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  • ISSN 1001-1455  CN 51-1148/O3
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  • 力学类中文核心期刊
  • 中国科技核心期刊、CSCD统计源期刊

活性无序合金冲击的释能特性及在毁伤元中应用研究进展

侯先苇 张先锋 熊玮 谈梦婷 刘闯 戴兰宏

李芝绒, 张玉磊, 袁建飞, 王胜强. 内部爆炸薄圆板的变形及有效载荷[J]. 爆炸与冲击, 2020, 40(11): 113101. doi: 10.11883/bzycj-2020-0045
引用本文: 侯先苇, 张先锋, 熊玮, 谈梦婷, 刘闯, 戴兰宏. 活性无序合金冲击的释能特性及在毁伤元中应用研究进展[J]. 爆炸与冲击, 2023, 43(9): 091401. doi: 10.11883/bzycj-2023-0189
LI Zhirong, ZHANG Yulei, YUAN Jianfei, WANG Shengqiang. Deformation and payload of thin circular plates subjected to internal explosion[J]. Explosion And Shock Waves, 2020, 40(11): 113101. doi: 10.11883/bzycj-2020-0045
Citation: HOU Xianwei, ZHANG Xianfeng, XIONG Wei, TAN Mengting, LIU Chuang, DAI Lanhong. Research progress on impact energy release characteristics of reactive disordered alloy and its application in kill elements[J]. Explosion And Shock Waves, 2023, 43(9): 091401. doi: 10.11883/bzycj-2023-0189

活性无序合金冲击的释能特性及在毁伤元中应用研究进展

doi: 10.11883/bzycj-2023-0189
基金项目: 国家自然科学基金(11790292,12141202,12002170)
详细信息
    作者简介:

    侯先苇(1997— ),女,博士研究生,18260081681@163.com

    通讯作者:

    张先锋(1978— ),男,博士,教授,lynx@njust.edu.cn

  • 中图分类号: O385

Research progress on impact energy release characteristics of reactive disordered alloy and its application in kill elements

  • 摘要: 无序合金是一种新型金属材料,突破了传统的合金设计理念,表现出不同于传统合金的优异力学性能、冲击释能及剪切自锐特性,在高温、高压、高应变率等环境具有良好的应用前景。分析活性无序合金的冲击释能特性对其应用于军事领域有着重要的指导作用,能为弹药战斗部的设计提供参考。本文阐述了静动态力学实验中典型无序合金的反应释能现象;总结了撞击速度与活性无序合金释能超压、释能效率之间的关系;讨论了撞击速度、材料破碎程度及靶标特征等因素对活性无序合金释能机理的影响;归纳了制备工艺及元素类型对活性无序合金释能特性的调控效果。进一步,本文梳理了活性无序合金在破片、穿甲弹芯和聚能装药战斗部三个方向的应用研究进展,分析了活性无序合金毁伤元的侵彻行为和作用机制。最后,针对活性无序合金材料未来的发展趋势和需求进行了展望。
  • 内爆炸毁伤是打击水面舰船重要的毁伤方式,战斗部内爆炸产生的压力载荷作用于舰船舱壁结构,产生侧舷、横舱壁等结构变形或破坏,导致船舱进水,严重时可造成整船沉没。由于内爆炸载荷是一种多波峰叠加的复杂压力波,瞬态压力峰值高,载荷作用时间长,对船体结构的毁伤破坏比自由环境下的爆炸毁伤更剧烈、更复杂,因此,内爆炸载荷作用下结构的失效破坏成为了国内外学者研究的热点。

    对于爆炸载荷作用下板结构的变形失效,已开展了大量的实验研究和理论分析。Nurick等[1]、Wen[2]开展了周边固支低碳钢圆板受均匀载荷作用的变形实验研究。Jacob等[3]、Gupta等[4]开展了固支圆板在空爆载荷作用下的边界撕裂破坏实验研究。Geretto等[5]开展了均布载荷作用下固支方板的失效模式实验。Teeling-Smith等[6]利用有限元分析软件开展了均布脉冲载荷作用下软钢薄圆板的变形撕裂研究,得到了板厚度、不同边界支撑等特性对板变形的影响。朱锡等[7]、陈长海等[8]开展了爆炸载荷作用下固支方板的变形实验研究。崔高领等[9]进行了均布冲击载荷对金属方板的仿真计算研究。这些研究均在空爆或半密闭环境下开展,而对于密闭环境下板结构变形与载荷关系的研究较少,如姚熊亮等[10]开展的舰船舱内爆炸载荷特征与板架毁伤规律仿真研究,侯海量等[11]开展的舱内爆炸载荷及舱室板架结构的失效模式研究。与空爆压力载荷相比,密闭环境下的压力载荷是一种多波峰叠加、准静态压力作用时间长的复杂压力波,受压后的板结构在产生塑性变形的过程中还存在极限变形[12]现象,即结构变形达到一定值后不会持续增大,后续阶段的压力载荷对结构变形不产生影响。这种产生板结构极限变形的压力载荷称为有效压力载荷或饱和压力载荷,研究有效压力载荷随时间的变化规律,掌握其与板结构的耦合作用关系,成为研究内爆炸结构变形破坏的关键。郑成等[13]、孔祥韶等[14]通过仿真计算方法,研究了密闭方形结构内方薄板的变形特性,并提出了方板变形预报模型和内爆炸压力载荷等效模型。而通过内爆炸实验方法研究板结构的变形特征与压力载荷关系,目前鲜有报道。

