关 键 词：

三维PROE 45 吨旋挖 钻机 驱动 链轮 设计 三维 PROE 10 PDF 图纸 CAD 制图 文档

资源描述：

喜欢这套资料就充值下载吧。。。资源目录里展示的都可预览。。。下载后都有，，请放心下载，，文件全都包含在内，，【下载后加 QQ:1064457796或1304139763,免费领CAD格式图纸】 ================================================= 喜欢这套资料就充值下载吧。。。资源目录里展示的都可预览。。。下载后都有，，请放心下载，，文件全都包含在内，，【下载后加 QQ:1064457796或1304139763,免费领CAD格式图纸】

内容简介：

湘潭大学兴湘学院毕业论文（设计）任务书论文（设计）题目： 45吨旋挖钻机驱动轮和拖链轮设计 学号： 2006183810 姓名： 龚创先 专业： 机械设计与制造及其自动化 指导教师： 周友行 系主任： 周友行 一、主要内容及基本要求主要内容： 1、熟悉履带行走装置的结构和行走原理，并与本组其他同学一起确定履带总体方案； 2、设计和计算驱动轮、液压马达和拖链轮相关参数（包括驱动轮的选型、拖链轮的选型和液压马达的型号）； 3、绘制具体的驱动轮、驱动轮与液压马达的CAD装配图、拖链轮非标准件零件CAD图以及拖链轮CAD装配图； 4、用PROE建立驱动轮和液压马达的三维模型、拖链轮的三维模型以及拖链轮非标准件的三维模型。 基本要求： 1、设计说明书一份； 2、提交CAD图纸；（驱动轮、驱动轮和液压马达装配图、拖链轮非标准件零件图和拖链轮装配图） 3 、提交PROE三维模型。（驱动轮与液压马达的装配图和零件图，拖链轮的装配图和零件图） 二、重点研究的问题 通过比较轮式行走装置与履带式行走装置比较的特点，确定行走装置方案为履带行走装置；根据履带行走装置基本参数，确定了履带行走装置主要部件“四轮一带”的型号，并完成“四轮一带”结构设计；完成了履带行走装置PRO/E三维图建模，并对进行干涉检测，以确定其结构的合理性和可行性。 三、进度安排序号各阶段完成的内容完成时间1查阅旋挖钻机相关资料第一周2查阅履带行走装置驱动轮和拖链轮资料第二周3确定整体大略方案第三周4确定驱动轮、拖链轮和液压马达选型第四周5履带行走装置基本参数确定第五、六周6CAD图纸绘制第七到第九周7PROE三维建模第十周到第十一周8制作设计说明书第十二周四、应收集的资料及主要参考文献（一）应收集的资料： 旋挖钻机行走装置的相关资料及与之相近的其他类型的工程机械相关资料。 （二）主要参考文献： 1.机械设计手册联合编写组编 .机械设计手册（上册） 第一分册 (第二版) M .化学 工业出版社,1979年10月北京第2版. 2.周良德 杨世平 等编著.现代工程图学M. 北京：化学工业出版社，2006.9. 3.吴庆鸣，何小新主编.工程机械设计M. 武汉：武汉大学出版社，2006.4 . 4.廖念钊等编著.互换性与技术测量M.北京：中国计量出版社，2007.6. 5.同济大学.液压挖掘机M.北京：中国建筑工业出版社，1986. 6.JB/T 2984.1-2001,履带式推土机拖链轮.中国机械工业联合会.发布中国标准出版 社. 2001-10-01实施. 7.JB/T 2984.4-1999,履带式推土机驱动轮齿块.中国机械工业局发布.中国机械行 业标准. 8.GB/T9140-1996，液压挖掘机结构与性能. 北京：中国标准出版社. 2009.4. Erosion wear of laminated ceramic nozzlesDeng Jianxin*, Liu Lili, Zhao Jinlong, Sun JunlongDepartment of Mechanical Engineering, Shandong University, Jinan 250061, Shandong Province, PR ChinaReceived 31 March 2006; accepted 30 June 2006AbstractSiC/(W,Ti)C ceramic nozzles with laminated structures were produced by hot pressing in order to reduce the tensile stress at the entryand exit region of the nozzle. Finite element method was used to evaluate the residual stresses due to the different thermal expansioncoefficients and shrinkage of the SiC and (W,Ti)C solidsolution during the sintering process of the composite. The erosion wear ofthe laminated ceramic nozzle was assessed by sand blasting; the results were compared with those obtained with an unstressed referencenozzle with the same composition. The experimental results have shown that the laminated ceramic nozzles have superior erosion wearresistance to that of the homologous stress-free nozzles.? 2006 Elsevier Ltd. All rights reserved.Keywords: Nozzles; Ceramic materials; Laminated materials; SiC1. IntroductionSand blasting treatment is an abrasive machining pro-cess and is widely used for surface strengthening 1, surfacemodification 2, surface clearing and rust removal 3,4,etc. It is suitable for the treatment of hard and brittle mate-rials, ductile metals, alloys, and nonmetallic materials. Inthe sand blasting process, a very high velocity jet of fineabrasive particles and carrier gas coming out from a nozzleimpinges on the target surface and erodes it. The fine par-ticles are accelerated by the gas stream, commonly com-pressed air at a few times atmospheric pressure. Theparticles are directed towards the surfaces to be treated.As the particles impact the surface, they cause a small frac-ture, and the gas stream carries both the abrasive particlesand the fractured particles away. The nozzle is the mostcritical part in the sand blasting equipment. There aremany factors that influence the nozzle wear such as: themass flow rate and impact angle 57, the erodent