**1. Introduction**

A lightweight and high-performance armor protection structure has always been an important goal of research on modern protection technology, as its lightweight and high ballistic performance can help ensure the mobility of military weapons, while reaching the protection goal [1,2]. Ceramic materials have lower densities than metal materials, as well as high hardness and compressive strength and are widely used in lightweight and highperformance armor [3–5]. On the other hand, because of the brittleness and low tensile strength of ceramics, they cannot absorb a large amount of energy in the penetration process. So, in practical applications, ceramic is usually used as the front plate and metal or fiberreinforced composite as the back plate, so that ceramic/metal or ceramic/composite material armor can be developed with improved ballistic performance [6]. In the process of projectile penetrating ceramic composite armor, the ceramic material first blunts and erodes the projectile to dissipate energy, and then the composite back plate absorbs the remaining kinetic energy to prevent projectile penetration [7,8]. Therefore, ceramic composite armor has a wide range of applications because of its high protection coefficient and good ballistic performance.

The conventional ceramic composite armor has good anti-penetration performance, but as projectiles have increasingly stronger penetration capabilities, to achieve the protection goal, the armor needs to have a larger mass and size. In practice, the ballistic impact

**Citation:** Jiang, A.; Li, Y.; Li, D.; Hou, H. Study on Anti-Penetration Performance of Semi-Cylindrical Ceramic Composite Armor against 12.7 mm API Projectile. *Crystals* **2022**, *12*, 1343. https://doi.org/10.3390/ cryst12101343

Academic Editors: Tomasz Sadowski and Vladislav V. Kharton

Received: 21 August 2022 Accepted: 17 September 2022 Published: 22 September 2022

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**Copyright:** © 2022 by the authors. Licensee MDPI, Basel, Switzerland. This article is an open access article distributed under the terms and conditions of the Creative Commons Attribution (CC BY) license (https:// creativecommons.org/licenses/by/ 4.0/).

on the armor is not perpendicular to its surface [9]. Therefore, researchers have carried out extensive research on the oblique penetration into the ceramic composite armor. It is found that when the projectile penetrates the ceramic composite armor with a non-ideal attitude, the projectile axis deviates from its initial impact angle under the action of the deflection moment because the axis of the projectile does not coincide with the normal line of the ceramic plate [10]. If the penetration angle keeps increasing, projectile ricochet may happen. In addition, the increase in penetration angle also leads to the increase in the effective target thickness during projectile penetration, and projectile deflection and yaw occur, making the penetration path of the projectile longer. The longer the interaction between the projectile and the ceramic armor lasts, the greater the erosion of the projectile [11] and the break-up degree of the ceramic [12], resulting in more kinetic energy dissipation [13]. In the study on the oblique penetration of the long-rod projectile into the ceramic composite armor, it has been also found that oblique penetration makes the dwell time of the long-rod projectile on the interface longer compared with vertical penetration [14]. These factors finally lead to a faster decline in projectile velocity [15], a reduction in penetration depth [16], an increase in the ballistic limit of the armor, and a significant improvement in the anti-penetration performance under the condition of oblique penetration into the ceramic composite armor.

In practical applications, such as personal protective equipment and other usage scenarios with space limitations, when the conditions do not allow the ceramic composite armor to be placed obliquely, by designing specially shaped ceramics to cover the armor surface [17] or be set inside the armor [18], the nominal normal penetration can be transformed into the actual local oblique penetration, penetration with an angle of attack or a combination of the two.

In terms of realizing the ceramic slope, S. Stanislawek [19] designed a pyramidal ceramic armor. The results showed that when the pyramids had large dimensions compared with the projectile and the impact point of the projectile was situated on the pyramid side wall, projectile turning could be especially observed, but the energy dissipation capacity of the composite armor was weaker than that of the homogeneous ceramic composite armor with equal mass. In addition, there was an obvious weak point where the pyramids adjoined, and the pyramid top was the tip of the inclined section that should be avoided, as pointed out in Ref. [15]. Based on Cohen. M's patent [20], W. L. Liu [21] carried out a study on a specially shaped ceramic composite armor with a hemispherical top and a cylindrical lower part. Compared with planar ceramics, closely arranged ceramic cylinders can transfer energy to the surrounding ceramic cylinders, and can also greatly dissipate the projectile's energy through break-up. However, it is obvious that with such a design, gaps exist between the adjacent ceramic cylinders, which may lead to anti-penetration performance reduction. J. M. Chen [22] improved the above-mentioned specially shaped ceramics by cutting the congruen<sup>t</sup> circles of the cylinder into regular hexagons, so that there can be no gap between each ceramic unit. However, this also brings more seams to the whole composite armor, and the decreased ballistic performance at the seams leads to more weak areas in the improved protective structure. The positive side of the above structure is that, due to the included angle between the projectile and the ceramic surface, the projectile is subject to the longitudinal and lateral resistances that unevenly vary in size and direction. This leads to ballistic deviation, serious deformation and damage to the projectile, thus improving the ballistic performance of the ceramic plate. M. Aydin [23] and R.Z. Shao [24] proposed a protective structure using ceramic balls, which provide a large number of slopes. Unlike the fixed-shaped ceramics, the reason for the deflection, yaw and fracture of the projectile against this type of ceramic armor is the rotation, movement and brittle fracture of the ceramic balls under impact loading. In addition, under this concept, the ceramic balls that break after each impact will soon be replaced by the adjacent new balls. Therefore, the armor can continuously resist multiple rounds of impact loads, without removing the damaged ceramic balls. The authors called this armor design "self-healing armor".

