機械畢業(yè)設(shè)計英文翻譯---刀具磨損

1、<p><b>　　刀具磨損</b></p><p>　　為了避免金屬切削刀具失效，第三章講述了它的最低性能要求，即機械性能和耐熱性。刀具失效是指過量的磨損會導致刀具失去切削材料的能力。在本章中，文章主要講述了降低刀具磨損的累積使用特點和機制，它們是最終導致刀具被替代的因素。在現(xiàn)實生產(chǎn)實踐中，有一中表示嚴重磨損程度的連續(xù)譜，在這里沒有什么要考慮的和可能在實踐中北描述為立即失效的兩者

2、之間沒有明顯的邊界.在本章和上一章節(jié)中有重復的內(nèi)容。</p><p>　　第二章和第三種的內(nèi)容表明，金屬切削刀具比普通機床軸承表面承受更大的摩擦力、正應(yīng)力、高溫。在大部分情況下，沒有辦法避免刀具磨損，但是可以研究如何避免加速刀具磨損的方法。刀具磨損的主要因素刀具表面應(yīng)力和溫度（主要取決于金屬切削模式——車削、銑削、轉(zhuǎn)削）、刀具和工件材料、切削速度、進給量、切削深度和切削液的類型等。在第二章中，主要講述了影響刀具磨

3、損的因素的微小變化都會導致磨損的變化。機械加工中，刀具磨損方式和磨損率對金屬切削操作和切削條件的變化同樣敏感。雖然刀具磨損無法避免，但是通常情況下可以控制磨損方式來減少刀具磨損。4.1節(jié)中介紹了刀具磨損的主要方式。</p><p>　　主要介紹了機械加工的經(jīng)濟型。為了盡量減少制造成本，不僅需要尋找最合適的刀具和工件材料，而且還要考慮切削刀具壽命。在刀具壽命結(jié)束時，刀具必須能夠替換或者維修以保證加工工件的精度、表面

4、粗造度或者完整性。4.2節(jié)主要介紹了刀具壽命的標準和估算。</p><p>　　4.1刀具磨損及其分類</p><p>　　4.1.1 刀具磨損的形式</p><p>　　根據(jù)刀具磨損的程度和磨損進程，刀具磨損可分為兩類，即磨損和斷裂。磨損（如第二章討論）是一種粗糙材質(zhì)表面損失或者微接觸，或者磨粒較小，最小至分子或者原子的去除機理。它通常會持續(xù)進行直到斷裂。另一方面

5、，斷裂是比磨損更嚴重的損害，它的發(fā)生具有突然性。正如上面所說，從微磨損到嚴重斷裂是一種連續(xù)的損害。</p><p>　　圖4.1顯示了一個典型的磨損模式，在這種情況下的磨損—一把硬質(zhì)合金刀具切割處于高速旋轉(zhuǎn)下的金屬工件。月牙洼前刀面磨損，前刀面?zhèn)纫韨?cè)邊磨損和在切削深度末端的凹口磨損，它們是磨損的典型方式。磨損量可以用在4.2節(jié)中介紹的VB、KT表示。</p><p>　　然而磨損量隨著切削

6、材料、切削方式和切削條件的變化而變化，如圖4.2。如</p><p>　　圖4.2(a)顯示月牙洼和后刀面磨損存在可疑忽略的溝槽磨損，在開機后用硬質(zhì)合 金刀具切削高速旋轉(zhuǎn)的45鋼的條件下。如果改為銑削，一個有裂縫的大幅度月牙洼磨損將成為磨損的顯著特點（圖4.2（b））。當陶瓷刀具車削鎳基超級合金時（圖4.2（c）項）在美國商務(wù)部線溝槽磨損是主要的磨損模式，而月牙洼和后刀面磨損幾乎可以忽略不計。圖4.2（d）給

