarithmic decrement; n = Number of cycles; x o = Initial amplitude at the peak; x n = Amplitude of the peak after n cycles; ζ = Damping ratio; Q = Quality factor.

Determination of the Natural Frequency and Damping Ratio by Experiment
The schematic diagram for the free vibration test is shown in Figure 2. A specific fixture was conducted to support the specimens acting as cantilever beams, and the piezoelectric accelerometer was used to detect the vibration response (Type 4507-B, Bruel & Kjaer, Naeuram, Denmark). An impact hammer exciter equipped with a force transducer (Type 8206, Bruel & Kjaer) was utilised in the excitation process. The vibration signals were gathered using the LAN-XI pulse analyser (type 3050 A-60, Bruel & Kjaer). Pulse Lab Shop software (Bruel & Kjaer) was used to handle the post-processing signal. The fast Fourier transform (FFT) was calculated using a 3200-line resolution and a frequency spread of 10k Hz. Ten data blocks were averaged in a linear mode. The data were averaged over ten tests in order to arrive at proper data. Once the data had been processed, it was examined using MEscope software (Vibrant Technology Inc., Scotts Valley, CA, USA). In the absence of non-destructive test scans, such as radiography or ultrasonic tests, all samples were analysed using an average of five samples for each alloy. A logarithmic decrement, Equations (1) and (2), were used to compute the damping ratio (ζ). The quality factor (Q) is obtained from Equation (3) [24,34]. Figure 3 shows the principal idea in which the logarithmic decrement is calculated from the time-domain graph. Consequently, the damping ratio (ζ) measures how the materials resist the vibratory motion. The variable xo refers to the initial amplitude on the time-domain graph, while xn represents the amplitude of the oscillating wave after n cycles.
where δ = Logarithmic decrement; n = Number of cycles; xo = Initial amplitude at the peak; xn = Amplitude of the peak after n cycles; ζ = Damping ratio; Q = Quality factor.  In order to calculate the mathematical eigenvalue of the natural frequencies, the analytical and mode shapes of the investigated material are obtained from the Euler-Bernoulli equation of the beam by adding boundary conditions to Equation (4); the natural frequency of the beam equation may be simplified using Equation (5): where (A) is the cross-section area of the modelled beam in mm 2 , (E) is the experimental elastic modulus obtained from the tensile test, (I) is the area moment of inertia, (l) is the modelled beam length, and (ρ) is the density of the investigated alloy. In the first, second, and third modes, α = 1.875, 4.694, and 7.854, respectively. Figure 4 shows the optical micrographs of the as-cast investigated alloys, Al-2.5% Mg, and Al-2.5% Mg/TiB. Large grains with a dendritic structure of common alloys were observed in the as-cast Al-2.5% Mg alloy. The average grain size was calculated using the average grain intercept (AGI) method.

Microstructure
The addition of 0.5% Ti and 0.1% B during the casting process resulted in the refinement of the grains and the disappearance of the dendritic structure. The results showed that the modified alloy, Al-2.5% Mg + TiB, had finer grain than the standard alloy by more than 10 times. The average grains size of the Al-2.5% Mg and Al-2.5% Mg/Ti-B alloys are 270 ± 10 µ m and 25.7 ± 3 µ m, respectively. In addition, the grains of Al-2.5% Mg + TiB alloy are equiaxed with an aspect ratio of 1.01. Figure 5 shows the SEM micrographs and the EDS point analysis of the as-cast alloys, Al-2.5% Mg and Al-2.5% Mg/Ti-B. It was observed that the common intermetallic phases were formed in between the dendrite arms of Al-2.5% Mg alloy (Figure 5a,c). Two types of intermetallic particles (Al3Ti and TiB2) develop and disperse in the melt and act as active sites during solidification when Al-Ti-B master alloys are added to the alloys [35]. In order to calculate the mathematical eigenvalue of the natural frequencies, the analytical and mode shapes of the investigated material are obtained from the Euler-Bernoulli equation of the beam by adding boundary conditions to Equation (4); the natural frequency of the beam equation may be simplified using Equation (5): where (A) is the cross-section area of the modelled beam in mm 2 , (E) is the experimental elastic modulus obtained from the tensile test, (I) is the area moment of inertia, (l) is the modelled beam length, and (ρ) is the density of the investigated alloy. In the first, second, and third modes, α = 1.875, 4.694, and 7.854, respectively.