Based on the advantages and disadvantages of the above-mentioned specially shaped ceramics, this paper proposes a ceramic composite armor, which is mainly divided into

the following two parts: specially shaped ceramic and metal back plate. Through ballistic impact experiments combined with FEM (finite element method) and SPH (smooth particle hydrodynamics) numerical calculations, the anti-penetration performance of the composite armor structure against the 12.7 mm API projectile is mainly studied; at the same time, the penetration and deflection processes of the projectile, the deformation and failure mode of the metal back plate are analyzed.

#### **2. Experimental and Numerical Methods**

#### *2.1. Experimental Design*

#### 2.1.1. Projectile and Target Plate

In the experiment, a 12.7 mm API projectile with a steel core coated with a copper sheath was used, with a diameter of 10.8 mm, a core length of 52 mm, and a weight of 30 g. The total weight of the core and the copper shell is about 48 g. The material of the core is T12A steel [25,26]. The target plate is divided into three parts, which are the specially shaped ceramic, the back plate, and the steel frame around the ceramic (see Figure 1). In the experiment, the diameter of the semi-cylindrical body selected in the experiment is 24 mm to ensure that the specially shaped ceramics play a deflection role, and, at the same time, to avoid obvious weak areas in the structure due to the non-uniformity of the ceramics, a 6 mm rectangular body of ceramics is set under the semi-cylindrical ceramic column to form specially shaped ceramic composed of semi-cylindrical and rectangular plates. Two materials of boron carbide and silicon carbide were selected for the ceramics. The back plate is 4 mm thick 12MnCrNi steel. The ceramic is surrounded by steel frames of equal height to constrain its displacement. Among them, the forming process of boron carbide and silicon carbide and the main mechanical properties of boron carbide, silicon carbide, and 12MnCrNi steel can be found in the literature [27].

**Figure 1.** Schematic diagram of composite armor, (**a**) SiC Ceramic composite armor, (**b**) B4C Ceramic composite armor.

#### 2.1.2. Experimental Setup and Brief Results

Ballistic impact experiments were carried out to analyze the ballistic performance of the composite armor. The experimental arrangemen<sup>t</sup> is shown in Figure 2, which is mainly composed of a ballistic gun, laser velocity measurement system, support and target network velocity measurement system. In the experiment, the 12.7 mm API projectile was launched by the 12.7 mm ballistic gun, and the amount of gunpowder fired determined the projectile's velocity. We used the laser velocity measurement system to measure the initial velocity of the projectile, and used the target net velocity measurement system to

measure the residual velocity of the projectile after passing through the target plate. A high-speed camera was set up at a distance of about 1 m from the right side of the target plate to observe the impact point and attitude of the projectile before hitting the target plate. The height was about the same as the trajectory, and the shooting rate was 62,000 frames /s. At the same time, the grid paper is arranged on the left side of the flight trajectory of the projectile. Perpendicular to the target plate, the grid drawn on the surface is 20 mm square. It is convenient to judge the position and flight attitude of the projectile body. The coordinate system in the experiment and numerical calculation is shown in Figure 2, where the origin of the coordinate system is the center point of the ceramic bottom surface.