7、出了一個氮化硅陶瓷車削工具切削碳鋼的結(jié)果。月牙洼和后刀面磨損會在很短的時間內(nèi)磨損更大。在切削工件材料變?yōu)閎相態(tài)的情況下，大量的切削材料粘附于鈦鋁合金的K級硬質(zhì)合金刀具的側(cè)邊部分，這樣導致刀具磨損斷裂或者破碎。</p><p>　　圖4.1典型的硬質(zhì)合金刀具磨損形式</p><p>　　（a）車削45碳鋼 （b）端面銑削45碳鋼</p><

8、p>　　（c）車削鉻鎳鐵718 （d）車削45碳鋼</p><p><b>　?。╡）車削鈦合金</b></p><p>　　典型的工具損傷觀察–磨損和斷裂： (a)刀具：燒結(jié)碳化物P10， v = 150 m min–1,d = 1.0 mm,f = 0.19 mm rev–1，t = 5分鐘; (b)刀具：燒結(jié)碳化

9、物P10， v = 400 m min–1， d = 1.0 mm， f = 0.19mm tooth–1，t = 5min; (c)刀具： Al2O3/TiC陶瓷刀具，v = 100 m min–1，d = 0.5 mm，f = 0.19 mm rev–1，t = 0.5分鐘;(d)刀具：Si3N4陶瓷刀具，v = 300 m min–1，d = 1.0 mm，f = 0.19 mm rev–1，t = 1分鐘; (e)刀具：燒結(jié)碳化

10、物P10，v = 150 m min–1 d = 0.5 mm，f = 0.1 mm rev–1，t = 2 min。 </p><p>　　4.1.2 刀具磨損的原因</p><p>　　第2.4章概述了導致磨料，膠粘劑和化學磨損機理的一般條件。在刀具的磨損，這些機理的重要性和發(fā)生的條件，可以按切削溫度來劃分，如圖4.3所示。再圖上有三個刀具磨損的因素被確定，分別為機械磨損、熱磨損和化

11、學磨損。機械磨損包括腐蝕、剝落、早期斷裂和疲勞，它基本上與溫度無關(guān)。熱磨損包括塑性變形、熱擴散和作為其典型形式的化學反應(yīng)，它隨著溫度的急劇增加。 （應(yīng)當指出，熱擴散和化學反應(yīng)是不是損害的直接原因。相反，它們會導致刀具表面被削弱，使磨損，抗機械沖擊或粘連可以更容易造成材料去除。）基于粘附的磨損被觀察到有一個在一定溫度范圍內(nèi)的局部最大值。</p><p>　　圖4.3刀具磨損和切削溫度的關(guān)系</p>&

12、lt;p>　　圖4.4機械磨損的分類</p><p><b>　　(1)機械磨損</b></p><p>　　根據(jù)刀具磨損的程度和磨損進程，刀具磨損可分為兩類，即磨損和斷裂。磨損（如第二章討論）是一種粗糙材質(zhì)表面損失或者微接觸，或者磨粒較小，最小至分子或者原子的去除機理。它通常會持續(xù)進行直到斷裂。另一方面，斷裂是比磨損更嚴重的損害，它的發(fā)生具有突然性。正如上面所

13、說，從微磨損到嚴重斷裂是一種連續(xù)的損害。</p><p>　　無論機械磨損被列為磨損或斷裂，它都視磨粒的大小而定。 如圖4.4所示的幾種不同的磨粒大小模式，它們從小于0.1微米達到約100微米（遠大于100微米被視為失效）。    磨料磨損（如圖2.29示意圖）通常是由滑動對刀具硬質(zhì)顆粒的磨損造成的。硬質(zhì)顆粒無論是來自工作材料的微觀結(jié)構(gòu)，還是從切削邊緣破碎的顆粒