    本文中基于双圆筒爆炸装置,开展TNT和某温压装药对铝质、钢质薄圆板的内爆炸实验,获取薄圆板的变形和压力载荷数据,分析薄圆板的破坏模式和压力载荷特点,并基于相同变形下作用载荷相等原理,确定薄圆板极限变形的有效比冲量和作用时间,提出圆薄板变形的预报模型并进行验证,以期为内爆炸结构毁伤研究提供技术参考。

    实验双圆筒装置如图1所示,由两段圆筒、薄平板、前/后端盖、密封圈组成,在圆筒端部设有法兰盘。薄平板放置于两个圆筒端部的法兰盘之间,由螺钉将两个圆筒、薄平板密封连接,形成两个密闭圆筒腔室。圆筒长1 670 mm,内径800 mm,壁厚12 mm。为达到薄平板与法兰盘连接接近固支条件,在法兰盘的端面上铣出几组细浅同心圆,并对圆筒内端面角作倒圆角处理,减小其对薄板变形的影响。薄平板为2 mm厚的铝板和1 mm 厚的Q235钢板,在靠近边缘的同心圆周上,设置与圆筒法兰盘孔对应的圆孔。

    图  1  双圆筒爆炸装置及测点布设位置
    Figure  1.  Double cylinder explosive device and locations of measuring points

    实验装药为柱形TNT和某温压装药,长径比1∶1,其中TNT密度为1.58 g/cm3,质量分别为20和40 g;某温压装药(主要组成为HMX和Al粉)密度为1.84 g/cm3,质量分别为20、30、40、50、60、70和80 g。实验时,将药柱垂直悬挂于圆筒的几何中心,由电雷管起爆1 g C4扩爆药柱,引爆装药。

    在爆炸圆筒一端圆形盖板的中心轴线上,按照从圆心到边缘的顺序均布4个压力测量点P1、P2、P3、P4,如图1(c)所示。测点布设的压力传感器为PCB公司113B24型壁面压力传感器,量程为0~6.9 MPa。传感器敏感面距盖板内表面约0.8 mm。安装完成后,在传感器头部敏感面与安装孔形成的凹槽内涂满油脂,使油脂表面与盖板表面平齐,其目的是延长爆炸热传递到传感器敏感面的时间,减小热冲击对压力载荷测量的影响。

    基于爆心对称的两个刚性壁面上,冲击波在静止刚性壁面的反射压力与运动刚性壁面的反射压力差异不大[15],可近似认为实验获取的盖板测点压力载荷等于圆薄板对称位置的压力载荷。

    本文中共进行了10个工况实验,其中工况1~3为铝质薄圆板的变形破坏实验,工况4是为了补充获取工况2开展的40 g TNT装药在爆炸室的压力载荷数据实验,工况5~10为钢质薄圆板的变形破坏实验。典型铝质、钢质薄圆板实验后的状态如图2所示,各实验工况薄圆板的变形挠度及破坏情况如表1所示,其中WY代表某温压装药。

    表  1  各实验工况圆板的变形结果
    Table  1.  Deformation results of circular plate under various experimental conditions
    实验工况平板材质平板厚度/mm装药类型装药质量/g圆板挠度/mm变形破坏结果
    12TNT20 71.5夹持边、中心塑性大变形
    22TNT40夹持边被切断
    32WY20 93.0夹持边间断性裂缝
    41TNT40 85.5夹持边、中心塑性大变形
    51WY30 86.0夹持边、中心塑性大变形
    61WY40100.5夹持边、中心塑性大变形
    71WY50111.0夹持边、中心塑性大变形
    81WY60122.0夹持边、中心塑性大变形
    91WY70134.0夹持边、中心塑性大变形
    101WY80147.0夹持边、中心塑性大变形
    下载: 导出CSV 
    | 显示表格
    图  2  典型铝质、钢质薄板实验后状态
    Figure  2.  Pictures of typical aluminum and steel thin circular plates after experiments