**Figure 2.** Experiment setup.

Four experimental tests were conducted. Figure 3 presents several high-speed photographs of the projectile before impacting the target under different working conditions. The numbering rules in the figure are as follows: the photo of the first frame when the projectile completely comes into view is photo No. 1, and then the photo of each subsequent frame is numbered in sequence. As can be observed from the figure, in Experiment 1, the projectile has an initial oblique angle of about 3.3◦; in Experiment 2, the projectile has an initial angle of attack of about 4.8◦; in Experiment 3 and 4, the projectile has an initial oblique angle of about 1.5◦. As shown in Figure 4, the impact point of this paper is defined as follows: the intersection of the extension line of the velocity direction of the center of mass of the projectile and the surface of the composite armor. In the high-speed camera image, it can be observed that several white lines are drawn on the target plate parallel to the edge of the armor, and their positions are located at the joint of the two cylinders. According to the high-speed camera results, the impact points of the projectiles in the four experiments can be determined. The brief experimental results are shown in Table 1.

#### *2.2. Numerical Model and Effectiveness Verification*

#### 2.2.1. Numerical Model

An adaptive coupling algorithm based on FEM and SPH in LS-DYNA [28] was adopted as the numerical model in this study. ERODING\_SURFACE\_TO\_SURFACE contact is defined between every two components. The contact algorithm AUTOMATIC\_SURFACE\_TO\_ SURFACE\_TIEBREA is employed to simulate the adhesion between the semi-cylindrical ceramic and the steel back plate, where NFLS and SFLS parameters are set to 20 MPa according to the adhesive strength provided by the manufacturer. Clamping constraints are applied to the steel back plate and the side of the rectangular plate in the specially shaped ceramic.

As shown in Figure 5, all components are modeled by a hexahedral solid element. During projectile penetration into the composite armor, the penetration effect is small due to the rapid separation of the jacket from the projectile core, so the core produces the main penetration effect [29]. Therefore, only the penetration effect of the core on the composite armor is considered in the numerical calculation [30], with a mesh size of about 0.735 mm. The mesh size of the semi-cylindrical ceramic is 0.75 mm in the radial and length directions, (**a**) (**b**) (**c**) (**d**) 

and the other parts continue to match it. The mesh size of the back plate and the rectangular plate of the ceramic is 0.75 mm.

**Figure 3.** High-speed photographs of impact points, (**a**) Experiment 1, (**b**) Experiment 2, (**c**) Experiment 3, (**d**) Experiment 4.

**Figure 4.** Schematic diagram of impact points in the case of normal penetration, oblique angle, and angle of attack. (**a**) Impact point in the case of normal penetration; (**b**) impact point in the case of oblique angle *θ*; (**c**) impact point in the case of angle of attack *α*.

**Table 1.** Brief experimental results.


**Figure 5.** Finite element model.

The constitutive model of B4C, SiC ceramics using the JH-2 model, metal using the Cowper–Symonds model, the introduction of two constitutive models and the detailed material parameters of B4C, SiC ceramics and 12MnCrNi can be observed in the literature [27]. According to Refs. [31–33], among the material parameters of T12A steel, those related to the strain rate effect is set to 0, that is, the strain rate effect is not considered. So, the strain rate effect of T12A steel is not considered either in the numerical model in this paper, and the strain rate parameters SRC and SRP in LS-DYNA are set to 0 as well. The detailed material parameters are shown in Table 2.

**Table 2.** Cowper–Symonds parameters of T12A steel, adapted from Refs. [31,32].


2.2.2. Verification of Calculation Results

The numerical calculation is performed according to the initial projectile velocities and impact points captured by the high-speed camera in the experiments, and the residual velocities of the projectile calculated by the numerical calculation are compared with the value measured by the experiment. As shown in Table 3, in the three working conditions with residual velocity records, the maximum deviation of the residual projectile velocity is 11.11%, showing good agreemen<sup>t</sup> between the two methods.


**Table 3.** Comparison of experimental and numerically calculated residual velocities.

The damage morphology of the steel back plate after the experiments is compared with that in the numerical calculation, and the experimental and numerical results are basically consistent. As shown in Figure 6, in Experiment 1, at T = 140 μs, four approximately vertical cracks appear in the back plate in the numerical calculation. In the final numerical and experimental results, the petaling part of the back plate can be divided into four regions, and each region is separated by cracks. As shown in Figure 7, in Experiment 3, elliptical breaches occur in both the experiment and numerical calculation; two shorter cracks appear near the short axis of the elliptical breaches, and meanwhile, in the direction of the long axis of the elliptical breaches, an outwardly rolled long petal appears on one side and a shorter petal on the other side. As shown in Figure 8, in Experiment 4, the back plate is not damaged in the experiment and numerical calculation, only the bulging-dishing deformation occurs, which has the following features: a relatively prominent bulge has formed at the vertex of the deformation, and the profile of the dishing deformation regions on both sides of the bulge is approximately straight.