abrasiveproperties 810, the nozzle material and its geometry1116, and the temperatures 17,18. Ceramics, beinghighly wear resistance, have great potential as the sandblasting nozzle materials.Several studies 11,15 have shown that the entry area ofa ceramic nozzle exhibited a brittle fracture inducedremoval process, while the center area showed plowingtype of material removal mode. As the erosive particleshit the nozzle at high angles (nearly 90?) at the nozzle entrysection in sand blasting (see Fig. 1), the nozzle entry regionsuffers form severe abrasive impact, which may cause largetensile stresses. The highest tensile stresses are located atthe entry region of the nozzle. Thus, the erosion wear ofthe nozzle entry region is always serious in contrast withthat of the center area 11,15.Laminated hybrid structures constituted by alternatelayers of different materials can be properly designed toinduce a surface compressive residual stress leading to animproved surface mechanical properties and wear resis-tance 1922. Residual stresses arise from a mismatchbetween the coefficients of thermal expansion (CTE), sin-tering rates and elastic constants of the constituent phasesand neighbouring layers, and the residual stress fielddepends on the geometry of the layered structure and onthe thickness ratio among layers 2326. Toschi 220263-4368/$ - see front matter ? 2006 Elsevier Ltd. All rights reserved.doi:10.1016/j.ijrmhm.2006.06.005*Corresponding author. Tel.: +86 531 88392047.E-mail address: jxdeng (D. Jianxin)./locate/ijrmhmInternational Journal of Refractory Metals & Hard Materials 25 (2007) 263270et al. reported that laminated hybrid structures canimprove the sliding wear resistance of alumina. Portu 27et al. showed that laminated structures with compressiveresidual stresses within the surface regions was a suitableway to obtain composite materials with superior tribologi-cal properties. Deng et al 28. showed that gradient cera-mic nozzle exhibited high wear resistance over commonceramic nozzles.In the present study, SiC/(W,Ti)C ceramic nozzles withlaminated structures were produced by hot pressing in orderto reduce the tensile stress at the entry and exit region of thenozzle. The residual stress of the laminated nozzle duringthe sintering process was calculated by means of the finiteelement method. The erosion wear of the laminated ceramicnozzles was investigated in comparison with an unstressedreference nozzle with the same composition.2. Materials and experimental procedures2.1. Preparation of SiC/(W,Ti)C laminated ceramicnozzle materialsThe starting materials were (W,Ti)C solidsolution pow-ders with average grain size of approximately 0.8 lm, pur-ity 99.9%, and SiC powders with average grain size of1 lm, purity 99.8%. Six different volume fractions of(W,Ti)C (55, 57, 59, 61, 63, 65 vol.%) were selected indesigning the SiC/(W,Ti)C laminated nozzle material witha six-layer structure. The compositional distribution of thelaminated ceramic nozzle materials is shown in Fig. 2. It isindicated that the compositional distribution of the lami-nated nozzle materials changes in nozzle axial direction.As the heat conductivity of SiC is higher than that of(W,Ti)C solidsolution, while its thermal expansion coeffi-cient is lower than that of (W,Ti)C, the layer with the high-est volume fraction of SiC was put both in the entry layerand in the exit layer (see Fig. 2(a). The homologous stress-free nozzle with no compositional change is shown in Fig. 2(b). The ceramic nozzle laminated both in entry and