14、。磨料磨損減少了刀具相對于粒子和一般取決于距離的切削困難（參見4.2.2節(jié)）。</p><p>　　摩擦磨損發(fā)生在磨料顆粒比磨料磨損比較大的情況下。在刀具與工件之間相互滑動運動，并且刀具材料的顆?；蛘呔Я１荒p破壞前，刀具材料的顆?；蛘呔Я５臋C械性能被微細裂縫消弱。 接下來主要依據(jù)破碎片的大小（有時候它由于它的大小限制被稱為細微碎片）。這是由機械沖擊載荷的規(guī)模導致切削力波動大，而不是固有的波動，導致局部

15、應(yīng)力磨損。    最后斷裂顆粒比破碎顆粒大，并分為三類：早期階段、難以預(yù)測階段和最后階段。削減如果刀具形狀或切割的條件是不適當?shù)模蛘呷绻毒邇?nèi)部存在一些缺陷，或在其邊緣有缺陷，這樣刀具磨損會立即發(fā)生在開始切削工件后。不可預(yù)知的斷裂可以發(fā)生在任何時間段，如果在切削過程中刀具或者工件尖端的壓力突然發(fā)生變化，例如抖動或不規(guī)則的工件表面硬度不均勻所引起。最后階段斷裂可經(jīng)常被觀察到，特別是在銑削過程中并

16、且刀具壽命末端的時候；這些主要是有機械疲勞或者熱應(yīng)力發(fā)生在工作部件凸出部分引起的磨損。</p><p>　　(2)熱磨損—塑性變形</p><p>　　當?shù)毒咛幱诟邷厍邢鳡顟B(tài)下時，刀具尖端部分不能承受氣條件下正應(yīng)力，此時熱磨損的塑性變形將被觀察到，如圖4.3所示。因此，發(fā)生于刀具處于高溫狀態(tài)下的硬度將作為塑性變形的顯著特點。所以例如一般情況下，高速鋼刀具及鈷含量高的硬質(zhì)合金刀具或金屬陶瓷刀

17、具用于切削條件苛刻的條件下，特別是在高進給速度的情況下。因此，邊緣變形將導致生成一個不正確的形狀尺寸的工件和快速去除工件材料的情況。</p><p>　　(3)熱磨損——擴散磨損</p><p>　　熱擴散磨損的結(jié)果發(fā)生在高溫切削條件下，如果刀具和工件材料的元素會擴散到彼此對方的結(jié)構(gòu)中。這是眾所周知的硬質(zhì)合金刀具，并已被研究了多年。例如Dawihl（1941）、特倫特（1952）、Trig

18、ger和Chao（1956年）、武山和村田（1963年）、格雷戈里（1965），庫克（1973）、上原（1976）、Narutaki和山根（1976年）、Usui et al（1978）和其他科學家。</p><p>　　由擴散控制的速率與絕對溫度以指數(shù)冪的形式成正比。在磨損的情況下，不同的研究者提出了不同的指前因子的因素：庫克研究提出了擴散深度h與相應(yīng)的時間t之間的關(guān)系（公式4.1（a））；更早以前，竹山和村田

19、（1963）也研究提出了這些觀點，并且更進一步提出滑動距離可能是一個更基本的變量（方程4.1（b））；隨后Usui et al. (1978)根據(jù)接觸力學和被2.4節(jié)提及的磨損提出了磨損會隨著正接觸應(yīng)力的增加而加?。ü?.1（c））。在以上所有例子中可知，磨損率的對數(shù)與1/θ將繪制出一條直線，直線的斜率就是C2。</p><p>　　圖示4.5火山口與側(cè)面磨損率深度碳素鋼轉(zhuǎn)由P20硬質(zhì)合金,來自Kitagawa

20、(1988) 的研究</p><p>　　圖4.5顯示了月牙洼和兩個側(cè)翼的深度為0.25％碳含量處的磨損率和0.46％碳含量鋼，用P20的硬質(zhì)合金刀具驚醒切削的結(jié)果，此實驗為了驗證方程的方式（4.1c）。圖4.5中出現(xiàn)兩個線性區(qū)域，并且當1/θ≈8.5×10^(-4) K^(-1)(或(θ≈1175K)時是一個臨界點。在較高溫度斜率（((>1175 K）是鋼材和水泥之間的碳化物（庫克，1