**Figure 6.** Comparison of back plate damage morphology of in Experiment 1.

**Figure 7.** Comparison of back plate damage morphology in Experiment 3.

**Figure 8.** Comparison of back plate damage morphology in Experiment 4.

### *2.3. Working Conditions*

To study the anti-penetration performance of the semi-cylindrical ceramic composite armor, this article adopts the method of combining experiment and numerical calculations to carry out research on 34 working conditions (Table 4). Specifically, working conditions No. 1–4 are the comparison and verification groups for the experimental and numerical methods; in working conditions, No. 5–17, only the impact point changes and the other conditions are kept unchanged. With a spacing of 1 mm, 13 impact points are selected successively from the top of the semi-cylinder to the seam (Figure 9). The impact point deviation degree *η* is used to represent the position of the impact point. At the top of the semi-cylinder, the impact point deviation degree is defined as *η* = 0, at the seam of the semi-cylinder, it is defined as *η* = 1, and at other positions, *η* = *d*/*R*, where *d* is the distance between the impact point and a point on the top of the nearest semi-cylinder, and *R* is the radius of the semi-cylindrical ceramic. In working conditions No. 18–29, only the semi-cylinder diameter and the impact point deviation degree *η* vary and the other conditions remain unchanged. To make the results comparable, the bottom surface area

of the four semi-cylindrical ceramics with different diameters is 120 × 60 mm2, and the volume is about 1.11 × 10<sup>5</sup> mm3, i.e., the average areal density in this area is kept the same, and its geometric dimensions are given in Figure 10. The ratio of semi-cylindrical ceramic diameter to core diameter is represented by *ξ*, whose values are 0.56, 1.11, 2.22 and 2.78 for the four composite armors. In working condition No. 30, a homogeneous ceramic composite armor with equal mass is used, the areal density of the ceramic and the metal back plate remain unchanged, and a planar structure is adopted, which is for comparative analysis. In working conditions No. 31–34, only the initial velocity of the projectile varies and the other conditions remain unchanged.

**Figure 9.** Impact point distribution.

**Figure 10.** Schematic diagram of the cross-section of composite armors with different ratios of semi-cylindrical ceramic diameter to core diameter under equal areal density.


**Table 4.** Working conditions for calculation.

#### **3. Results and Analysis**

#### *3.1. Analysis of Penetration Process*

In order to better reveal the penetration process of the 12.7 mm API projectile into the ceramic composite armor, the penetration process of the projectile body under working condition 11 (*η* = 0.5) is analyzed. Figure 11 shows the velocity–time–history curve of the projectile. For the convenience of analysis, the lateral and vertical acceleration time–history curves of the projectile and three typical process pictures are also added in the velocity– time–history curve. According to Figure 11, the penetration process can be divided into the following four stages: asymmetric erosion of the projectile, ceramic cone squeezing movement, back plate failure and projectile exit.

In the asymmetric erosion stage, when the projectile hits the ceramic, the tip part of the projectile head rapidly breaks, and the ogive nose head characteristics of the projectile body gradually disappear. At the same time, due to the semi-cylindrical surface of the ceramic, the erosion failure of the projectile is asymmetric, the length of the projectile is greatly eroded, and the velocity of the projectile decreases greatly. The projectile penetrates further into the ceramic, and cracks and fragments appear in the ceramic and form ceramic cones. During the formation of ceramic cones, the vertical force of the projectile core increases sharply. At this stage, the back plate has not been squeezed by the ceramic cone, and the back plate almost has no deformation. The duration of this stage is denoted as *t*1.

In the phase of the ceramic cone squeezing movement, the projectile penetrates further into the ceramic interior, and the asymmetric erosion failure degree of the warhead decreases. When the projectile extrudes the ceramic cone, the particles in the cone are accelerated and crushed continuously, and the diameter and thickness of the bottom of the ceramic cone become smaller and smaller. The vertical force of the projectile core starts to decrease. The projectile compresses the ceramic cone and acts on the back plate, which starts to produce local bulging deformation. When the velocity of the remaining ceramic cone reaches the velocity of the projectile, the remaining ceramic crushing cone moves with the projectile at the same speed, and the ceramic cone stops being abrasive on the projectile, and the vertical force of the projectile core continues to decrease. The plastic deformation of the back plate expands, and when the deformation of the plastic bulge area reaches a certain degree, the back plate begins to undergo tensile failure. The duration of this stage is denoted as *t*2.