exitarea is named GN-3, while the stress-free nozzle is namedCN-2.SixSiC/(W,Ti)Ccompositepowdersofdifferentmixture ratios were prepared by wet ball milling in alco-hol with cemented carbide balls for 80 h respectively.Following drying, the mixtures composite powders withdifferent mixture ratios were laminated into the mouldin turn. The sample was then hot-pressed in flowingnitrogenfor40 minat1900 ?Ctemperaturewith30 MPa pressure.Fig. 1. Schematic diagram of the interaction between the erodent particleand the nozzle in sand blasting processes.Fig. 2. Compositional distribution of (a) the SiC/(W,Ti)C ceramic nozzle laminated both in entry and exit area (GN-3), (b) the homologous stress-freenozzles (CN-2).264D. Jianxin et al. / International Journal of Refractory Metals & Hard Materials 25 (2007) 2632702.2. Sand blasting testsFig. 3 shows the schematic diagram of the abrasive air-jet machine tool (GS-6 type), which consists of an air com-pressor, a blasting gun, a control valve, a particle supplytube, a filter, a desiccator, an adjusting press valve, a dustcatcher, an abrasive hopper, and a nozzle. The air and gritflow adjusting was controlled by the valves and regulators.The gas flow rate is controlled by the compressed air, andthe abrasive particle velocity through the nozzle is adjustedto 60 m/s.The erodent abrasives used in this study were of siliconcarbide (SiC) powders with 50150 lm grain size. TheSEM micrograph of the SiC powders used for the dry sandblasting is shown in Fig. 4.Nozzles with internal diameter 8 mm and length 30 mmmade from SiC/(W,Ti)C laminated structure (GN-3) andstress-free structure (CN-2) were manufactured by hot-pressing as can be seen in Fig. 5.The mass loss of the worn nozzles was measured with anaccurate electronic balance (minimum 0.1 mg). All the testconditions are listed in Table 1. The erosion rates (W) ofthe nozzles are defined as the nozzle mass loss (m1) dividedby the nozzle density (d) times the mass of the erodentabrasive particles (m2):Fig. 3. Schematic diagram of the sand blasting machine tool (1) aircompressor, (2) control valve, (3) filter, (4) desiccator, (5) press adjustingvalve, (6) dust catcher, (7) blasting gun, (8) abrasive hopper, (9) ceramicnozzle).Fig. 4. SEM micrograph of the SiC abrasives used for sand blasting.Fig. 5. Photo of the GN-3 laminated ceramic nozzles.Table 1Sand blasting test conditionsSand blasting equipmentGS-6 type sand blasting machine toolNozzle materialGN-3 laminated nozzle CN-2stress-free nozzleDimension of nozzleU8 mm (internal diameter) 30 mm (length)Erodent abrasives50150 lm SiC powdersCompressed air pressure0.4 MPaCumulative mass weighAccurate electronic balance(minimum 0.1 mg)Table 2Hardness of different layers of the laminated nozzle materialsLayer(W,Ti)C content (vol.%)Vickers hardness Hv (GPa)15526.8925726.5235925.9346125.7056324.6766524.15D. Jianxin et al. / International Journal of Refractory Metals & Hard Materials 25 (2007) 263270265W m1=d:m21where the W has the units of volume loss per unit mass(mm3/g).The finite element method (FEM) was used as a meansof numerically evaluating the residual stress and its distri-bution of the laminated ceramic nozzle in the fabricatingprocesses.For observation of the micro-damage and determinationof erosion mechanisms, the worn nozzles were sectionedaxially. The eroded bore surfaces of the nozzles were exam-ined by scanning electron microscopy.Fig. 6. SEM micrographs of each polished layer of the GN-3 laminated ceramic nozzle material (a) the first layer (entry