    图2可以看出,工况2的铝质薄圆板从夹持边界剪切断裂,切下圆板飞向邻室,落于后端盖底部,扭缩成团,如图2(b)所示,其剪切断面边缘有微小弯曲和大小不均匀的小尖刺。除工况2外,其他工况的铝质、钢质薄板均产生了四周顶起的锥形隆起结构,在薄板的夹持边界和中心区域产生了显著塑性大变形,在中心区域形成了比周边结构更陡峭的锥尖,且锥角随装药质量的增大而减小,更尖锐。在工况3的铝板夹持边界还产生了两段不连续的断裂裂缝,如图2(c)中红色圈内标注线及左侧放大图所示,从裂缝断面可以看出,夹持边界有显著的板厚拉伸减薄现象,断面边缘不规则,有长度不等的细长尖刺。工况5~10的装药为某温压药,钢质薄板产生了大变形,变形挠度随装药质量的增加而增大。

    从上述圆板变形结果可以看出,在圆板夹持边界和中心产生了塑性大变形,在夹持边界还出现了局部撕裂和剪切断裂现象,主要原因是在圆板夹持边界和中心产生了应力极值点。参考方形薄板的应力响应分析[16],在爆炸压力载荷作用下,固支夹持边界处形成弯曲转角,产生拉伸应变,当弯曲应变小于边界极限应变时,夹持边界产生大弯角,形成的运动塑性铰环从夹持边界向圆板中心移动收缩。在塑性铰环内部,圆板作刚体平行移动[17],塑性铰环通过的外部则形成了曲面板,并按照锥形分布速度运动。当后续压力载荷作用下,圆板变形不持续增大时,塑性铰环收缩到圆板中心,形成锥尖;当弯曲应变接近板的极限应变时,在夹持边界产生局部的撕裂;当超过板的极限应变后,夹持边界产生横向剪切断裂。

    圆板的实验结果表明,在内爆炸载荷作用下,薄圆板产生了3种破坏模式:塑性大变形、拉伸撕裂、横向剪切。该结果与文献[14]所得到的空爆压力载荷作用下梁、圆板的变形破坏模式一致。

    工况7的4个测点测量的压力载荷曲线和积分处理后的比冲量曲线如图3所示。从图3(a)的压力载荷曲线可以看出,4个压力测点的压力载荷到达时间差小于0.12 μs,P1、P2、P3测点最大压力峰值基本一致,角隅测点P4的最大峰值约为其他测点最大峰值的2倍,4个测点的压力载荷随时间的变化趋势基本一致。从图3(b)的比冲量曲线可以看出:在3 ms内,4个测点的比冲量大小与比冲量增长量基本一致,虽然P4测点的最大压力峰值最高,但是比冲量与其他测点基本相当;3 ms后,除P3测点外,其他测点的比冲量增长量基本一致。观察P3测点的压力载荷曲线发现,3 ms后,其压力值比其他测点略小,原因可能是受到爆炸热冲击对压力传感器性能的影响,由于压电型传感器具有热释电效应,当传感器的隔热防护作用不够时,爆炸热通过热传导作用到传感器的敏感元件上,输出热冲击干扰信号,并且传感器的预紧结构受热膨胀,预紧力减小,导致传感器的灵敏度变小,输出的压电信号也减小。

    图  3  工况7的4个测点压力载荷曲线和比冲量曲线
    Figure  3.  Pressure load curves and specific impulse curves of four measuring points under condition 7

    其他实验工况下4个测点的载荷特性与工况7基本类似,除角隅位置压力载荷的最大峰值是其他测点的2倍外,其他时刻4个测点的压力载荷大致相等,比冲量也基本一致。因此可由一个测点的压力载荷反映整个圆板面上的压力载荷。各工况圆板中心测点P1的压力载荷曲线如图4所示。

    图  4  各实验工况圆板中心的压力载荷曲线
    Figure  4.  Pressure load curves of circular plates under various experimental conditions

    图4所示的压力载荷曲线可以看出,薄圆板受到多波峰叠加的复杂压力载荷作用。在初始阶段,压力波以显著的一大一小波峰组合周期性衰减出现,变化周期为2.8~3.5 ms(药量越大周期越短),每一周期内的波峰值均比前一周期对应的波峰值小,3个周期后,两个波峰逐渐融合,形成了压力波动逐渐减小的准静态压力。工况2的压力曲线在7.9 ms内,波形特征与其他工况的变化规律类似,7.9 ms后压力逐渐减小,形成约12 ms的周期性振荡波。工况5~10的压力载荷最大峰值和匀化形成的准静态压力均随着装药质量的增大而增大,但振荡周期随着装药质量的增大而缩短,从3.5 ms逐渐缩短到2.8 ms。

    将上述各工况圆板中心测点P1的压力载荷积分处理,得到比冲量时间曲线,如图5所示。

    图  5  各实验工况圆板中心比冲量曲线
    Figure  5.  Specific impulse curves of circular plates under various experimental conditions

