The critical behavior of Kac-type models for semi-infinite systems

The critical behavior of the layer magnetizations and local susceptibilities of theD-vector lattice models with Kac-type ferromagnetic interactions for a semi-infinite system is studied. These local quantities behave less singularly than the bulk ones, showing that this is not peculiar to the two-dimensional Ising model. Moreover, the limiting form (at the critical point) of the magnetization profile can be obtained, which, when properly scaled, satisfies the minimum condition in the Landau theory for a semi-infinite continuous system. Landau-type critical behavior is thus recovered.     

一类反应扩散方程解的渐近性质及其应用

本文讨论问题 ｕｔ＝Ａｕｘｘ＋ｆ（ｘ，ｔ，ｕ）， ｕｘ｜ｘ＝０＝０，ｕｘ｜ｘ＝１＝０， ｕ｜ｔ＝０＝ｕ０（ｘ）。 的解的渐近性质，将参考文献［１］的Ｌ＾２范数估计     

一个反应扩散方程的门槛结果

本文讨论反应扩散方程Ｃａｕｃｈｙ问题解的整体存在性，渐近性质和Ｂｌｏｗｕｐ问题．其中或者１＜ｑ＜ｐ＜＋∞，ｎ＝２．得到门槛结果．     

炭纤维织物/环氧树脂基复合材料的摩擦磨损性能研究

研究了炭纤维织物/环氧(CF/EP)复合材料与45#钢在环-环端面干摩擦状态下的摩擦磨损特性,考查了制备工艺和MoS2与石墨不同配比等对CF/EP复合材料干摩擦性能的影响,采用扫描电子显微镜观察复合材料及其偶件磨损表面形貌.结果表明:半干法制备的环氧树脂体积分数为40%的CF/EP复合材料的摩擦系数稳定;纯CF/EP复合材料主要表现为粘着磨损特性;MoS2与石墨改性后复合材料摩擦磨损性能明显改善,质量比为1.5∶1的MoS2与石墨改性CF/EP复合材料具有最佳的摩擦磨损性能,其稳态摩擦系数为0.14～0.15,磨损量3.15×10-5 mg/r.     

手机虹膜识别镜头设计

随着近年来图像传感器的快速商用化以及生物识别算法的发展,虹膜识别功能得以应用于移动终端设备。获取虹膜图像是虹膜识别的关键一步,运用ZEMAX光学设计软件设计了一款适用于手机的虹膜识别镜头。该镜头采用豪威科技公司OmniVision_OV2281传感器,采用三片式非球面光学塑料设计,F数为2.3,全视场角为34°,在1/2奈奎斯特频率220 lp/mm处MTF值均大于0.39,且系统总长仅3 mm。根据ZEMAX像质评价方法以及公差分析结果可知,该镜头各项光学指标优良,具有像质好、体积小,质量轻、价格低、容易加工等特点。     

理想弹塑性固体Riemann问题的解结构与初值条件

针对理想弹塑性固体材料的一维Riemann问题,在不考虑真空的情况下,讨论其所有可能存在的解结构,给出每一种解结构下对应的初值条件且证明该系列初值条件的完备性,即任意给定的物理量初值均有且只有一种解结构与之对应.基于该理论,在设计精确或近似理想弹塑性Riemann问题求解器时,可以依据初值条件对任意物理量初值直接判断其对应的解结构,从而提高求解器的精度和效率.数值试验验证了该系列初值条件的正确性和有效性.     

水分子在氢化锂表面的吸附行为

运用理论分析方法计算研究了水分子在氢化锂表面的吸附行为,分析了氢化锂表面改性对其疏水性能的影响。结果表明,在LiH-111面和LiH-100面上构建槽结构、柱状结构后,水分子在其上的吸附力比完整表面更强,说明表面微结构的引入的确改变了势能分布。壁相交处存在势能叠加,加强了吸附水分子的能力,但是没有引起表面的亲水性能变化。水分子可以稳定的吸附在完美的LiH（001）表面,其解离能垒仅为0.386 eV,这一解离反应在室温下完全可以进行。水分子极易在具有结构缺陷的LiH表面解离,这是LiH在一定湿度的空气和水环境中极易分解的根本原因。     