zone), (b) the second layer, (c) thethird layer, (d) the fourth layer, (e) the fifth second layer, and (f) the sixth layer.Fig. 7. Distribution of (a) the axial (rz), (b) the radial (rr), and (c) the circumferential (rh) residual stresses in the GN-3 laminated nozzle in fabricatingprocess.266D. Jianxin et al. / International Journal of Refractory Metals & Hard Materials 25 (2007) 2632703. Results and discussion3.1. Microstructural characterization and propertiesof the laminated nozzle materialsHardness measurements were performed by placingVickers indentations on every layer of the cross-sectionalsurface of GN-3 laminated nozzle material. The indenta-tion load was 200 N and a minimum of three indentationswere tested for each layer. The Vickers hardness (GPa) ofeach layer is given byHv 1:8544P2a22where P is the indentation load (N), 2a is the catercornerlength (lm) due to indentation. Hardness of each layerof the GN-3 laminated nozzle material is presented inTable 2.SEM micrographs of each polished layer of GN-3 lami-nated ceramic nozzle material are shown in Fig. 6. Theblack areas were identified by EDX analysis as SiC, andthe white phases with clear contrast were (W,Ti)C. It canbe seen that the SiC particles are quite uniformly distributedthroughout the microstructure, porosity is virtually absent.3.2. Residual stress at the laminated nozzlesThe residual stress of the laminated ceramic nozzle in thefabricating process was calculated by means of the finite ele-ment method by assuming that the compact is cooled fromsintering temperature 1900 ?C to room temperature 20 ?C.Thermo-mechanical properties of (W,Ti)C and SiC are asfollows:W;TiC : E 480 GPa; m 0:25; a 8:5 ? 10?6K?1;k 21:4 W=m K:SiC : E 450 GPa; m 0:16; a 4:6 ? 10?6K?1;k 33:5 W=m K:Owing to the symmetry, an axisymmetric calculationwas preferred. Presume that it was steady state boundaryconditions. The results of the distribution of the axialFig. 8. (a) The axial (rz), (b) the radial (rr), and (c) the circumferential (rh) residual stresses in the GN-3 laminated nozzle in fabricating process at differentposition along the axial direction of the nozzle.D. Jianxin et al. / International Journal of Refractory Metals & Hard Materials 25 (2007) 263270267(rz), the radial (rr), and the circumferential (rh) residualstresses calculated by FEM in the GN-3 laminated nozzlein cooling process from sintering temperature to room tem-perature are showed in Fig. 7. It is obvious that an excesscompressive residual stress is formed both at the entry andthe exit region of the GN-3 laminated nozzle. Fig. 8 showsthe axial (rz), the radial (rr), and the circumferential (rh)residual stresses in GN-3 laminated nozzle at different posi-tion along its axes. It in indicated that rz, rr, and rhresid-ual stress both at the entry zone and at the exit zone iscompressive, and the maximum value is ?94.003 MPa,?130.949 MPa, and ?265.368 MPa respectively. There-fore, laminated structures in ceramic nozzles can form anexcess compressive residual stresses at the entry and exitregion of the nozzle during fabricating process.3.3. Erosion wear of the laminated nozzleThe erosion wear of the GN-3 laminated ceramic nozzlewas assessed in comparison with the CN-2 stress-free cera-mic nozzle by sand blasting. Fig. 9 shows the cumulativemass loss of the GN-3 and CN-2 nozzles in sand blastingprocesses. It can be seen that the cumulative mass loss con-tinuously increased with the operation time. Comparedwith GN-3 laminated nozzle, the CN-2 stress-free nozzleshowed higher cumulative