Search results

It can be seen that both the NTE and TE specimen are bi-modal microstructure, consisting of equiaxed primary α phase (αp) in a lamellar α+β matrix (transformed β phase, βT), for which the volume fraction of αp phase is about 20%, and average grain size of the αp phase is about 15 µm.
Plotted in the figure are the cyclic stress amplitude vs. the number of cycles at different constant total strain ranges, typically being ±0.45%, ±0.50%, ±0.60%, ±0.70%, ±0.80% and ±1.00%.
The total strain amplitude as a function of the cyclic number to failure for the NTE specimens and the TE specimens are plotted in Fig. 4.
For instance, the cyclic number to failure of the NTE specimen and the TE specimen, within a constant total strain amplitude ±0.60%, are 2114 and 3688, respectively.
From Fig. 6 (a) and (b), it can be noticed that "A", "B" and "C" are the fatigue failure originated region, the crack propagation region and the final rupture region, 100 10 1 10 2 103 10 4 10 5 600 650 700 750 800 850 900 950 1000 1050 1100 1.00 0.80 0.70 0.60 0.50 0.45 Cyclic Stress Amplitude/MPa *umber of Cycles, � TE ± ∆εt /2 (%) 10 0 10 1 10 2 10 3 10 4 10 5 600 650 700 750 800 850 900 950 1000 1050 1100 NTE ± ∆εt /2 (%) 1.00 0.80 0.70 0.60 0.50 0.45 Cyclic Stress Amplitude/MPa *umber of Cycles, � Fig. 3 Stress response to cyclic straining of Ti600 alloy before and after thermal exposure (a) NTE; (b) TE (a) (b) 10 2 10 3 104 105 0.3 0.4 0.5 0.6 0.7 0.8 0.9 1.0 1.1 Total strain amplitude, ∆∆∆∆εεεεt/2 /% Cyclic number to failure, �f NTE TE Fig. 4 Fatigue life curves of Ti600 alloy before and after thermal exposure respectively.

As a material removal process, there are two key factors in the grinding process to affect the surface performance: the geomorphology of the wheel and the chip formation process involved[3], which considers the interaction of the workpiece surface and the abrasive grains.
But in super-high speed(SHS) grinding process, the number of particles involved in interaction is much more than that in common grinding, which makes the surface performance become better after grinding in theory because of more particles joining in machining.
Fig.1 The layout of point grinding Fig.2 Contact area with α Table1 The explanation for the parameters in the paper α swivel angle between wheel axis and workpiece axis ds diameter of wheel dw diameter of workpiece de equivalent diameter of wheel lc length of contact arc ap depth of cutting b contact width in theory br contact width in actual A contact area between wheel and workpiece h thickness of chip f(h) statistical distribution of thickness of chip K revised coefficient Ra surface roughness E(Ra) expectation of roughness ha average thickness of chip vw speed of workpiece vs speed of wheel C number of particles in the unit of area r ratio between width and thickness of chip In the process of grinding, the contact zone between the wheel and the workpiece has been assumed to a rectangle include the width and the length, which are indicated by the contact width and the length of contact arc between the wheel
The effective particles of joining in cutting becomes more than common cylindrical grinding, which makes the more number of particles interfere to the removal material of the workpiece to decrease the distance between the peak and the valley in the unit time.
The surface quality has been improved in theory based on the number of cutting from effective particles in SHSP grinding while grinding in the same wheel speed and other factors compared to SHS grinding.

Most of these tailings are fine-grained residues with low copper content (0.1-0.8%) and include toxic compounds, such as heavy metals, arsenic, and flotation reagents, amongst others.
A similar decrease in cell numbers has been previously reported [15].
Key: (▲) copper soluble in the offline trap, (■) numbers of planktonic-phase microorganisms and (●) glycerol in the sulfidogenic vessel.

It results in lowered surface roughness, higher compressive residual stress, better grain refinement, increased surface hardness, and enhanced corrosion resistance.
Shot peening results in hardening of the surface by generating large number of dislocations, induces near-surface residual compressive stress (RCS), introduces severe plastic deformation (SPD) and roughens the surface [12, 16, 17].
It was observed that adding lower shot intensity at the second stage and the third stage for SP4 resulted in improved refinement in grain.
The key factors causing the increase in hardness are residual compressive stress, grain refinement, and micro strain [27].