In the failure stage of the back plate, the projectile penetrates further. Due to the failure of the back plate, the vertical force of the projectile decreases greatly, and the velocity decrease rate decreases greatly. The left and right sides of the projectile head touch the back plate successively. At this time, the projectile has a large deflection, and the contact area between the right side of the projectile and the back plate is large, so that the velocity of the projectile decreases and the "secondary deceleration" begins. The duration of this phase is denoted as *t*3.

In the phase of projectile exit, after the projectile exits out of the back plate, the attitude of the projectile is greatly deflected compared with the incident, and the velocity direction of the projectile is also changed.

When the deviation degree of the impact point changes, the penetration process will be partially different. When the deviation of the impact point is close to 0 or 1, the degree of asymmetric erosion in the first stage of the penetration process will be significantly reduced. As a result, the attitude deflection of the projectile is small during the penetration process, and the secondary deceleration process is not obvious during the penetration process of the projectile. The whole penetration process is similar to that of homogeneous ceramic composite armor.

The projectile deflection process in this study is similar to that reported in the literature [27], but in the process of projectile penetration, due to the ogive nose of the projectile head, the contact area between the projectile head and the ceramic is large at the initial moment when the projectile hits the ceramic. This allows the projectile to deflect slightly more than the flat-ended rod projectile in the first stage. In the next penetration stage, the rapid erosion failure oval head did not play a significant role. In addition, because the 12.7 mm API projectile has a long body and a relatively low velocity, the contact area between the projectile and the back plate was large for a long time in the failure stage of the back plate. As a result, the negative angular acceleration of the projectile at this stage was large, the angular velocity of the projectile decreased to a negative value, the deflection angle of the projectile decreased to 0, and then the inverse direction increased.

#### *3.2. Backplate Failure Mode Analysis*

As the 12.7 mm API projectile penetrates the ceramic part, the geometric characteristics of the ogive nose of the projectile have been completely destroyed, and the damaged nose becomes similar to that of the flat-nosed projectile. However, during the projectile penetration into the semi-cylindrical ceramic composite armor, the ceramic in front of the projectile is broken and a ceramic cone is formed; the projectile squeezes the ceramic cone to move forward, causing bulging deformation in a large area of the back plate around the projectile nose. Such an impact response is similar to that of an ogive-nosed projectile perforating a thin plate armor at a low velocity. During the penetration, at the impact center, the tensile deformation of the back plate increases sharply as it is squeezed by the projectile and the broken ceramic cone, so necking occurs, and cracks are generated and gradually expand to form petals. The projectile and the broken ceramic cone continue to press forward, and the petals bend and turn outward, forming the dishing deformationpetaling failure (Figure 12). If the projectile does not perforate the back plate, the back plate displays asymmetric bulging-dishing deformation (Figure 13).

**Figure 12.** Dishing deformation-petaling failure.

**Figure 13.** Bulging-dishing deformation.

In the working conditions where the projectile attitude and trajectory apparently change during penetration, the forces on the broken ceramic cone and the deformation area of the back plate bulge are obviously asymmetric. Meanwhile, due to the large projectile deflection, the breach shape is elliptical. The long axis direction of the ellipse is consistent with the axis direction of the projectile, and petals appear on both sides of the elliptical breaches (Figure 14). Taking working condition 11 as an example, the failure mode is analyzed as follows. When the projectile perforates and exits the back plate, the projectile first hits one side of the back plate obliquely, and further moves in this direction, resulting in a strip crack in the back plate in the direction parallel to the *Z*-axis (Figure 15 (T = 75 μs)), and the crack keeps expanding at both ends. When the crack expands to a certain degree, the projectile squeezes the back plate on the side of the crack (Figure 15 (T = 88 μs)), making the petals on one side of the back plate higher, whose width is roughly equal to that of the projectile, but less than the length of the original strip crack. Then, two smaller cracks appear near the short axis of the ellipse (Figure 15 (T = 114 μs)). When one side of the projectile tail hits the other side of the back plate, the petals on the other side also become higher. However, on this side, the projectile moves in the direction of gradually moving away from the petals; both the height and size of the petals on the projectile tail side are smaller than those on the nose side (Figure 15 (T = 194 μs)).

**Figure 14.** Fracture morphology of back plate in Experiment 3.

**Figure 15.** Deformation and failure process of the back plate under working condition 11.

In the working conditions where the projectile attitude and trajectory change little during penetration, the petals on the back plate appear more evenly, the breach shape is relatively regular, and the petal height is roughly the same (Figure 16). Taking working condition 17 as an example, when petaling failure occurs to the back plate and since there are many ceramic fragments in the front of the projectile and the deflection is small, the back plate is subjected to a relatively uniform force, resulting in a relatively uniform distribution of cracks. As the back plate damage continues along the crack, petals with large areas and good integrity are formed (Figure 17).