mass loss under the same testconditions.The worn ceramic nozzles were cut after operation inlongitudinal directions for failure analysis. Fig. 10 showsthe photos of the inner bore profile of the GN-3 andCN-2 nozzles after 540 min operation. It is showed thatinner bore diameter of the worn CN-2 nozzle along thenozzle longitudinal directions is larger than that of theworn GN-3 laminated nozzles, especially at the nozzleentry region.The results of the nozzle entry bore diameter variationwith the erosion time of for GN-3 and CN-2 nozzles areshown in Fig. 11. It is indicated that the entry bore dia-meter enlarges greatly with the operation time for CN-2stress-free nozzle. While the entry bore diameter increasesslowly with the operation time for GN-3 laminated nozzle.Fig. 12 shows the comparison of the erosion rates for GN-3and CN-2 nozzles in sand blasting processes. It is obviousthat the erosion rate of the stress-free nozzles is higherthan that of the laminated nozzles. Therefore, it is appar-ently that the GN-3 laminated nozzles exhibited higher ero-sion wear resistance over the CN-2 stress-free nozzle underthe same test conditions.Fig. 9. Cumulative mass loss of the GN-3 laminated nozzle and the CN-2stress-free nozzle in sand blasting processes.Fig. 10. Photos of the worn inner bore profile of (a) the GN-3 laminated nozzle, (b) the CN-2 stress-free nozzle after 540 min operation.Fig. 11. Nozzle entry bore diameter variation with the erosion time for theGN-3 laminated nozzle and the CN-2 stress-free nozzle in sand blastingprocesses.268D. Jianxin et al. / International Journal of Refractory Metals & Hard Materials 25 (2007) 263270Fig. 13 shows the SEM micrographs of the entry boresurface of the worn CN-2 stress-free nozzle. From theseSEM micrographs, different morphologies and fracturemodes of the nozzles can be seen clearly. The CN-2stress-free nozzle at the entry area failed in a highly brittlemanner, and exhibited a brittle fracture induced removalprocess. There are a lot of obvious pits located on the noz-zle bore surface indicating that brittle fracture took place.Characteristic SEM pictures taken on the eroded entrybore surface of the GN-3 laminated ceramic nozzle areshown in Fig. 14. It is shown that the appearance of theeroded areas of the laminated nozzle showed a relativesmooth surface by contrast with that of the stress-freenozzle.Ceramic nozzle failure by erosion wear is generallycaused by fracture owing large the tensile stress at the noz-zle entry zone 1115. Because the nozzle entrance regionsuffers form severe abrasive impact, and generates largetensile stress, which may cause the subsurface lateral cracksand facilitates removal of the material chips. Thus, the ero-sion wear of the nozzle depends on the stress distribution inthe entry region. Once the maximum tensile stress exceedsthe ultimate strength of the nozzle material, fracture willoccur.The higher erosion wear resistance of the GN-3 lami-nated nozzle compared with that of the CN-2 stress-freenozzle can be analysed in terms of the formation of com-pressive residual stresses both on the entry area and onthe exit region. As calculated above, compressive residualFig. 