Results and Discussion
3.1. Microstructure Figure 4 shows the optical micrographs of the as-cast investigated alloys, Al-2.5% Mg, and Al-2.5% Mg/TiB. Large grains with a dendritic structure of common alloys were observed in the as-cast Al-2.5% Mg alloy. The average grain size was calculated using the average grain intercept (AGI) method.
The addition of 0.5% Ti and 0.1% B during the casting process resulted in the refinement of the grains and the disappearance of the dendritic structure. The results showed that the modified alloy, Al-2.5% Mg + TiB, had finer grain than the standard alloy by more than 10 times. The average grains size of the Al-2.5% Mg and Al-2.5% Mg/Ti-B alloys are 270 ± 10 µm and 25.7 ± 3 µm, respectively. In addition, the grains of Al-2.5% Mg + TiB alloy are equiaxed with an aspect ratio of 1.01. Figure 5 shows the SEM micrographs and the EDS point analysis of the as-cast alloys, Al-2.5% Mg and Al-2.5% Mg/Ti-B. It was observed that the common intermetallic phases were formed in between the dendrite arms of Al-2.5% Mg alloy (Figure 5a,c). Two types of intermetallic particles (Al 3 Ti and TiB 2 ) develop and disperse in the melt and act as active sites during solidification when Al-Ti-B master alloys are added to the alloys [35].   It was confirmed by X-ray diffraction plots that there were Al3Ti and TiB2 phases present, which function as potential nucleants for the nucleation of the main phase. Regarding an explanation of the improvement in the grain refinement of aluminium alloys caused by the addition of the Al-0.5 Ti-0.1 B master alloy, several theories have described the mechanisms of the refinement and enhanced properties of the modified structures [36][37][38]. Grain refining in aluminium alloys requires the addition of solute atoms and the inclusion of nucleant particles. Consequently, Al3Ti production may be attributed to the grain refinement process of the Al-2.5% Mg alloy caused by the inclusion of the Al-0.5 Ti-0.1 B master alloy. Figure 6 shows the XRD analysis of the investigated alloys. The results revealed that adding 0.5 wt %Ti and 0.1 wt %B resulted in forming TiB2 and Al3Ti aside from the standard phases of Al-2.5% Mg, which act as inclusion centres that lead to finer grains of Al-2.5% Mg + TiB. In addition, these intermetallic phases were formed around   It was confirmed by X-ray diffraction plots that there were Al3Ti and TiB2 phases present, which function as potential nucleants for the nucleation of the main phase. Regarding an explanation of the improvement in the grain refinement of aluminium alloys caused by the addition of the Al-0.5 Ti-0.1 B master alloy, several theories have described the mechanisms of the refinement and enhanced properties of the modified structures [36][37][38]. Grain refining in aluminium alloys requires the addition of solute atoms and the inclusion of nucleant particles. Consequently, Al3Ti production may be attributed to the grain refinement process of the Al-2.5% Mg alloy caused by the inclusion of the Al-0.5 Ti-0.1 B master alloy. Figure 6 shows the XRD analysis of the investigated alloys. The results revealed that adding 0.5 wt %Ti and 0.1 wt %B resulted in forming TiB2 and Al3Ti aside from the standard phases of Al-2.5% Mg, which act as inclusion centres that lead to finer grains of Al-2.5% Mg + TiB. In addition, these intermetallic phases were formed around It was confirmed by X-ray diffraction plots that there were Al 3 Ti and TiB 2 phases present, which function as potential nucleants for the nucleation of the main phase. Regarding an explanation of the improvement in the grain refinement of aluminium alloys caused by the addition of the Al-0.5 Ti-0.1 B master alloy, several theories have described the mechanisms of the refinement and enhanced properties of the modified structures [36][37][38]. Grain refining in aluminium alloys requires the addition of solute atoms and the inclusion of nucleant particles. Consequently, Al 3 Ti production may be attributed to the grain refinement process of the Al-2.5% Mg alloy caused by the inclusion of the Al-0.5 Ti-0.1 B master alloy. Figure 6 shows the XRD analysis of the investigated alloys. The results revealed that adding 0.5 wt %Ti and 0.1 wt %B resulted in forming TiB 2 and Al 3 Ti aside from the standard phases of Al-2.5% Mg, which act as inclusion centres that lead to finer grains of Al-2.5% Mg + TiB. In addition, these intermetallic phases were formed around the grains on the grain boundaries, acting