    除工况2外,其他工况的比冲量时间曲线变化规律类似,在约0.35 ms内,比冲量曲线急剧上升,随后呈波浪式增长,并且随着时间的延长,波浪振幅逐渐减小,逐渐趋于线性增长。这主要是由于爆炸室内压力波趋于匀化,形成了压力波动较小的准静态压力所致。比冲量波动周期等于压力载荷波动周期,并且随着装药质量的增加,比冲量也随之增大。

    工况2与工况4的装药类型和装药质量相等,比冲量值在7.9 ms内基本一致,7.9 ms后,工况2的比冲量增长率相对减缓,形成了周期约12 ms的新波动。结合工况2薄圆板的破坏结果,可得到在7.9 ms时刻,铝板受到的比冲量为1.720 MPa·ms,铝板夹持边界的弯曲应变超过板的极限应变,产生了瞬时剪切断裂现象。工况3的铝板夹持边界产生了两小段撕裂破坏,其破坏时刻的弯曲应变接近铝板的极限应变,受到的比冲量应小于1.720 MPa·ms。工况5~10的钢质薄圆板,在压力载荷作用时间内,夹持边界产生的弯曲应变均小于材料的极限应变。

    基于圆板上比冲量时间曲线呈线性增长的特点,其增长量由圆筒内形成的准静态压力产生,因此,除去比冲量曲线前期0.35 ms内的急剧上升段,选取0.35~20.0 ms的比冲量数据作线性拟合处理,得到比冲量平均增长率,该增长率近似等于圆筒内的准静态压力。由于急剧上升段的比冲量主要由压力载荷的最大峰值脉冲积分产生,脉冲持续时间短,可以近似认为圆板受到的比冲量瞬时增长到Δi,然后线性增长,因此,圆板上的比冲量i可表示为:

    i=pt+Δi
    (1)

    式中:p为圆筒内准静态压力,t为压力载荷作用时间,Δi为比冲量快速增长量。

    对各工况的比冲量数据进行处理,可得到各工况的准静态压力p和比冲量快速增长量Δi表2为工况5~10的准静态压力pΔi以及3、5和10 ms时的比冲量实验值和依据式(1)得到的计算值。

    表  2  工况5~10的 p和Δi及典型时刻模型比冲量的计算值和实验值
    Table  2.  p and Δi of conditions 5−10 and the calculated and experimental specific impulses at typical times
    实验
    工况
    压力/
    MPa
    比冲量快速增长量/
    (MPa·ms)
    3 ms 时的比冲量/(MPa·ms)5 ms 时的比冲量/(MPa·ms)10 ms 时的比冲量/(MPa·ms)
    计算值实验值计算值实验值计算值实验值
    50.1990.2900.8610.7581.2361.2642.1722.217
    60.2350.3321.0560.9701.5121.4092.6532.568
    70.2940.3931.2371.2001.7691.7013.0973.244
    80.3220.4711.4081.2892.0101.8563.5153.520
    90.3420.5181.5711.4242.2402.1233.9123.927
    100.3770.5661.7271.6482.4602.4464.2914.342
    下载: 导出CSV 
    | 显示表格

    对比表2中的比冲量计算结果和实验结果可知,3、5和10 ms时段内的计算结果与实验结果的偏差分别为13.6%、8.3%和4.5%。可以看出:随着载荷作用时间的加长,模型计算结果与实验结果的偏差减小。这表明比冲量计算模型可以近似预估圆板受到的比冲量,且载荷作用时间越长,计算结果越接近实验结果。

    Barker等[18]提出了一种内爆炸准静态压力p计算模型:

    p=A(m/V)γ
    (2)

    式中:m为炸药装药质量,V为内爆炸空间体积,Aγ为相关因子。

    将上述工况5~10的准静态压力p的实验结果、实验装药、圆筒体积,按照式(2)的幂指数模型进行拟合,可以得到该装药的准静态压力计算模型,其中:系数A=1.865,γ=0.67。依据该计算模型得到工况5~10的准静态压力p为0.200、0.243、0.282、0.319、0.353、0.386 MPa,与表2中压力的实验结果进行比对可知,偏差小于4.7%。

    上述快速增长比冲量Δi,主要由压力载荷曲线中起始段最大峰值的压力脉冲积分得到,该脉冲的最大峰值、脉宽与装药质量及爆心距相关,因此,按照比冲量与比对距离成幂指数关系:

    Δi=K(3m/r)δ
    (3)

    式中:Kδ为因数,r为内爆炸爆心距。将表2中工况5~10的Δi实验值、装药质量、爆心距按照式(3)的幂指数模型进行拟合处理,得到K=2.051,δ=2.11。依据该模型计算工况5~10的Δi分别为0.299、0.372、0.441、0.506、0.569、0.630 MPa·ms,与表2Δi的实验结果比对可知,偏差小于3.3%,表明该模型能够描述冲量曲线中快速增长段的比冲量Δi

    将式(2)、式(3)代入式(1),则式(1)转化为:

    i=A(m/V)γt+K(3m/r)δ
    (4)