**Figure 16.** Fracture morphology of back plate in Experiment 1.

**Figure 17.** Deformation and failure process of the back plate under working condition 17.

#### *3.3. Influence of Impact Point on Anti-Penetration Performance*

The ceramic composite armor designed in this paper has periodic inhomogeneity in the direction perpendicular to the length of the ceramic column, so that the anti-penetration performance of the composite armor will be affected by the change in the impact point. In this section, under the condition that the initial velocity of the projectile is 810 m/s and the ratio of the diameter of the semi-cylindrical ceramic to the core is unchanged, the influence of the impact point on the anti-penetration performance of the semi-cylindrical ceramic composite armor is explored by changing the deviation degree *η* of the impact point.

Figure 18 shows the relationship between the residual projectile velocity *ν*r and the impact point deviation degree *η*. As shown in the figure, with the gradual increase *η*, the residual velocity *ν*r displays an overall decreasing trend first and then increases. For the residual velocity *ν*r, the change in impact point leads to the variation in two influencing factors, with the first being (1) ceramic thickness. The influence of the ceramic thickness below the projectile on the residual projectile velocity is mainly reflected in the change in the time *t*1 + *t*2 from the beginning of projectile penetration to back plate failure, when projectile velocity experiences a significant reduction. The thicker the ceramic, the longer *t*1 + *t*2, and the greater the velocity reduction. After the back plate is damaged, the velocity reduction rate of the projectile slows down rapidly. In the working conditions with large ceramic thicknesses, when the back plate starts to be damaged, the projectile velocity is smaller than that in the conditions with small ceramic thicknesses, so the projectile and the

composite armor have an increased action time, causing greater velocity reductions in the third and fourth stages of penetration than that in the conditions with small thicknesses. Therefore, without considering projectile deflection, the thicker the ceramic below the projectile, the greater the deceleration capability of the composite armor to the projectile. (2) The second influencing factor is the maximum attitude deflection angle *β*max of the projectile. As shown in Figure 19, with the increase *η*, the *β*max increases first and then decreases. The change in *β*max mainly affects the projectile's deceleration process in the third stage. The greater the *β*max, the greater the effect of the back plate on the projectile and the greater the deceleration degree in the third stage. Therefore, with the increase *η*, although the ceramic material below the projectile decreases gradually, the *β*max in the penetration process gradually increases first, and projectile deceleration in the third stage of penetration is obvious, resulting in the decrease in the residual projectile velocity. When *η* is further increased and the impact point is gradually close to the seam, the *β*max in during penetration is gradually decreased, and meanwhile, the ceramic material below the projectile is further reduced, so the residual projectile velocity is significantly increased.

**Figure 18.** Relationship between residual projectile velocity and impact point deviation degree *η*.

**Figure 19.** Relationship between the maximum projectile attitude deflection angle *β*max and impact point deviation degree *η*.

In order to reflect the anti-penetration performance of the semi-cylindrical ceramic composite armor more directly, the area of the composite armor is divided according to the different anti-penetration performance. The division criteria are the same as in the literature [27], and the remaining characteristics of the projectile body are shown in Table 5, where *<sup>E</sup>*plate is the residual kinetic energy of the projectile with the same initial velocity when penetrating the equivalent homogeneous ceramic composite armor. According to the

division criteria and the above residual characteristics of the projectile body, the composite armor can be divided into three areas, whose penetration resistance decreases successively, which are named as the strong protection zone, secondary protection zone, and weak protection zone. The distribution is shown in Figure 20, accounting for 66.67%, 16.67% and 16.67%, respectively.


**Table 5.** Residual characteristics of projectile at different impact points.

**Figure 20.** Area division of specially shaped ceramic composite armor.

#### *3.4. Influence of the Ratio of Semi-Cylindrical Ceramic Diameter to Core Diameter on Anti-Penetration Performance*

In order to investigate the effect of the ratio of the semi-cylindrical ceramic diameter to core diameter *ξ* on the anti-penetration performance, the areal density of the semicylindrical ceramic and the initial projectile velocity are left unchanged, and *ξ* = 0.56, 1.11, 2.22 and 2.78 are used. For the three typical impact points when *η* = 0, 0.5 and 1, a total of twelve working conditions are calculated respectively to study the anti-penetration performance of the semi-cylindrical ceramic composite armor under different semi-cylindrical ceramic diameters.