as a barrier to grain growth. Figure 7 shows the DSC analysis of the investigated alloys in order to determine the liquidus and solidus temperatures. The liquidus and solidus temperatures for the Al-2.5% Mg alloy were 651 • C (Figure 7b) and 609 • C (Figure 7a), respectively; whereas the liquidus and solidus temperatures for the Al-2.5%, Mg + TiB alloy were 658 • C (Figure 7b) and 602 • C (Figure 7a), respectively. Solidus temperature was obtained by the heating curve and the liquidus temperature was obtained by the cooling curve. The alloy's solidification temperature range was approximately 42-56 • C. Adding the Ti-B increased the solidification range by 14 • C. The stability was determined to be excellent because of the wide solidification range. the grains on the grain boundaries, acting as a barrier to grain growth. Figure 7 shows the DSC analysis of the investigated alloys in order to determine the liquidus and solidus temperatures. The liquidus and solidus temperatures for the Al-2.5% Mg alloy were 651 °C ( Figure 7b) and 609 °C (Figure 7a), respectively; whereas the liquidus and solidus temperatures for the Al-2.5%, Mg + TiB alloy were 658 °C ( Figure 7b) and 602 °C (Figure 7a), respectively. Solidus temperature was obtained by the heating curve and the liquidus temperature was obtained by the cooling curve. The alloy's solidification temperature range was approximately 42-56 °C. Adding the Ti-B increased the solidification range by 14 °C. The stability was determined to be excellent because of the wide solidification range.   Figure 8 shows the engineering stress-strain curves for as-cast Al-2.5% Mg and modified Al-2.5% Mg/Ti-B alloys. The basic mechanical characteristics of any material are ductility and strength, although these attributes are often specified in opposition to one another in their specifications. Consequently, materials may be ductile or strong, but they are seldom both at the same time. The as-cast sample had a minimum ultimate tensile strength (UTS) and elongation. This was because the as-cast sample had a dendritic structure with coarse and continuous intermetallic compounds. As seen in Figure 8, the refined the grains on the grain boundaries, acting as a barrier to grain growth. Figure 7 shows the DSC analysis of the investigated alloys in order to determine the liquidus and solidus temperatures. The liquidus and solidus temperatures for the Al-2.5% Mg alloy were 651 °C ( Figure 7b) and 609 °C (Figure 7a), respectively; whereas the liquidus and solidus temperatures for the Al-2.5%, Mg + TiB alloy were 658 °C ( Figure 7b) and 602 °C (Figure 7a), respectively. Solidus temperature was obtained by the heating curve and the liquidus temperature was obtained by the cooling curve. The alloy's solidification temperature range was approximately 42-56 °C. Adding the Ti-B increased the solidification range by 14 °C. The stability was determined to be excellent because of the wide solidification range.   Figure 8 shows the engineering stress-strain curves for as-cast Al-2.5% Mg and modified Al-2.5% Mg/Ti-B alloys. The basic mechanical characteristics of any material are ductility and strength, although these attributes are often specified in opposition to one another in their specifications. Consequently, materials may be ductile or strong, but they are seldom both at the same time. The as-cast sample had a minimum ultimate tensile strength (UTS) and elongation. This was because the as-cast sample had a dendritic structure with coarse and continuous intermetallic compounds. As seen in Figure 8, the refined  Figure 8 shows the engineering stress-strain curves for as-cast Al-2.5% Mg and modified Al-2.5% Mg/Ti-B alloys. The basic mechanical characteristics of any material are ductility and strength, although these attributes are often specified in opposition to one another in their specifications. Consequently, materials may be ductile or strong, but they are seldom both at the same time. The as-cast sample had a minimum ultimate tensile strength (UTS) and elongation. This was because the as-cast sample had a dendritic structure with coarse and continuous intermetallic compounds. As seen in Figure 8, the refined grains of the modified Al-2.5% Mg/Ti-B alloy enhanced both the tensile strength and the elongation of the alloy. The optimal amount of grain refiners enhanced the tensile strength and elongation of the alloys' fracture. The main cause for this improvement is most likely owing to the alloy's reduced