    Zhao等[12]提出了平板变形的极限响应现象,即在平板变形达到一定值后不会持续增加,后续的作用载荷对平板的变形不产生影响,存在平板极限变形的有效载荷及作用时间。对于薄板结构,一般遵循冲量毁伤准则,即对薄板的破坏主要由冲量载荷产生。在空爆环境下,冲量值可通过冲击波压力正压时间内的比冲量与板面积的乘积得到,而在内爆炸环境下,由于压力载荷为多波峰叠加并逐渐匀化为准静态压力的复杂波,正压时间长,无法确定载荷作用时间,因此不能依据获取的压力载荷数据直接得到有效比冲量和作用时间。

    上述内爆炸压力载荷未完全匀化前的压力波,可近似看作一种瞬态升压后又缓慢衰减的单波峰压力波(忽略内部压力波动),与外爆炸压力波波形特点相似。因此,可基于相同变形下冲量载荷相等原理,认为空爆条件下圆板受到的冲量载荷等于内爆炸条件下圆板极限变形所受到的有效冲量,再依据有效冲量,得到载荷作用时间。

    在空爆条件下,Jacob等[19]提出了钢质圆板的变形挠度计算模型:

    δ0H=0.425ϕc
    (5)

    式中:δ0为圆板变形挠度;H为圆板厚度;ϕc为无量纲数,其表达式为:

    ϕc=IπRH2ρσ0
    (6)

    式中:I为圆板受到的冲量,R为圆板半径,ρ为平板材料的密度,σ0为平板材料的静态屈服应力。

    空爆作用下圆板上的冲量I等于内爆炸作用下圆板上的有效冲量I0,因此,式(5)、式(6)变形后,得到内爆炸圆板上的有效冲量:

    I0 =δ0H×πRH2ρσ00.425=πδ0RHρσ00.425
    (7)

    图3中圆板各测点的比冲量曲线可以得到,圆板面上各测点的比冲量基本相等,随时间加长比冲量的增长率也基本一致,表明圆板面上各位置的瞬态比冲量基本一致,随时间的增长比冲量增量也基本相当,特别是装药质量越大,一致性越好。因此,圆板上任意一点的有效冲量可通过测量点的有效比冲量与圆板面积之积得到:

    I0=i0s
    (8)

    式中:i0为圆板测量点的有效比冲量,s为圆板面积。

    将工况5~10中钢质圆板的变形挠度代入式(7),并结合式(8),得到钢质圆板的有效冲量I0、有效比冲量i0,如表3所示,其中钢板密度为7 800 kg/m3σ0=235 MPa。

    表  3  工况5~10钢质圆板的有效冲量和有效比冲量
    Table  3.  Effective impulses and effective specific impulses of steel circular plates under conditions 5−10
    实验工况圆板挠度/mm有效冲量/(Ns)有效比冲量/(MPams)修正有效冲量/(Ns)修正有效比冲量/(MPams)作用时间/ms
    5 86.03440.656389 0.7772.93
    6100.54020.7674560.9122.76
    7111.04440.8475051.0092.55
    8122.0476 0.9085421.0842.43
    9134.05361.0236121.2242.36
    10147.05881.1226731.3452.26
    下载: 导出CSV 
    | 显示表格

    式(6)中忽略了爆炸动态加载过程中材料应变率的影响,在瞬态强压力载荷作用下,平板结构的动力响应与材料的应变率显著相关,因此,需要考虑材料应变率变化的影响。Cowper-Symonds提出了材料动态屈服应力与静态屈服应力的关系模型[19]

    σdσ0=1+(v0δ32˙ε0R2)1/q
    (9)

    式中:σd为平板材料的动态屈服应力,v0为平板的瞬态速度,˙ε0q为与材料相关的常数。按照动量守恒,平板上的比冲量iv0的关系为i=ρδv0,代入式(9)得到:

    σdσ0=1+(i32ρ˙ε0R2)1/q
    (10)

    对于Q235低碳钢材料,˙ε0一般取值[19]为40.4 s−1q取值为5。将表3中的有效比冲量i0代入式(10),得到对应的σd,再将σd代入式(7),得到修正后的有效冲量Im和有效比冲量im

    依据修正后的有效比冲量im,在各工况比冲量时间曲线上,由im得到对应有效比冲量作用时间t,如表3所示。由表3可以看出:随着圆板变形挠度的增大,有效比冲量im随之增大,有效载荷作用时间t随着圆板变形挠度的增大而缩短。

    将有效比冲量im和作用时间t进行数据拟合处理,得到有效比冲量im与作用时间t的关系式:

    t=75.64i0.49m
    (11)