21、973年）擴散過程的典型。在較低溫度下斜率是一個隨溫度變化的機械磨損過程的典型，例如摩擦磨損。</p><p>　　擴散可直接顯示在靜態(tài)條件下的高溫。如圖4.6顯示了一個典型靜態(tài)的擴散試驗結(jié)果，其中一個P-級硬質(zhì)合金刀具在1200攝氏度溫度下對一個0.15％碳鋼持續(xù)加載30分鐘之間通過硬質(zhì)合金刀具和鋼界面在4％Nital（一磺酸的合成酒精）蝕刻下，金相部分顯示鋼珠光體已經(jīng)從原來的水平增加。 這意味著，硬

22、質(zhì)合金中的碳已擴散到剛里面。</p><p>　　此外，電子探針顯微分析儀（EPMA）表明，鈷和鎢已從工具材料也擴散到鋼鐵中，并且是鐵鐵擴散到鋼刀具材料。 許多研究者都認為相互擴散是硬質(zhì)合金刀具擴</p><p>　　（b） 到界面的距離（um）</p><p>　　圖示4.6 典型的靜態(tài)擴散試驗結(jié)果,因為P10耦合

23、至0.15% C鋼(Narutaki和Yamane,1976年) （a）通過Nital蝕刻的接口部分;（b）通過電子探針分析元素的擴散 </p><p>　　散磨損的原因，但是沒有詳細的說明，關(guān)于這種現(xiàn)象將導致工件材料的去除效果。</p><p>　　Naerheim和遄達（1977）提出，對雙方碳化鎢鈷（金級）和WC的磨損率，（鈦，</p><p>　　鉭，鎢）的

24、C -鈷（P級）硬質(zhì)合金是由擴散速率控制鎢（和Ti和Ta）和碳原子組合成的工作的材料，如圖4.7所示。 這種觀點是基于透射電子顯微鏡（TEM）對月牙洼磨損的觀察，顯示在該工具的碳化物顆粒內(nèi)無一0.01的工具芯片接口毫米的距離的結(jié)構(gòu)變化。對與于P級比K級材料磨損較慢，這是緩慢擴散，它解釋了前者比后者的情況。Naerheim和遄達指出，在他們的切削試驗中，被拉伸碳化物顆粒并沒</p><p>　　有在粘附物

25、的底部被觀察到。這不是上原的（1976年）的經(jīng)驗。用K級或者P級含碳量為百分之47的刀具進行切削，他收集切屑，并將它溶解在酸性溶液中提取粘結(jié)的碳化物，最后讓它通過一個0.1 mm過濾嘴，通過這種方案進行分類碳化物尺寸。 用K -級刀具，他只觀察碳化物小于0.1毫米的大小，這與Trent研究結(jié)果相一致。然而，用P-級刀具，他觀察到碳化物大于0.1毫米大小。這表明K和P型材料不同的磨損機理。</p><

26、;p>　　擴散磨損的另一個例子是金剛石切割刀具、硅氮化硅陶瓷刀具和SiC晶須增韌氧化鋁陶瓷刀具在加工鋼時的嚴重磨損。 碳、硅和氮在高溫下它們都極容易擴散到鐵中，并且氮化硅和碳化硅很容易溶解于鐵水。</p><p>　　如果一個層作為擴散屏障沉積在刀具上，這樣就可以減少硬質(zhì)合金刀具的擴散磨損熱。在實際生產(chǎn)中有兩種這樣類型沉積層：一個是由涂層刀具提供;另一種是保護性氧化層沉積在切割過程中的磨損表面，用

27、于還原特殊鋼（如鈣脫氧鋼），即通常有'belag之稱的層。</p><p>　　注：文章來源Metal_Machining。</p><p>　　Tool damage</p><p>　　Chapter 3 considered cutting tool minimum property requirements (both mechanical and