Figure 21 gives a comparison of the residual velocities of the projectile when penetrating ceramic composite armors with different *ξ* values, under the above three impact point conditions. By comparing the residual velocities of the projectile with the same diameter but different impact point deviation degrees *η*, it can be concluded that when *ξ* = 0.56, 1.11, the residual velocity difference under the three typical impact point deviation degrees is relatively small. This is mainly because the semi-cylindrical ceramic diameter is too small; in the first stage of penetration, it does not cause large asymmetric erosion to the projectile, resulting in small projectile deflection during penetration (Figure 22). In the third stage of penetration, the secondary deceleration of the projectile in the case of *η* = 0.5 is not apparent.

**Figure 21.** Comparison of residual velocities of the projectile when penetrating the ceramic composite armor with different *ξ* values when *η* = 0, 0.5, 1.

**Figure 22.** Damage produced when 12.7 mm API projectile penetrates three semi-cylindrical ceramic composite armors with different *ξ* values, when *η* = 0.5, (**a**) *ξ* = 0.56, (**b**) *ξ* = 1.11, (**c**) *ξ* = 2.22, (**d**) *ξ* = 2.78.

Regarding the anti-penetration performance of composite armors with different *ξ* values, as can be observed from Figure 21, when *ξ* = 0.56, 1.11, the residual velocities under the three typical impact point deviation degrees are slightly less than or slightly greater than the residual velocity *<sup>ν</sup>*plate in the case of homogeneous ceramic composite armor with equal areal density, and the projectile attitude deflection angle does not change significantly. So, the semi-cylinder design does not play a positive role in improving the anti-penetration performance of the armor. When *ξ* = 2.78, under the same areal density, the distribution of the ceramic material in the X direction is extremely uneven, resulting in the fact that the residual velocities in the case of *η* = 0, 0.5 are smaller than *<sup>ν</sup>*plate, but the residual velocity with *η* = 1 is much greater than *<sup>ν</sup>*plate; meanwhile, the theoretical value of the projectile attitude deflection angle is 0 in this case, which is unfavorable for armor protection. The anti-penetration performance of the ceramic composite armor with *ξ* = 2.22 has been described in Section 3.3. The comprehensive comparison shows that the composite armor with *ξ* = 2.22 performs the best in resisting penetration among the designed four types of composite armor with different semi-cylindrical ceramic diameters, under the areal density conditions adopted in this paper.

#### *3.5. Influence of Projectile Initial Velocity*

In order to explore the anti-penetration performance of the semi-cylindrical ceramic composite armor against the projectile with different initial velocities, the initial velocities of *ν*0 = 400, 700, 1000 and 1300 m/s are used, while keeping the deviation of the impact point of the projectile at *η* = 0.5. Under different initial velocity conditions, the maximum attitude deflection angle (before it completely hits the target) and residual mass of the projectile are shown in Figure 23. As can be observed from the figure, when the initial velocity of the projectile increases, the erosion degree of the projectile increases continuously, and the maximum attitude deflection angle decreases.

**Figure 23.** Maximum attitude deflection angle and residual mass of projectile under different initial velocities.

The increase in the initial projectile velocity directly leads to the decrease in its target penetration time. Under the working condition of *ν*0 = 1000 m/s, at t = 34 μs, the displacement of the center of mass of the projectile is Δy = −3.22 cm. Figure 24 presents the Y-direction displacement–time curve of the node at the center of mass of the projectile under different initial velocities. As illustrated, Δy = −3.22 cm under the working conditions of *ν*0 = 700, 1000 and 1300 m/s corresponds to 52 μs, 34 μs and 25 μs, respectively. In the working condition of *ν*0 = 400 m/s, the deflection of the projectile is too large, which cannot be displayed in the figure, and the corresponding time is t = 112 μs. Figure 25 shows the penetration under different working conditions with the same displacement of Δy = −3.22 cm. It can be observed from the figure that the projectile nose is near the bottom of the ceramic half cylinder in the three working conditions, i.e., the asymmetric erosion stage of the projectile ends. In other words, due to the increase in the initial projectile velocity, the time required for the projectile to go through this stage is shortened, and the angular acceleration differences between the three working conditions at this stage are small, all within the range of 0~0.008 rad·μs<sup>−</sup>1. Therefore, the time of the projectile in this phase is proportional to its attitude deflection angle, which is 13.74◦, 4.42◦, 1.37◦, and 0.37◦ in the three conditions. The magnitude of the attitude deflection angle of the projectile has a positive feedback effect on its further deflection. The larger the attitude deflection angle, the stronger the asymmetric action on the projectile, resulting in a further increase in the deflection of the projectile, which further promotes its self-deflection; otherwise, the further deflection will be smaller. Therefore, as the velocity increases, the deflection effect of the projectile decreases continuously. At the same time, the increase in the initial projectile velocity leads to the increase in the projectile-target acting force during the projectile's penetration into the composite armor, which then results in an increased degree of projectile erosion.