., can also be based on the intensity of the diffraction pattern and quantitatively determining the shape of the material content of the respective phases, grain size, degree of crystallization, the size of the micro and macro stress magnitude of stress and the like.
The surface of the heat-treated bituminous 1700℃ ~ 2200℃ appear worm-like extension of the basic structural unit having a large degree of orientation increased significantly, but there are still a large number of pits, the development of the crystal structure is not very complete.
heat treatment temperature in 2400℃；a7：SEM of the bitumite under heat treatment temperature in 2600℃；b1：SEM of the anthracite；b2：SEM of the anthracite under heat treatment temperature in 1400℃；b3：SEM of the anthracite under heat treatment temperature in 1700℃；b4：SEM of the anthracite under heat treatment temperature in 2000℃；b5：SEM of the anthracite under heat treatment temperature in 2200℃；b6：SEM of the anthracite under heat treatment temperature in 2400℃；b7：SEM of the anthracite under heat treatment temperature in 2600℃) As can be seen from Figure 3b2 ~ Figure 3b7, when the heat treatment temperature increased from 1400℃ to 2600℃ during the more obvious changes in morphology anthracite, anthracite outer heat-treated 1400℃ ~ 1700℃ entire large particle surface becomes relatively smooth surface formation of a more fine fused defects and the formation of more small filamentous crystallites. 1700℃ ~ 2200℃ heat-treated anthracite large particles beginstraight smooth surface, reducing the number
of particles of microcrystalline, orientation increased significantly, began to develop grow, forming irregular graphite crystals. 2200℃ ~ 2600℃ heat-treated grain anthracite graphitization further development grew, and tends to complete, and significantly reduce crystal defects, grain thickness was thinner, forming an ideal flat graphite crystal.

The cell adhesion test showed that the cell number of vascular endothelial in the austenitic stainless steel was more than the titanium alloy materials, and the cells grow in good condition.
The total numbers of adhered platelets were counted.
The grain is 5～6 grade.
Fig.5 Platelets adhesion number comparison between high nitrogen nickel-free austenitic stainless steel and titanium alloy,*, significant difference (P<0.05), **, extremely significant difference (P<0.01) Hemolysis rate test.
The platelets adhesion number was little and had no obvious gathered phenomenon, which indicated that the materials in this experiment had good biocompatibility.

This bistability is replaced in the (NAg,NCu,P,T) ensemble by a continuous evolution of both the structure and the concentration of the (001) facets from Cu-rich square-shaped to Ag-rich diamond-shaped facets as the number of Ag atoms increases.
These potentials have been quite successful in the calculation of surface (dense and vicinal) [5,10], grain boundary [11] and cluster [12] properties of metals and alloys.
A standard Metropolis algorithm is used [13] and the averages are evaluated over 5.105 MC macrosteps, a similar number of macrosteps being used to reach equilibrium.
A MC macrostep corresponds to propositions of random atomic displacement and propositions of individual chemical switch in the p-GC ensemble, or propositions of atomic exchange between heteroatomic pairs in the C ensemble, being the total number of atoms and the number of minority atoms (I = Cu, Ag).
To elucidate this unexpected result, we plot in Fig. 2b the evolution of the couple of angles (see Fig. 1a) as a function of the number of MC steps for a (001) facet concentration close to 0.5, i.e. in the bistability domain of the p-GC ensemble.

While the EB-PVD TBCs often exhibit columnar grain characteristic, the inner finer sub-grains are arranged in the coarse columnar grains.
The major axis of the columnar grain is often parallel to the thermal flux direction which is not beneficial to decrease the effective thermal conductivity of the TBCs.
The number of the micro-pores of DCL LZ/YSZ TBCs did not exhibit evident decrease tendency which is attributed to its excellent sintering resistance ability of the LZ layer at high temperature.
The number of the micro-pores of the DCL LZ/YSZ TBCs still did not show evident decrease tendency which is attributed to its super sintering resistance ability at high temperature[35].

The micrograph picture of the material Fe1.5Cr0.2Mo sintered steel with the pyrohydrolysis treatment (Fig. 4) shows a uniform, homogeneous fine-grained ferrite and pearlite microstructure.
Increase of wear rate is smallest, for load cycles number NL = 1,5×106 is wear rate δwn = 86 mm.
Figure 14: Comparison of wear and load cycles number for different speed sliding and t =160h Figure 14 shows the comparison of wear δwn and load cycles number for different sliding speeds vgs = 0.76 m/s, 2.53 m/s and 5.05 m/s after operating time t = 160 h.
In tests with sliding speeds vgs = 0.76 m/s occur the highest wear rate for the smallest load cycles number.
The micrograph picture of the material Fe1.5Cr0.2Mo sintered steel with the pyrohydrolysis treatment shows a uniform, homogeneous fine-grained ferrite and pearlite microstructure.

AWJ subsurface, as well as common machined features such as grain deformation, possess certain characteristics linked to the AWJ process which have been less explored.
The mathematical model, presented as regression coefficients in Fig. 1 had a good experimental design with a condition number of 1.15, an excellent fit as indicated by the R2 parameter (0.900) and a very good prediction power with a high Q2 (0.817).
A fast traverse rate does not allow the jet of water to penetrate the material and minimises the number of particles that strike the material, increasing the kerf width at the bottom of the sample.
The mathematical model had a good experimental design as evaluated by the low condition number (2.28), a very good fit (R2=0.859) and good prediction power (Q2=0.572).
Acknowledgement The authors acknowledge the support of the European Commission through the 7th Framework Programme Transport (including Aeronautics) Call, Project number 234325 - ADMAP-GAS.