28、thermal) to avoid immediate failure. By failure is meant damage so large that the tool has no useful ability to remove work material. Attention is turned, in this chapter, to the mech- anisms and characteristics of lesse

29、r damages that accumulate with use, and which eventu- ally cause a tool to be replaced. In reality, there is a continuous spectrum of damage severities, such that there is no sharp boundary betw</p><p>　　Ch

30、apters 2 and 3 have demonstrated that cutting tools must withstand much higher fric- tion and normal stresses – and usually higher temperatures too – than normal machine tool bearing surfaces. There is, in most cases, no

31、 question of avoiding tool damage, but only of asking how rapidly it occurs. The damages of a cutting tool are influenced by the stress and temperature at the tool surface, which in turn depend on the cutting mode – for

32、exam- ple turning, milling or drilling; and the cutting c</p><p>　　The economics of machining were introduced in Chapter 1. To minimize machining cost, it is necessary not only to find the most suitable too

33、l and work materials for an oper- ation, but also to have a prediction of tool life. At the end of a tool’s life, the tool must be replaced or reground, to maintain workpiece accuracy, surface roughness or integrity. S

34、ection 4.2 considers tool life criteria and life prediction.</p><p>　　4.1 Tool damage and its classification</p><p>　　4.1.1 Types of tool damage</p><p>　　Tool damage can be classi

35、fied into two groups, wear and fracture, by means of its scale and how it progresses. Wear (as discussed in Chapter 2) is loss of material on an asperity or micro-contact, or smaller scale, down to molecular or atomic re

36、moval mechanisms. It usually progresses continuously. Fracture, on the other hand, is damage at a larger scale than wear; and it occurs suddenly. As written above, there is a continuous spectrum of damage scales from mic

37、ro-wear to gross fracture.</p><p>　　Figure 4.1 shows a typical damage pattern – in this case wear – of a carbide tool, cutting steel at a relatively high speed. Crater wear on the rake face, flank wear on th

38、e flank faces and notch wear at the depth of cut (DOC) extremities are the typical wear modes. Wear measures, such as VB, KT are returned to in Section 4.2.</p><p>　　Damage changes, however, with change of m

39、aterials, cutting mode and cutting condi- tions, as shown in Figure 4.2. Figure 4.2(a) shows crater and flank wear, with negligible notch wear, after turning a medium carbon steel with a carbide tool at high cutting spee

40、d. If the process is changed to milling, a large crater wear with a number of cracks becomes the distinctive feature of damage (Figure 4.2(b)). When turning Ni-based super alloys with ceramic tools (Figure 4.2(c)) notch

41、wear at the DOC lin</p><p>　　4.1.2 Causes of tool damage</p><p>　　Chapter 2.4 outlined the general conditions leading to abrasive, adhesive and chemical wear mechanisms. In the context of cutti

42、ng tool damage, the importance and occurrence of these mechanisms can be classified by cutting temperature, as shown in Figure 4.3. Three causes of damage are qualitatively identified in the figure: mechanical, thermal

43、 and adhesive. Mechanical damage, which includes abrasion, chipping, early fracture and fatigue, is basi- cally independent of temperature. Thermal damag</p><p>　　Mechanical damage</p><p>　　Whet

44、her mechanical damage is classified as wear or fracture depends on its scale. Figure 4.4 illustrates the different modes, from a scale of less than 0.1 ?m to around 100 ?m (much greater than 100 ?m becomes failure).<

45、;/p><p>　　Abrasive wear (illustrated schematically in Figure 2.29) is typically caused by sliding hard particles against the cutting tool. The hard particles come from either the work mater- ial’s microstructur

46、e, or are broken away from the cutting edge. Abrasive wear reduces the harder is the tool relative to the particles and generally depends on the distance cut (see Section 4.2.2).</p><p>　　Attrition wear occu

47、rs on a scale larger than abrasion. Particles or grains of the tool material are mechanically weakened by micro-fracture as a result of sliding interaction with the work, before being removed by wear.</p><p>