**Figure 24.** The time-history curve of Y-direction displacement of the projectile center of mass under different initial velocities.

**Figure 25.** Penetration under different working conditions.

To sum up, the anti-penetration performance of the semi-cylindrical ceramic composite armor against projectiles with different initial velocities shows the following trend: under low initial projectile velocities, the composite armor mainly exhibits large deflection and a relatively small erosion effect on the projectile; as the initial velocity increases, the erosion effect of the composite armor on the projectile gradually increases, while the deflection effect decreases.

## **4. Conclusions**

A semi-cylindrical ceramic composite armor structure is designed in this paper. The processes of projectile penetration deflection and the deformation and failure mode of the back plate are analyzed by the method of combining experiment and numerical calculations. The protective effect of the composite armor with different ratios of semi-cylindrical ceramic to core diameter on 12.7 mm armor-piercing firebombs in different areas and under the condition of equal areal density is mainly explored, and the trend of anti-penetration performance of the composite armor to projectiles with different initial velocities is reported.

(1) The process of the 12.7 mm API projectile penetrating ceramic composite armor can be divided into four stages. Projectile attitude deflection during penetration is mainly attributed to the non-axial force on the projectile, due to the asymmetric erosion of the projectile nose by the specially shaped ceramic and the non-ideal attitude of the projectile when penetrating the back plate. Due to projectile deflection, the projectile velocity experiences a significant secondary decline at the stage of back plate failure. After exiting the target plate, the projectile has an attitude deflection angle and angular velocity.

(2) After the projectile perforated and exited the target plate, dishing deformationpetaling failure occurred at the back plate, which is similar to the deformation/failure mode of an ogive-nosed projectile perforating a thin plate at a low velocity. When the projectile deflected to a certain extent during penetration, the breaches in the back plate showed elliptical shapes of varying degrees, and the size and height of the petals were also significantly different. When the attitude deflection was small, the breaches were regular, and the difference in the size and height of petals was relatively small.

(3) Due to the periodic inhomogeneity of the structure in the direction perpendicular to the length of the semi-cylinder, the impact point of the projectile has a grea<sup>t</sup> influence on the anti-penetration performance of the composite armor to 12.7 mm API projectiles. According to the remaining characteristics of the projectile, the composite armor can be divided into strong protection area, secondary protection area and weak protection area, and the proportion of each area is 67.67%, 16.67% and 16.67%, respectively.

(4) For the semi-cylindrical ceramic composite armor designed in this paper, when the ratio of semi-cylindrical ceramic diameter to core diameter *ξ* is less than 2, it leads to a small deflection during projectile penetration, and the design of the semi-cylinder contributes very little to improving the anti-penetration performance of the composite armor. Among the tested composite armor with *ξ* = 0.56, 1.11, 2.22 and 2.78, the armor with *ξ* = 2.22 has the best anti-penetration performance.

(5) The anti-penetration performance of the semi-cylindrical ceramic composite armor against projectiles with different initial velocities shows the following trend: under low initial projectile velocities, the composite armor mainly exhibits large deflection and a relatively small erosion effect on the projectile; as the initial velocity increases, the erosion effect of the composite armor on the projectile gradually increases, while the deflection effect decreases.

**Author Contributions:** Literature review, A.J. and Y.L.; writing—original draft preparation, A.J. and Y.L.; writing—review and editing, A.J., D.L. and H.H.; experiment performance, Y.L. and A.J.; experiment analysis, A.J. All authors have read and agreed to the published version of the manuscript.

**Funding:** This research was funded by the National Natural Science Foundation of China, gran<sup>t</sup> numbers 51679246 and 52101378.

**Institutional Review Board Statement:** Not applicable.

**Informed Consent Statement:** Not applicable.

**Data Availability Statement:** Not applicable.

**Acknowledgments:** The authors would like to thank the editor, associate editor, and the anonymous reviewers for their helpful comments and suggestions that have improved this paper.

**Conflicts of Interest:** The authors declare no conflict of interest.