Geometric dynamic recrystallization of austenitic stainless steel through linear plane-strain machining

ABSTRACT

Type 316L austenitic stainless steel was severely plastically deformed at room temperature using linear plane-strain machining in a single pass that imparted shear strains up to 2.2 at strain rates up to 2?×?10³ s^?1. The resulting microstructures exhibited significant grain size refinement and improved mechanical strength where geometric dynamic recrystallization was identified as the primary microstructural recrystallization mechanism active at high strain rates. This mechanism is rarely observed in low to medium stacking fault energy materials. The critical stress required for twin initiation is raised by the combined effects of refined grain size and the increase in stacking fault energy due to the adiabatic heating of the chip, thus permitting geometric dynamic recrystallization. The suppression of martensite formation was observed and is correlated to the significant adiabatic heating and mechanical stabilisation of the austenitic stainless steel. A gradient of the amount of strain induced martensite formed from the surface towards the interior of the chip. As the strain rate is increased from 4?×?10² s^?1–2?×?10³ s^?1, a grain morphology change was observed from a population of grains with a high fraction of irregular shaped grains to one dominated by elongated grain shapes with a microstructure characterised by an enhanced density of intragranular sub-cell structure, serrated grain boundaries, and no observable twins. As strain rates were increased, the combination of reduction in strain induced martensite and non-uniform intragranular strain led to grain softening where a Hall-Petch relationship was observed with a negative strengthening coefficient of ?0.08?MPa m^1/2.     

A thermochemical instability. II. Inhomogeneous fluctuations

The behavior of coupled stochastic fields near a cusp bifurcation is studied. The results are applied to a thermochemical model and the possibility of observing nonclassical critidal behavior is discussed.     

Response of an elastic Bingham fluid to oscillatory shear

The response of an elastic Bingham fluid to oscillatory strain has been modeled and compared with experiments on an oil-in-water emulsion. The newly developed model includes elastic solid deformation below the yield stress (or strain), and Newtonian flow above the yield stress. In sinusoidal oscillatory deformations at low strain amplitudes the stress response is sinusoidal and in phase with the strain. At large strain amplitudes, above the yield stress, the stress response is non-linear and is out of phase with strain because of the storage and release of elastic recoverable strain. In oscillatory deformation between parallel disks the non-uniform strain in the radial direction causes the location of the yield surface to move in-and-out during each oscillation. The radial location of the yield surface is calculated and the resulting torque on the stationary disk is determined. Torque waveforms are calculated for various strains and frequencies and compared to experiments on a model oil-in-water emulsion. Model parameters are evaluated independently: the elastic modulus of the emulsion is determined from data at low strains, the yield strain is determined from the phase shift between torque and strain, and the Bingham viscosity is determined from the frequency dependence of the torque at high strains. Using these parameters the torque waveforms are predicted quantitatively for all strains and frequencies. In accord with the model predictions the phase shift is found to depend on strain but to be independent of frequency.Notation A plate strain amplitude (parallel plates) - A _R plate strain amplitude at disk edge (parallel disks) - G elastic modulus - m torque (parallel disks) - M normalized torque (parallel disks) = 2m/R ³₀ - N ratio of viscous to elastic stresses (parallel plates) =µ A/ ₀ ratio of viscous to elastic stresses (parallel disks) =µ A _R/₀ - r normalized radial position (parallel disks) =r/R - r radial position (parallel disks) - R disk radius (parallel disks) - t normalized time = t — /2 - t time - _E elastic strain - _P plate strain (displacement of top plate or disk divided by distance between plates or disks) - _PR plate strain at disk edge (parallel disks) - ₀ yield strain - _E normalized elastic strain = _E/₀ - _P normalized plate strain = _P/₀ - _PR normalized plate strain at disk edge (parallel disks) = _PR/₀ - ₀ normalized plate strain amplitude (parallel plates) =A/ ₀ — normalized plate strain amplitude at disk edge (parallel disks) =A _R/₀ - phase shift between _P andT (parallel plates) — phase shift between _PR andM (parallel disks) - µ Bingham viscosity - stress - ₀ yield stress - T normalized stress =/ ₀ - frequency