48、;　　Next in size comes chipping (sometimes called micro-chipping at its small-scale limit). This is caused by mechanical shock loading on a scale that leads to large fluctuations in cutting force, as opposed to the inhere

49、nt local stress fluctuations that cause attrition.</p><p>　　Finally, fracture is larger than chipping, and is classified into three types: early stage, unpredictable and final stage. The early stage occurs i

50、mmediately after beginning a cut if the tool shape or cutting condition is improper; or if there is some kind of defect in the cutting tool or in its edge preparation. Unpredictable fracture can occur at any time if the

51、stress on the cutting edge changes suddenly, for example caused by chattering or an irreg- ularity in the workpiece hardness. Final s</p><p>　　Thermal damage – plastic deformation</p><p>　　The p

52、lastic deformation type of thermal damage referred to in Figure 4.3 is observed when a cutting tool at high cutting temperature cannot withstand the compressive stress on its cutting edge. It therefore occurs with tools

53、having a high temperature sensitivity of their hardness as their weakest characteristic. Examples are high speed steel tools in general; and high cobalt content cemented carbide tools, or cermet tools, used in severe con

54、ditions, particularly at a high feed rate. Deformation </p><p>　　Thermal damage – diffusion</p><p>　　Wear as a result of thermal diffusion occurs at high cutting temperatures if cutting tool and

55、 work material elements diffuse mutually into each other’s structure. This is well known with cemented carbide tools and has been studied over many years, by Dawihl (1941), Trent (1952), Trigger and Chao (1956), Takeyama

56、 and Murata (1963), Gregory (1965), Cook (1973), Uehara (1976), Narutaki and Yamane (1976), Usui et al. (1978) and others. The rates of processes controlled by diffusion are exponentially</p><p>　　igure 4.5

57、shows experimental results for both the crater and flank depth wear rates of a 0.25%C and a 0.46%C steel turned by a P20 grade carbide tool, plotted after the manner of equation (4.1c). Two linear regions are seen: in th

58、is case the boundary is at 1/??≈ 8.5 10–4 K–1 (or ??≈ 1175 K). The slope of the higher temperature data (??> 1175 K) is typi- cal of diffusion processes between steels and cemented carbides (Cook, 1973). The smaller

59、 slope at lower temperatures is typical of a </p><p>　　Diffusion can be directly demonstrated at high temperatures in static conditions. Figure 4.6 shows a typical result of a static diffusion test i

60、n which a P-grade cemented carbide tool was loaded against a 0.15% carbon steel for 30 min at 1200?C. A metallographic section through the interface between the carbide tool and the steel, etched in 4% Nital (nitric acid

61、 and alcohol) shows that the pearlite in the steel has increased from its original level. This means that carbon from the cemented carbi</p><p>　　Naerheim and Trent (1977) have proposed that the wear rates o

62、f both WC-Co (K-grade) and WC-(Ti,Ta,W)C-Co (P-grade) cemented carbides are controlled by the rate of diffusion of tungsten (and Ti and Ta) and carbon atoms together into the work material, as indicated in Figure 4.7. Th

63、is view is based on transmission electron microscope (TEM) observations on crater wear that show no structural changes in the tool’s carbide grains within a distance of 0.01 ?m of the tool–chip interface. The slower wea&

64、lt;/p><p>　　Other examples of diffusion wear are the severe wear of diamond cutting tools, silicon nitride ceramic tools and SiC whisker reinforced alumina ceramic tools when machining steel. Carbon, silicon an

65、d nitrogen all diffuse easily in iron at elevated temperatures; and silicon nitride and silicon carbide dissolve readily in hot iron.</p><p>　　Thermal diffusion wear of carbide tools can be decreased if a la

66、yer acting as a barrier to diffusion is deposited on the tool. There are two types of layer in practice: one is as provided by coated tools; the other is a protective oxide layer deposited on the wear surfaces during cut