12. Comparison of the erosion rate of the GN-3 laminated nozzle andthe CN-2 stress-free nozzle in sand blasting processes.Fig. 13. SEM micrographs of the entry bore surface of the worn CN-2 stress-free ceramic nozzle.Fig. 14. SEM micrographs of the entry bore surface of the worn GN-3 laminated ceramic nozzle.D. Jianxin et al. / International Journal of Refractory Metals & Hard Materials 25 (2007) 263270269stresses were formed at the entry and exit region of theGN-3 laminated nozzle in fabricating process from sinter-ing temperature to room temperature, which may partiallycounteract the tensile stresses in the nozzle entry and exitsection resulting from external loadings. This effect maylead to the increase in resistance to fracture, and thusincrease the erosion wear resistance of the laminatednozzle.4. ConclusionsSiC/(W,Ti)C laminated ceramic nozzles were producedby hot pressing. The purpose is to reduce the tensile stressat the entry and exit area of the nozzle during sand blastingprocesses. Particular attention was paid to the erosion wearof this kind laminated ceramic nozzle. Results showed thatthe laminated ceramic nozzles have superior erosion wearresistance to that of homologous stress-free ceramic nozzle.The mechanism responsible was explained as the formationof compressive residual stresses both at the entry area andat the exit region of the laminated ceramic nozzle in fabri-cating process, which may partially counteract the tensilestresses resulting from external loadings. Laminated struc-ture in ceramic nozzles is an effective way to improve theerosion wear resistance of the stress-free ceramic nozzles.AcknowledgementsThis work was supported by the National NaturalScience Foundation ofChina(50475133), Specialized Re-search Fund for Doctoral Program of Higher Education(20030422105), Natural Science Foundation of Shan-dong Province (Y2004F08), and the Program for NewCentury Excellent Talents in University (NCET-04-0622).References1 LiGuoying.Surfaceengineering. Beijing: MechanicalIndustryPublishing House; 1998.2 Deng Jianxin, Lee Taichiu. Techniques for improved surface integrityand reliability of machined ceramic composites. Surface Engineering2000;16(5):4114.3 Raykowski A, Hader M. Blasting cleaning of gas turbine compo-nents: deposit removal and substrate deformation. Wear 2001;249:12732.4 Djurovic B, Jean E. Coating removal from fiber composites andaluminum using starch media blasting. Wear 1999;224:2237.5 Oka YI, Ohnogi H. The impact angle dependence of erosion damagecaused by solid particle impact. Wear 1997;203204:5739.6 Finnie I, Stevick GR, Ridgely JR. The influence of impingementangle on the erosion of ductile metals by angular abrasive particles.Wear 1992;152:917.7 Wellman RG, Allen C. The effect of angle of impact and materialproperties on the erosion rates of ceramics. Wear 1995;186187:11723.8 Srinivasan S, Scatterrgood RO. Effect of erodent hardness on erosionof brittle materials. Wear 1988;128:13952.9 Shipway PH, Hutchings IM. The influence of particle properties onthe erosive wear of sintered boron carbide. Wear 1991;149:8598.10 Bahadur S, Badruddin R. Erosion particle characterization and theeffect of particle size and shape on erosion, Proceedings of theinternational conference on wear of materials, ASME, New York,(1989): 14353.11 Deng Jianxin. Erosion wear of boron carbide nozzles by abrasive air-jets. Materials Science Engineering A 2005;408(12):22733.12 Deng Jianxin, Feng Yihua, Ding Zeliang. Wear behaviors of theceramic nozzles in sand blasting treatments. Journal of the EuropeanCeramic Society. 2003;23:3239.13 Deng Jianxin, Zhang Xihua, Niu Pingzhang, et al. Wear of ceramicnozzles by dry sand blasting. Tribology International 2006;39(3):27480.14 Deng Jianxin. Sand erosion performance of B4C/(W,Ti)C ceramicblasting nozzles. Advances in Applied Ceramics 2005;104:5964.15 Deng Jianxin, Zheng Zhongc