grain size, which results in a finer distribution of second phases (i.e., intermetallics). Table 2 summarises the mechanical properties of the investigated alloy. The sample's ultimate tensile strength and elongation were increased from 156 MPa (for the as-cast sample) to 205 MPa (modified alloy using Ti-B modifiers). The elongation of the modified Al-2.5% Mg/Ti-B alloy samples was about 100% more than that of the as-cast sample. With the inclusion of Ti-B modifier elements, it was clear that the refined grain alloy displayed greater elongation. The yield strength of the modified alloy was insignificantly enhanced by adding Ti-B compared to the standard alloy. The increase in the yield strength was 5 MPa, while the increase in the ultimate tensile strength was 40 MPa. In the same manner, the Young's modulus was increased by 4 GPa. Generally, the overall enhancement in the mechanical properties was satisfactory, which underlies this alloy's wide use in many industrial applications. grains of the modified Al-2.5% Mg/Ti-B alloy enhanced both the tensile strength and the elongation of the alloy. The optimal amount of grain refiners enhanced the tensile strength and elongation of the alloys' fracture. The main cause for this improvement is most likely owing to the alloy's reduced grain size, which results in a finer distribution of second phases (i.e., intermetallics). Table 2 summarises the mechanical properties of the investigated alloy. The sample's ultimate tensile strength and elongation were increased from 156 MPa (for the as-cast sample) to 205 MPa (modified alloy using Ti-B modifiers). The elongation of the modified Al-2.5% Mg/Ti-B alloy samples was about 100% more than that of the as-cast sample. With the inclusion of Ti-B modifier elements, it was clear that the refined grain alloy displayed greater elongation. The yield strength of the modified alloy was insignificantly enhanced by adding Ti-B compared to the standard alloy. The increase in the yield strength was 5 MPa, while the increase in the ultimate tensile strength was 40 MPa. In the same manner, the Young's modulus was increased by 4 GPa. Generally, the overall enhancement in the mechanical properties was satisfactory, which underlies this alloy's wide use in many industrial applications.

Hardness Evaluation
Hardness is considered to be a good indicator for the other mechanical properties. Figure 9 shows the Vickers hardness results of the investigated alloys. Interestingly, the improved Al-2.5% Mg/TiB alloy had a Vickers hardness of about 67 HV, which is roughly 18% higher than the as-cast alloy (55 HV). The intermetallic compounds (ICs) are thought to have a significant effect on the properties of the modified alloy [39]. This is primarily due to Ti and B reacting at higher temperatures during the casting process to produce intermetallic compounds. These intermetallic compounds (Al3Ti, TiB2, etc.) have significantly higher hardness, resulting in a considerable increase in hardness at the Al-Mg interface. The results revealed that the hardness was increased by adding 0.5 Ti + 0.1 B due

Hardness Evaluation
Hardness is considered to be a good indicator for the other mechanical properties. Figure 9 shows the Vickers hardness results of the investigated alloys. Interestingly, the improved Al-2.5% Mg/TiB alloy had a Vickers hardness of about 67 HV, which is roughly 18% higher than the as-cast alloy (55 HV). The intermetallic compounds (ICs) are thought to have a significant effect on the properties of the modified alloy [39]. This is primarily due to Ti and B reacting at higher temperatures during the casting process to produce intermetallic compounds. These intermetallic compounds (Al 3 Ti, TiB 2 , etc.) have significantly higher hardness, resulting in a considerable increase in hardness at the Al-Mg interface. The results revealed that the hardness was increased by adding 0.5 Ti + 0.1 B due to the formed intermetallic phases and the refined structure. As a result, plastic deformation becomes more difficult, eventually increasing hardness at the bonding interface. Furthermore, the distribution and quantity of intermetallic compounds in Al-Mg alloy materials may be relevant. to the formed intermetallic phases and the refined structure. As a result, plastic deformation becomes more difficult, eventually increasing hardness at the bonding interface. Furthermore, the distribution and quantity of intermetallic compounds in Al-Mg alloy materials may be relevant.