    因此,当确定了圆板材料、尺度和极限变形量后,可以通过式(7)和式(10)得到有效比冲量,再依据式(4)和式(11)预估圆板极限变形下的装药质量。

    依据上述方法,预估工况5~10钢质圆板极限变形下的装药量,分别为26、35、44、52、63和75 g,与实验装药量比较可知,偏差小于13.3%,表明该模型可以预估内爆炸作用下圆板的变形情况。

    通过双圆筒型装置内薄圆板的爆炸实验,研究了圆板的变形破坏模式和比冲量载荷变化规律,并基于相同变形下的冲量载荷相等原理,确定了内爆炸圆板极限变形下的有效比冲量和作用时间,提出了薄圆板变形的预报模型,并进行了验证,结果表明:

    (1)在内爆炸压力载荷作用下,圆板的夹持边界和中心区域是应力集中区,圆板产生了塑性大变形、拉伸撕裂和横向剪切3种破坏模式。

    (2)圆板上的内爆炸压力载荷为多波峰的复杂压力波,初始阶段比冲量陡峭增长,随后由波浪式增长逐渐匀化为线性增长,增长率近似等于装药在爆炸室内形成的准静态压力。

    (3)在实验圆筒装置内,当1 mm厚钢质圆板产生86~147 mm的变形挠度时,有效比冲量在0.777~1.345 MPa·ms范围,有效载荷作用时间在2.26~2.93 ms范围。通过验证,由圆板变形预估模型得到的装药质量与实验装药质量偏差小于13.3%。

  • 图  1  室温下空气中测试的锆基非晶合金试样断裂瞬间[19]

    Figure  1.  Moment of fracturing a BAA specimen testedat room temperature in air[19]

    图  2  摆锤冲击试验装置及空气环境中试验现象[20]

    Figure  2.  Pendulum impact test device and test phenomena in air environment[20]

    图  3  Zr41.2Ti13.8Cu12.5Ni10Be22.5分子轨道能级谱[20]

    Figure  3.  Molecular orbital energy spectrum of Zr41.2Ti13.8Cu12.5Ni10Be22.5[20]

    图  4  氮气环境中断裂后断口扫描电镜照片[20]

    Figure  4.  Scanning electron microscope photos of fracture surface of the specimen fracturing in nitrogen environment[20]

    图  5  准密闭容器试验[25]

    Figure  5.  Quasi-sealed chamber test[25]

    图  6  高速摄影图片及容器内超压时程曲线[26]

    Figure  6.  Video frames and pressure curves inside the chamber[26]

    图  7  破片撞击靶板后反应产物形貌与成分[26]

    Figure  7.  Morphology and composition of the reaction products of fragment after impacting target[26]

    图  8  高熵合金破片不同撞击速度下压力峰值[33]

    Figure  8.  Peak overpressures at different impact velocities of the high-entropy alloy fragments[33]

    图  9  多种活性材料的单位质量能量密度[34]

    Figure  9.  Specific energy per unit mass of various reactive materials[34]

    图  10  锆基非晶合金动态压缩高速摄影图像[37]

    Figure  10.  High-speed photography of Zr-based amorphous alloy under dynamic compression[37]

    图  11  锆基非晶合金动态压缩模拟损伤云图[37]

    Figure  11.  Simulational damage contours of Zr-based amorphous alloy under dynamic compression[37]

    图  12  氩气中不同撞击速度下动态破碎锆基非晶合金累积质量分布试验数据[38]

    Figure  12.  Experimental data of cumulative mass distribution forZr-based amorphous alloy after dynamic fragmentation atdifferent impact velocities in argon atmosphere[38]

    图  13  TiZrNbV高熵合金动态压缩背散射电子成像结果[40]

    Figure  13.  BSE result of TiZrNbV high entropy alloy after dynamic compression[40]

    图  14  不同撞击速度下回收试样的断口形貌[40]

    Figure  14.  Fracture morphology of recovered specimen at different impact velocities[40]

    图  15  原位晶化对锆基非晶合金能量释放行为的影响[45]

    Figure  15.  Effect of in-situ crystalline phases on the energy release behaviors of Zr-based amorphous alloy[45]

    图  16  NbZrTiTa高熵合金和HfZrTiTa0.53合金弹丸在不同速度下撞击靶箱后的碎片[50]

    Figure  16.  The fragments of NbZrTiTa high-entropy alloy and HfZrTiTa0.53 high-entropy alloy projectilesimpacting the target at different velocities[50]

    图  17  1200 m/s速度下NbZrTiTa高熵合金弹丸碎片的截面背散射电子成像[50]

    Figure  17.  Cross-section BSE photos of NbZrTiTa high-entropy alloy projectile at 1200 m/s[50]

    图  18  0.5 mm厚的盖板下破片不同撞击速度对应的压力-时间的曲线[60]

    Figure  18.  Pressure as a function of time for a 0.5 mmcover target thicknesses[60]

    图  19  不同靶板厚度下不同撞击速度对应的超压-时间曲线[60]

    Figure  19.  Overpressure as a function of time for differentcover plate at different impact velocities[60]

    图  20  超压-反应速率曲线[60]

    Figure  20.  Reaction efficiency as a function of shock pressure[60]

    图  21  冲击温度-反应速率曲线[60]

    Figure  21.  Reaction efficiency as a function of shock temperature[60]

    图  22  Zr55Cu30Ni5Al10非晶合金破片典型速度撞击间隔靶板高速摄影图片[71]

    Figure  22.  High-speed photographs of Zr55Cu30Ni5Al10 amorphous fragments impacting spacing targets at typical velocity[71]

    图  23  WFeNiMo高熵合金在不同速度下穿靶燃烧过程的高速摄影[72]

    Figure  23.  High-speed video frames of combustion process of WFeNiMo HEA at different speeds[72]

    图  24  高速撞击后高熵合金回收破片细观结构[72]

    Figure  24.  Microstructure of high-entropy alloy fragments after high speed impact[72]

    图  25  非晶破片毁伤后效仿真结果[73]

    Figure  25.  Simulation results of amorphous fragmentation damage aftermath[73]

    图  26  W/Zr基非晶合金预制破片[11]

    Figure  26.  W/Zr-based amorphous alloy fragments[11]

    图  27  预制破片布置方式[11]

    Figure  27.  Arrangement of performed fragments[11]

    图  28  典型时刻高速摄影图片[11]

    Figure  28.  High-speed photographs at typical moments[11]

    图  29  棉被和油箱毁伤情况[11]

    Figure  29.  The damage of quilts and fuel tanks[11]

    图  30  破片侵彻后油箱[11]

    Figure  30.  The oil tank penetrated by fragments[11]

    图  31  复合材料弹芯的“自锐”和钨合金弹芯的“镦粗”[77]

    Figure  31.  “Self-sharpening” of composite core and the “upsetting” of tungsten alloy core[77]

    图  32  弹芯残体照片[82]

    Figure  32.  Pictures of penetrator residual[82]

    图  33  钨丝/锆基非晶复合材料侵彻深度与着靶动能及长径比的关系曲线[80, 86]

    Figure  33.  Curves of kinetic energy and penetration depth of Wf/Zr-MG and WHA rods[80, 86]

    图  34  不同直径钨丝/锆基非晶复合材料着靶速度-侵彻深度关系[86]

    Figure  34.  Relationship between penetration depth and impact velocities of different Zr-based composite materials[86]

    图  35  多组分钨丝/锆基非晶合金复合材料杆弹横截面[86]

    Figure  35.  The cross section of multi-component Wf/Zr-based amorphous composite rod projectiles[86]

    图  36  分段式钨丝/锆基非晶合金复合材料杆弹及侵彻结果(单位:mm)[86]

    Figure  36.  Segmented Wf/Zr-based amorphous composite rod projectiles and penetration results (unit: mm)[86]

    图  37  弹体侵彻靶体的高速摄像[88]

    Figure  37.  High-speed video photographs of the projectiles penetrating the targets[88]

    图  38  长杆弹侵彻深度和撞击动能的关系[88]

    Figure  38.  Relation between penetration depth and kineticenergy of long rod projectiles[88]

    图  39  长杆弹弹孔体积和撞击动能的关系曲线[88]

    Figure  39.  Relation between total penetration volume and kinetic energy of long rod projectiles[88]

    图  40  弹体侵彻靶板典型过程[89]

    Figure  40.  Typical frames of the projectiles penetrating the targets[89]

    图  41  弹体侵彻后靶板表面毁伤效果[89]

    Figure  41.  The targets damaged surface after the projectiles penetrating[89]

    图  42  钨丝/锆基非晶合金复合材料自锐剪切失效的 4 种模式[81]

    Figure  42.  Four modes of self-sharpening shear failure of Wf/Zr-based amorphous composites material[81]

    图  43  钨丝增强金属玻璃复合材料弹残余弹体头部及其附近位置 SEM 图像[79]

    Figure  43.  SEM images of tungsten wire reinforced metal glass composite residual projectile head and its vicinity[79]

    图  44  回收弹体TEM测试结果[90]

    Figure  44.  Transmission electron microscope (TEM) bright-field images of LRPs after impact[90]

    图  45  回收弹体TEM明图中的变形孪晶和堆叠断层[90]

    Figure  45.  TEM results showging the multiple deformation twins and the stack faults[90]

    图  46  钨丝/锆基非晶合金复合材料杆弹不同着靶速度下的侵彻断裂模式[86]

    Figure  46.  Fracture modes of Wf/Zr-based amorphous composite projectile at different impact velocities[86]

    图  47  WFeNiMo和93W长杆弹对靶体的侵彻深度与动能关系[9]

    Figure  47.  Depth of WFeNiMo rod and 93W rod penetrating targets versus kinetic energy[9]

    图  48  等截面直管内两相的流动模型[91]