Corrosion
Intergranular corrosion (IGC) occurs when the electrochemical potential difference between an alloy's intermetallic components corrodes the intergranular component. The samples were cut into parts with dimensions of 25 × 15 × 2 mm 3 , and subsequently ground to 2400 level grit and finally polished and captured. The main aim of the IGC test is to show the effect of grain refining on the corrosion behaviour, so the samples were visually examined. This type of corrosion is developed on the grain boundaries and does not cause significant damage to the grains themselves. IGC can take on various forms depending on the alloying elements and heat treatment used. Intergranular corrosion infiltrates more rapidly than pitting corrosion, although it eventually reaches a depth that is self-limiting in its penetration. Even though aluminium-magnesium alloy containing less than 3% Mg has excellent corrosion resistance, the high proportion of Mg causes intergranular corrosion during the joining process or as a result of surface modification methods. According to the results, the IGC rate in the as-cast sample rose due to the dendritic structure of the grains and their large size. Hence, the precipitates at the grain boundaries significantly impacted the corrosion rate [13,40]. Figure 10 represents a micrograph of the studied alloys taken immediately after 24 h of immersion in the solution without any surface preparation. The results revealed that the intergranular corrosion began as tiny pits and spread quickly throughout the intergranular pathways (Figure 10a,b). In contrast, the modified Al-2.5% Mg/Ti-B alloy exhibited improved corrosion resistance owing to the Ti-B addition (Figure 10c,d).

Corrosion
Intergranular corrosion (IGC) occurs when the electrochemical potential difference between an alloy's intermetallic components corrodes the intergranular component. The samples were cut into parts with dimensions of 25 × 15 × 2 mm 3 , and subsequently ground to 2400 level grit and finally polished and captured. The main aim of the IGC test is to show the effect of grain refining on the corrosion behaviour, so the samples were visually examined. This type of corrosion is developed on the grain boundaries and does not cause significant damage to the grains themselves. IGC can take on various forms depending on the alloying elements and heat treatment used. Intergranular corrosion infiltrates more rapidly than pitting corrosion, although it eventually reaches a depth that is self-limiting in its penetration. Even though aluminium-magnesium alloy containing less than 3% Mg has excellent corrosion resistance, the high proportion of Mg causes intergranular corrosion during the joining process or as a result of surface modification methods. According to the results, the IGC rate in the as-cast sample rose due to the dendritic structure of the grains and their large size. Hence, the precipitates at the grain boundaries significantly impacted the corrosion rate [13,40]. Figure 10 represents a micrograph of the studied alloys taken immediately after 24 h of immersion in the solution without any surface preparation. The results revealed that the intergranular corrosion began as tiny pits and spread quickly throughout the intergranular pathways (Figure 10a,b). In contrast, the modified Al-2.5% Mg/Ti-B alloy exhibited improved corrosion resistance owing to the Ti-B addition (Figure 10c,d).  Figure 11 shows the simulated resonant of the first three modes; however, the resonant frequencies were high due to the dimension of the sample and the closeness of the values between both investigated cases. The simulated frequency response function (FRF) is considered the main parameter worth studying due to its importance in structural applications. Hence, the harmonic response behaviour is built on the modal analysis in the simulation module. The simulated standard alloy showed less resonant frequency at the first three mode shapes than the modified alloy by 43 Hz, 69 Hz, and 278.2 Hz, respectively, as demonstrated in Table 3. The predicted natural frequency of the modified alloy increased by a fixed rate of 3.17% more than the standard alloy. The simulated results revealed that the resonance frequencies at higher modes increased for the modified alloy; hence, this improvement leads to stability when exposed to a high excitation source. This result matched the experimental free vibration test, as shown in Figure 12. The experimental natural frequency at the first mode of the standard alloy showed a value larger than the numerical value by only 14 Hz. While the modified alloy showed a variation of 28 Hz for the numerical model, these values reveal the closeness between the measured frequency and the theoretical values. Therefore, improvement in the mechanical properties leads to enhancing the dynamic properties via increasing the natural frequency. Moreover, the high damping capacity of the metal leads to a rise in the safety rate in marine and vehicle industries.  Figure 11 shows the simulated resonant of the first three modes; however, the resonant frequencies were high due to the dimension of the sample and the closeness of the values between both investigated cases. The simulated frequency response function (FRF) is considered the main parameter worth studying due to its importance in structural applications. Hence, the harmonic response behaviour is built on the modal analysis in the simulation module. The simulated standard alloy showed less resonant frequency at the first three mode shapes than the modified alloy by 43 Hz, 69 Hz, and 278.2 Hz, respectively, as demonstrated in Table 3. The predicted natural frequency of the modified alloy increased by a fixed rate of 3.17% more than the standard alloy. The simulated results revealed that the resonance frequencies at higher modes increased for the modified alloy; hence, this improvement leads to stability when exposed to a high excitation source. This result matched the experimental free vibration test, as shown in Figure 12. The experimental natural frequency at the first mode of the standard alloy showed a value larger than the numerical value by only 14 Hz. While the modified alloy showed a variation of 28 Hz for the numerical model, these values reveal the closeness between the measured frequency and the theoretical values. Therefore, improvement in the mechanical properties leads to enhancing the dynamic properties via increasing the natural frequency. Moreover, the high damping capacity of the metal leads to a rise in the safety rate in marine and vehicle industries.