    Figure  48.  Model of two-phase flow in a straight pipe with equal cross section[91]

    图  49  不同初始浓度及密度对硬相浓度演化的影响[91]

    Figure  49.  Effect of initial concentration on concentration evolution of hard phase[91]

    图  50  Zr57Cu15.4Ni12.6Al10Nb5非晶合金射流成型形态[95]

    Figure  50.  Shape of Zr57Cu15.4Ni12.6Al10Nb5 jet forming[95]

    图  51  Zr41.2Ti13.8Cu12.5Ni10Be22.5非晶合金射流成型形态[96]

    Figure  51.  Shape of Zr41.2Ti13.8Cu12.5Ni10Be22.5 jet forming[96]

    图  52  塑性和脆性药型罩形成的射流[98]

    Figure  52.  Jets by plastic and brittle liner[98]

    图  53  两种材料杆式射流不同时刻下的成形状态[99]

    Figure  53.  Shape of rod jets about two materials at different times[99]

    图  54  CrMnFeCoNi与紫铜材料流动速度(V2)与临界压垮角(βc)关系[100]

    Figure  54.  Relationship between flow velocity (V2) and critical crushing angle (βc) of CrMnFeCoNi and copper[100]

    图  55  材料流动速度(V2)与临界压垮角(βc)曲线不同取值位置有限元仿真结果[100]

    Figure  55.  Finite element simulation results of value positions of flow velocity (V2) and critical crushing angle (βc) curve[100]

    图  56  不同硬化指数k下射流形态对比[100]

    Figure  56.  Comparison of jet shape under different hardening index (k)[100]

    图  57  不同炸高下药型罩侵彻深度[105]

    Figure  57.  Penetration depths of liners under different stand off[105]

    图  58  数值模拟模型及成型射流[12]

    Figure  58.  Model and jet structure of numerical simulation[12]

    图  59  聚能装药结构[109]

    Figure  59.  Shaped charge[109]

    图  60  靶板截面形貌和晶相[12]

    Figure  60.  Cross-section profile and crystal phase of target plate[12]

    图  61  残余射流区的XRD谱[12]

    Figure  61.  XRD spectrum of residual zone[12]

    图  62  残余射流区的EDS谱[12]

    Figure  62.  EDS spectrum of residual zone[12]

    图  63  射流侵彻后靶板的EBSD细观分析:(a)变形区IPF图;(a)中区域b的(b1、b2)IPF图和对应的KAM图;(a)中区域c的(c1, c2) IPF图和对应的KAM图[113]

    Figure  63.  Microstructural analysis of the residual jet after penetration via EBSD: (a) IPF map of deformation zone; (b1, b2) IPF map and corresponding KAM map of region b in (a); (c1, c2) IPF map and corresponding KAM map of region c in (a)[113]

    图  64  再结晶区的高倍BSE-SEM图像(a)及线扫描分析(b):在(a)中显示的两个晶界上进行线扫描,其对应的位置在(b)中用虚线标记[113]

    Figure  64.  High-magnification BSE-SEM images (a) and line scan analysis (b) of the recrystallization region: a line scan was conducted across two grain boundaries as displayed in (a), the corresponding locations of which are labeled with dashed lines in (b)[113]

    图  65  CoCrNi残余射流侵彻后的TEM组织分析:(a) CoCrNi残余射流的TEM照片,其中的白色虚线标记了沿晶界的纳米尺寸沉淀;(b) 降水(图(a)中的红色矩形区域)的HAADF-TEM照片;(c~e) 图(b)中对应的Co、Cr、Ni元素分布;(f) 降水SAED图(区域I(b)),(g) 图(b)中Ⅰ,Ⅱ,Ⅲ,Ⅳ区域Co,Cr,Ni元素含量[113]

    Figure  65.  Microstructural analysis of CoCrNi residual jet after penetration by TEM: (a) TEM images of CoCrNi residual jet, where the white dashed line marks the nanosized precipitations along grain boundaries; (b) HAADF-TEM image of the precipitation (red rectangle region in (a)); (c–e) Corresponding element distributions of Co, Cr, and Ni in (b); (f) SAED pattern ofprecipitation (region I in (b)); (g) Element content of Co, Cr, and Ni in region I, II, III, IV in (b)[113]

    表  1  锆基非晶合金的冲击化学反应行为[36]

    Table  1.   Impact-induced chemical reaction behavior of ZrTiNiCuBe[36]

    射击序号 靶板厚度/mm 撞击速度/(m·s−1 超压峰值/MPa 扩孔半径/mm 挠度/mm
    1 3 1450 0.02 7~10 10~15
    2 3 1560 0.04 10~15 15~20
    3 2 1348 0.05 20~25 20~25
    4 2 1218 0.024 8~12 10~15
    5 4.5 1630 0.021 7~10 8~10
    下载: 导出CSV
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