Dynamic Characteristics
The as-cast Al-2.5% Mg alloy showed a natural frequency lower than the modified alloy containing Ti-B modifiers. The experimental free vibration test showed the time decay curves of both conditions; Figure 13a shows a long-time response for the as-cast Al-2.5% Mg alloy, while the modified alloy showed less time decay. Changes in the microstructure and size of refined grains can explain the difference in the time response in each case. As the mechanical properties were enhanced, the dynamic properties also improved due to increasing the first-mode resonant frequency. Figure 12 shows an increase in the natural frequency of the modified Al-2.5% Mg alloy by 7%. The damping ratio (ζ) of the standard Al-2.5% Mg alloy was 3.28 ± 0.0029%, whereas the modified Al-2.5% Mg alloy Ti-B was 5.61 ± 0036%. The values were consistent with the damping cross-references [41]. The refined grains played an essential role in the dynamic properties-that is, the existence of the extra grain boundaries impeded the exciting vibration waves when transmitted from one grain to another [33]. Table 4 shows the dynamic characterisation of the investigated alloys. The quality factor (Q) provides a more reliable indication of the dynamic properties of the structure. When an external force is applied to a resonator, the Q factor is described as the resonator's centre frequency ratio to its bandwidth. A higher Q indicates a slower rate of energy loss and slower decay of oscillations. Figure 11. (a) First mode shape; (b) second mode shape; (c) third mode shape simulation analysis of the standard Al-2.5% Mg alloy; and (d) simulation of modal analysis for the studied alloys using FRF representation.    Table 5. Comparison of the theoretical value of the first mode resonance frequency and the experimentally measured value.  Resonant frequency employing the mathematical equation was used to validate the natural frequency value obtained from the experimental results. Table 5 shows the comparison between the two methods; hence, the mathematical formula in Equation (5) was used to calculate the theoretical value of the first resonance mode only. The experimental resonance frequencies were closed to the theoretical values; thus, it was considered an indicator of the validity of the laboratory results. On the other hand, knowing the theoretical resonance value that depends on the mechanical properties can help predict the damping capacity by adapting their parameters using FEM analysis in future work.

Conclusions
In this study, standard Al-2.5% Mg cast alloy was modified using Ti-B modifier elements; the following results were concluded from this investigation.
The presence of titanium and boron in Al-Mg alloys produced excellent grain refinement that causes an improvement in the mechanical properties: thus, the enhancement in tensile strength by 30.5% and elongation by 100%. On the other hand, there was a slight enhancement in the hardness behaviour of the modified Al-2.5% Mg/TiB alloy due to the formation of intermetallic phases.
The standard Al-2.5% Mg cast alloy showed intergranular corrosion that started in tiny pits and soon expanded across the dendritic grain boundaries. The modified Al-2.5% Mg/Ti-B alloy exhibited improved corrosion resistance owing to the refined and minimised grain structure.
The modified alloy's dynamic properties were improved because increasing the number of grain boundaries helps absorb the amplitude of the propagated waves passing through these grains. However, there is no significant change in the resonance frequency, which is increased by 6.9% than the standard alloy.
The recommendation for further work is to study the distribution of the refined grains caused by the modifier's elements on the fabricated cast and their influence on the manufacturing process.